JP7385160B2 - steel material - Google Patents

Description

The present disclosure relates to a steel material, and more particularly to a steel material suitable as a material for mechanical structural parts manufactured by performing gas carburizing treatment.

In this specification, gas carburizing treatment also includes gas carbonitriding treatment. Further, in this specification, gas carburizing treatment includes a gas carburizing process (including a gas carbonitriding process) and a quenching process after the gas carburizing process.

Machine structural parts are typified by, for example, gears and shafts for automobiles, construction vehicles, and the like. As mechanical structural parts, mechanical structural alloy steel materials such as SCr420, SCM420, and SNCM420 specified in JIS G 4053 (2016) are used.

These steel materials are manufactured into mechanical structural parts, for example, through the following manufacturing process. A steel material is subjected to forging (hot forging or cold forging) and/or cutting to produce an intermediate product having a desired shape. Heat treatment (quenching and tempering, carburizing treatment, carbonitriding treatment, etc.) is performed on the intermediate product to adjust the hardness and microstructure of the intermediate product. Through the above manufacturing process, a mechanical structural component is manufactured.

As mentioned above, during the manufacturing process of mechanical structural parts, cutting may be performed on steel materials. Therefore, high machinability is required of steel materials that are used as raw materials for mechanical structural parts.

In recent years, mechanical structural parts have been made lighter and smaller with the aim of improving the fuel efficiency of automobiles, construction vehicles, and the like. Therefore, mechanical structural parts are required to have excellent bending fatigue strength and surface fatigue strength.

Gas carburizing treatment and gas carbonitriding treatment are known as methods for increasing the bending fatigue strength and surface fatigue strength of mechanical structural parts. In gas carburizing treatment and gas carbonitriding treatment, a hardened layer (carburized layer or carbonitrided layer) is formed on the surface layer of mechanical structural parts. This hardened layer improves the bending fatigue strength and surface fatigue strength of mechanical structural parts.

By the way, when gas carburizing treatment (gas carburizing treatment and gas carbonitriding treatment) is performed, mechanical structural parts are likely to be deformed. In this specification, deformation of mechanical structural parts during gas carburizing treatment is referred to as heat treatment deformation. Heat treatment deformation distorts the shape of mechanical structural parts. Distortion of the shape of mechanical structural parts causes noise and vibration during operation of automobiles, construction vehicles, and the like. Therefore, there is a need for a steel material that can suppress heat treatment deformation when gas carburizing treatment is performed.

Techniques related to suppressing heat treatment deformation are proposed in JP-A-9-137266 (Patent Document 1) and JP-A-11-50191 (Patent Document 2).

The steel material disclosed in Patent Document 1 has, in mass%, C: 0.03 to 0.40%, Mn: 2.0% or less, Si: 2.0% or less, and Al: 0.015 to 0.06. %, N: 0.005 to 0.03%, P: 0 to 0.030%, balance: Fe and inevitable impurities. Furthermore, in this steel material, when the quenching start temperature in quenching performed after surface hardening treatment of parts molded using this steel material is T _A , T _A is T1 (=788-117 x [C] + 29 ×[Si]-14×[Mn]) and not more than T2 (=900-387×[C]+63×[Si]-18×[Mn]), and furthermore, Heq ₁ (=[C] The chemical composition is adjusted so that +0.12×[Si]+0.13×[Mn]) is 0.33 or more.

In Patent Document 1, with the above configuration, the area fraction of pro-eutectoid ferrite in the structure of the core of a mechanical structural component after carburization is set to 20 to 80%. As a result, heat treatment deformation of the steel material is suppressed.

However, in the mechanical structural component of Patent Document 1, the mechanical structural component may have low bending fatigue strength.

The carburized shaft-shaped part disclosed in Patent Document 2 has, in mass%, C: 0.10 to 0.35%, Si: 0.02 to 0.50%, Mn: 0.30 to 1.80%, S: 0.005-0.15%, Al: 0.015-0.040%, Nb: 0.005-0.040%, N: 0.0060-0.0200%, P: 0.025% The following contains Ti: 0.01% or less, O: 0.0025% or less, and further contains Cr: 0.40-1.80%, Mo: 0.02-1.0%, Ni: 0.1 ~3.5%, V: 0.03~0.5%, and the remainder consists of iron and inevitable impurities. In this carburized shaft-shaped part, Nb(CN), AlN, or composite precipitates of Nb(CN) and AlN with a diameter of 0.1 μm or less are dispersed in a total of 80 pieces/100 μm2 ^{or more} , and the austenite grain size is is number 8 or higher.

In Patent Document 2, coarse grains are suppressed during carburizing treatment. As a result, heat treatment deformation of the steel material is suppressed.

In the carburized shaft-shaped component of Patent Document 2, it is thought that heat treatment deformation is suppressed to some extent during gas carburizing treatment. However, in order to suppress noise and vibration during operation of automobiles, construction vehicles, etc., there may be steel materials whose heat treatment deformation can be suppressed by other means.

Techniques for suppressing heat treatment deformation by means different from Patent Document 1 and Patent Document 2 are disclosed in International Publication No. 2014/038548 (Patent Document 3), Japanese Patent Application Publication No. 2013-108144 (Patent Document 4), and Japanese Patent Application Publication No. 2013-151719. This method is proposed in Japanese Patent Application Publication No. 2003-100000 (Patent Document 5).

The steel material disclosed in Patent Document 3 has, in mass%, C: 0.20 to 0.30%, Si: 0.10 to 1.50%, Mn: 0.10 to 1.20%, and P: 0. .030% or less, S: 0.030% or less, Cr: 1.30 to 2.50%, Cu: 0.30% or less, Al: 0.008 to 0.300%, O: 0.0030% or less , N: 0.0020 to 0.0300%, and the remainder consists of Fe and inevitable impurities. In this steel material, the martensitic transformation start temperature (Ms point) is 460° C. or lower. Furthermore, the hardness at a distance of 1.5 mm from the quenched end of the steel measured by the Jominy single end quenching method is defined as J1.5, and the hardness at a distance of 9 mm from the quenched end of the steel material is defined as J1.5. When the hardness is defined as J9 and the hardness at a position 11 mm from the quenched end is defined as J11, (J9/J1.5) is 0.70 to 0.85, and (J11/J1. 5) is 0.67 to 0.78.

In the steel material disclosed in Patent Document 3, the Ms point is set low and the hardness is adjusted within a predetermined range. Thereby, heat treatment deformation of the steel material is suppressed.

The steel material disclosed in Patent Document 4 has, in mass%, C: 0.10 to 0.25%, Si: 0.01 to 0.10%, Mn: 0.40 to 1.00%, and S: 0. .003 to 0.050%, Cr: 1.60 to 2.00%, Mo: 0 to 0.10%, Al: 0.025 to 0.050%, N: 0.0100 to 0.0250%. The remainder consists of Fe and impurities, and P, Ti, and O (oxygen) in the impurities are respectively P: 0.025% or less, Ti: 0.003% or less, and O: 0.0020% or less. . Further, in this steel material, fn (=Cr+2×Mo) is 1.82 to 2.10. Furthermore, in this steel material, the difference value between the maximum value and the minimum value of the Ms point at 17 measurement positions in a cross section perpendicular to the longitudinal direction of the steel material is 10 or less.

The steel material disclosed in Patent Document 5 has, in mass%, C: 0.1 to 0.3%, Si: 0.01 to 0.6%, Mn: 0.4 to 1.0%, and S: 0. .003 to 0.05%, Cr: 0.80 to 2.00%, Mo: 0 to 0.50%, Al: 0.01 to 0.05%, and N: 0.010 to 0.025 %, the remainder consists of Fe and impurities, and P, Ti, and O in the impurities are P: 0.025% or less, Ti: 0.003% or less, and O: 0.002% or less. be. Furthermore, in this steel material, the difference value between the maximum value and the minimum value of the Ms point at 17 measurement positions on a cross section perpendicular to the longitudinal direction of the steel material is 10 or less. The microstructure of this steel material consists of ferrite, pearlite, and/or bainite. Furthermore, in this steel material, the ratio between the maximum value and the minimum value of the average grain size of ferrite in the cross section is 2.0 or less.

In Patent Document 4 and Patent Document 5, variations in the Ms point in the cross section of the steel material are suppressed. As a result, heat treatment deformation of the steel material is suppressed.

Japanese Patent Application Publication No. 9-137266 Japanese Patent Application Publication No. 11-50191 International Publication No. 2014/038548 Japanese Patent Application Publication No. 2013-108144 Japanese Patent Application Publication No. 2013-151719

However, the bending fatigue strength and the surface fatigue strength may be increased and heat treatment deformation may be suppressed by means other than Patent Documents 3 to 5.

The purpose of the present disclosure is to provide a steel material that has excellent machinability, has excellent bending fatigue strength and surface fatigue strength after gas carburizing treatment, and can suppress heat treatment deformation after gas carburizing treatment. The goal is to provide the following.

The steel material of the present disclosure has the following configuration.

A steel material,
The chemical composition is in mass%,
C: 0.20-0.25%,
Si: 0.40 to 0.70%,
Mn: 0.50-0.90%,
Cr: 1.00-2.00%,
S: 0.005-0.050%,
N: 0.0050-0.0200%,
Al: 0.001-0.100%,
O: 0.0050% or less, and
P: Contains 0.030% or less,
the remainder consists of Fe and impurities, and satisfies formula (1),
In a cross section that is perpendicular to the longitudinal direction of the steel material and has a circular shape with a radius R,
The center position of the cross section, and the eight R/2 positions that are R/2 positions in the radial direction from the center of the cross section and are arranged at a pitch of 45° around the center of the cross section, When defined as nine cross-sectional observation positions,
The microstructure at each cross-sectional observation position contains ferrite, and the remainder consists of pearlite and/or bainite,
The arithmetic mean value of the area fraction of ferrite at the nine cross-sectional observation positions is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less,
Among the average grain sizes of ferrite at the nine cross-sectional observation positions, the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less,
In a longitudinal section that is parallel to the longitudinal direction of the steel material and includes the central axis of the steel material,
Three center axis positions arranged at an R/2 pitch on the center axis, and six R/2 positions arranged at R/2 positions in the radial direction from each center axis position. , when defined as nine longitudinal section observation positions,
The microstructure at each longitudinal section observation position contains ferrite, and the remainder consists of pearlite and/or bainite,
The arithmetic mean value of the area fraction of ferrite at the nine longitudinal section observation positions is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less,
Among the average grain sizes of ferrite at the nine longitudinal cross-sectional observation positions, the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less,
Steel material.
1-(0.5C+0.03Si+0.06Mn+0.01Cr+0.05Mo)<0.800 (1)
Here, the content (mass %) of the corresponding element is substituted for each element symbol in formula (1). If the corresponding element is not contained, "0" is assigned to the element symbol.

The steel material according to the present disclosure has excellent machinability, has excellent bending fatigue strength and surface fatigue strength after gas carburizing treatment, and can suppress heat treatment deformation after gas carburizing treatment.

FIG. 1 is a diagram showing the relationship between the F1 (=1-(0.5C+0.03Si+0.06Mn+0.01Cr+0.05Mo)) value and the maximum deformation amount ratio (%). FIG. 2 is a schematic cross-sectional view of the steel material of this embodiment, which is a cross section perpendicular to the longitudinal direction. FIG. 3 is a schematic diagram of a longitudinal section of the steel material of this embodiment, which is parallel to the longitudinal direction and includes the central axis. FIG. 4 is a schematic diagram of the band structure. FIG. 5 is a diagram showing an example of a heat pattern of a gas carburizing process and a quenching process. FIG. 6 is a plan view of the Ono rotary bending test piece prepared in the example. FIG. 7 is a plan view of a test piece for a roller pitting fatigue test prepared in an example. FIG. 8 is a schematic diagram for explaining a roller pitching fatigue test. FIG. 9 is a front view of a large roller test piece prepared in an example. FIG. 10A is a perspective view of a gear simulating test piece produced in an example. FIG. 10B is a perspective view of the through hole in FIG. 10A.

The present inventors have discovered that the present inventors have excellent machinability, have excellent bending fatigue strength and surface fatigue strength when gas carburizing is performed, and have excellent bending fatigue strength and surface fatigue strength. We investigated and studied steel materials that can suppress heat treatment deformation.

The present inventors first studied a steel material that has excellent machinability and also has excellent bending fatigue strength and surface fatigue strength after gas carburizing treatment from the viewpoint of chemical composition.

As a result of the study, the chemical composition, in mass%, was C: 0.20 to 0.25%, Si: 0.40 to 0.70%, Mn: 0.50 to 0.90%, Cr: 1.00. ~2.00%, S: 0.005~0.050%, N: 0.0050~0.0200%, Al: 0.001~0.100%, O: 0.0050% or less, P: 0 .030% or less, Mo: 0 to 0.30%, Nb: 0 to 0.050%, Ti: 0 to 0.020%, Cu: 0 to 0.50%, Ni: 0 to 0.80%, Steel material containing V: 0 to 0.30%, Mg: 0 to 0.0035%, Ca: 0 to 0.0030%, and rare earth elements: 0 to 0.0050%, with the balance consisting of Fe and impurities. If so, it was thought that it would have excellent machinability and, furthermore, could have excellent bending fatigue strength and surface fatigue strength after gas carburizing treatment.

The present inventors further investigated means for suppressing heat treatment deformation after gas carburizing treatment. The present inventors focused on the microstructure of steel materials. If the microstructure in each part of the steel material is as uniform as possible, specifically, if the variation in the phase composition of the microstructure and the variation in crystal grains in each part of the steel material are suppressed, gas Variations in the timing of martensitic transformation during carburizing and quenching can be suppressed. As a result, heat treatment deformation can be suppressed. Therefore, the present inventors investigated the phase structure and crystal grain size at each location of the steel material.

The present inventors first focused on variations in the microstructure in a cross section that is a cross section perpendicular to the longitudinal direction of the steel material. In order to quantify the microstructure variation in the cross section, the cross section observation position, which is the observation position of the microstructure in the cross section, was defined as follows.

When the radius of the cross section of the steel material is R, the center position of the cross section and the position R/2 in the radial direction from the center of the cross section, and are arranged at a pitch of 45° around the center of the cross section. The R/2 positions of the locations are defined as the cross-sectional observation positions of the nine locations.

The present inventors investigated and examined the microstructure at each cross-sectional observation position. As a result of the study, it was found that heat treatment deformation after gas carburizing treatment can be suppressed if the microstructure at the cross-sectional observation position satisfies the following requirements.
(1) The microstructure at each cross-sectional observation position contains ferrite, and the remainder consists of pearlite and/or bainite.
(2) The arithmetic mean value of the area fraction of ferrite at nine cross-sectional observation positions is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less.
(3) Among the average grain sizes of ferrite at nine cross-sectional observation positions, the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less.

However, even with steel materials having the above-mentioned chemical composition and satisfying the above-mentioned microstructure, heat treatment deformation is still not sufficiently suppressed, and especially noise and vibration during operation of automobiles and construction vehicles, etc. It has been found that there are cases where it is not possible to suppress the effects sufficiently. Therefore, the present inventors conducted further investigation.

As a result, the following items were found. In order to suppress noise and vibration during operation, it is effective to suppress three-dimensional heat treatment deformation of steel materials. As described above, heat treatment deformation in the direction perpendicular to the longitudinal direction of the steel material can be suppressed by suppressing variations in the phase structure and crystal grains of the microstructure in the cross section of the steel material.

However, simply suppressing variations in the microstructure in the cross section of the steel material only suppresses two-dimensional heat treatment deformation. In other words, even if variations in the microstructure in the cross section of the steel material are suppressed, the microstructure in the longitudinal section, which is a cross section parallel to the longitudinal direction of the steel material and including the central axis of the steel material, may vary. In this case, variations occur in heat treatment deformation. As a result, noise and vibration during operation cannot be sufficiently suppressed.

Therefore, the present inventors focused on not only the variation in the microstructure of the cross section of the steel material but also the variation of the microstructure of the longitudinal section of the steel material. In order to quantify the variation in the microstructure in the longitudinal section, the longitudinal section observation position, which is the observation position of the microstructure in the longitudinal section, was defined as follows.

The three central axis positions arranged at an R/2 pitch on the central axis of the steel material and the six R/2 positions arranged at R/2 positions in the radial direction from each central axis position are 9. Defined as the vertical section observation position of a location.

The present inventors investigated and examined the microstructure at each longitudinal section observation position. As a result of the study, it was found that if the microstructure at the cross-sectional observation position satisfies the above requirements and the microstructure at the longitudinal cross-section observation position satisfies the following requirements, heat treatment deformation after gas carburizing treatment can be sufficiently suppressed. There was found.
(4) The microstructure at each vertical section observation position contains ferrite, and the remainder consists of pearlite and/or bainite.
(5) The arithmetic mean value of the area fraction of ferrite at nine longitudinal section observation positions is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less.
(6) Among the average grain sizes of ferrite at nine longitudinal cross-sectional observation positions, the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less.

However, even if the steel material has the above chemical composition and the microstructure at the cross-sectional observation position and the longitudinal cross-section observation position satisfies the above requirements (1) to (6), it still cannot sufficiently resist heat treatment deformation. There were times when it could not be suppressed. Therefore, the present inventors conducted further investigation.

Here, the present inventors focused on martensitic transformation after gas carburizing treatment. Then, the present inventors conducted a detailed study on the mechanism of occurrence of martensitic transformation during gas carburizing and quenching.

In all of the above-mentioned Patent Documents 3 to 5, heat treatment deformation is suppressed by suppressing variations in the transformation timing of martensite depending on each location in the steel material during gas carburizing and quenching. Specifically, in Patent Document 3, by setting the Ms point to 460° C. or lower, the martensitic transformation timing is prevented from shifting significantly in each part of the steel material. In Patent Documents 4 and 5, by suppressing variations in the Ms point in each part of the steel material, the martensitic transformation timing is prevented from shifting significantly in each part of the steel material.

Therefore, the present inventors first used a steel material having the above-mentioned chemical composition and, as in Patent Documents 3 to 5, set the martensitic transformation timing at each part of the steel material to be the same, thereby reducing heat treatment deformation. tried to suppress it. Specifically, heat treatment deformation can be suppressed by suppressing variations in the microstructure at each location of the steel material (cross-sectional observation position, longitudinal section observation position), and by suppressing variation in the Ms point at each location as much as possible. I tried.

However, as a result of the investigation conducted by the present inventors, even if the variation in the microstructure in each part of the steel material with the above-mentioned chemical composition is suppressed, the martensitic transformation timing in each part of the steel material inevitably deviates slightly. It turned out that it is extremely difficult to achieve martensitic transformation at the same time. Specifically, if the rapid cooling time in gas carburizing treatment is divided into minute periods, even if the variation in the microstructure at the cross-sectional observation position and longitudinal cross-sectional observation position of the steel material is minimized, , a minute time period in which a part undergoing martensitic transformation (hereinafter also referred to as "martensite transformed part") and a part not undergoing martensitic transformation (hereinafter also referred to as "martensitic untransformed part") coexist. It turns out that bands inevitably occur.

Microstructural changes in steel materials during vacuum carburizing treatment are thought to occur as follows.
When the quenching time (quenching time) is divided into minute periods, martensitic transformation begins in a part of the interior of the steel material. Thereafter, as time progresses, martensitic transformation progresses from the central portion toward the surface layer. In other words, martensitic transformation occurs not from the surface layer of the steel material but from within the steel material.

Due to the gas carburizing treatment, the carbon concentration on the surface layer of the steel material is higher than the carbon concentration inside the steel material. Therefore, the Ms point of the surface layer of the steel material is lower than the Ms point inside the steel material. Furthermore, even if it is possible to make the Ms point uniform at each location inside the steel material, the cooling rate at each location will not be completely the same due to the shape of the steel material. Therefore, when the quenching time is divided into minute periods, martensitic transformation starts from the part where the cooling rate inside the steel material is fast among the parts of the steel material. Therefore, during quenching in the gas carburizing process, a minute period in which martensite-transformed portions and martensite-untransformed portions coexist always occurs.

Based on the above findings, the present inventors decided to use gas carburizing instead of suppressing heat treatment deformation by keeping the martensitic transformation timing as similar as possible, as in the technical ideas disclosed in Patent Documents 3 to 5. We investigated means for suppressing heat treatment deformation on the premise that there is always a minute time period in which martensite-transformed portions and martensite-untransformed portions coexist.

During quenching, the untransformed martensite portion is softer than the martensite transformed portion. Furthermore, the martensitic transformed portion having a body-centered cubic lattice structure has a larger volume than the martensitic untransformed portion having a face-centered cubic lattice structure. Therefore, when a portion of the steel material undergoes martensitic transformation during quenching, and a martensite-transformed portion and a martensite-untransformed portion coexist, distortion occurs in the martensite-untransformed portion. This distortion is thought to cause heat treatment deformation.

Therefore, the present inventors have determined that, on the premise that during gas carburizing treatment, there is a minute period in which martensite-transformed portions and martensite-untransformed portions coexist, at the time when martensite-transformed portions are generated, It was thought that if the strength of the untransformed martensite portion of the steel sheet could be maintained high, the occurrence of distortion in the untransformed martensite portion could be suppressed, and as a result, heat treatment deformation could be suppressed.

Therefore, the present inventors further investigated a means for maintaining high strength of the martensite-untransformed portion when the martensite-transformed portion is generated during quenching in gas carburizing treatment. In steel materials having the above chemical composition, in order to increase the strength of the untransformed martensite portion in the temperature range where the martensitic transformed portion is generated, it is necessary to strengthen the untransformed martensite portion in the temperature range where the martensitic transformed portion is generated. It is effective to appropriately contain elements that

In the above chemical composition, the present inventors believe that C, Si, Mn, Cr, and Mo are effective as elements that increase the strength of the untransformed martensite portion in the temperature range where the martensitic transformed portion is generated. . Therefore, we further investigated the relationship between these elements and the amount of heat treatment deformation during quenching in gas carburizing treatment. As a result, it was found that heat treatment deformation can be significantly suppressed when the following formula (1) is further satisfied in the steel material having the above-mentioned chemical composition.
1-(0.5C+0.03Si+0.06Mn+0.01Cr+0.05Mo)<0.800 (1)
Here, the content (mass %) of the corresponding element is substituted for each element symbol in formula (1). If the corresponding element is not contained, "0" is assigned to the element symbol.

Define F1=1-(0.5C+0.03Si+0.06Mn+0.01Cr+0.05Mo). Figure 1 shows the F1 value and the maximum value for steel materials whose chemical composition contains each element within the above-mentioned range, and whose microstructure variations at the cross-sectional observation position and the longitudinal-sectional observation position satisfy the above-mentioned requirements. It is a figure which shows the relationship with a deformation amount ratio (%). The maximum deformation amount ratio is an index of heat treatment deformation. The larger the maximum deformation amount ratio, the larger the heat treatment deformation of the steel material. The maximum deformation amount ratio was determined by the method described below.

Referring to FIG. 1, the content of each element in the chemical composition is within the above-mentioned range, and the microstructure at the cross-sectional observation position and longitudinal section observation position satisfies the above-mentioned conditions (1) to (6). For steel materials that meet the requirements, the maximum deformation ratio decreases as F1 decreases. When F1 becomes less than 0.800, the maximum deformation amount ratio decreases significantly. In other words, the maximum deformation amount ratio to F1 has an inflection point near F1=0.800. Therefore, if F1 is less than 0.800, heat treatment deformation of the steel material during carburizing and quenching can be sufficiently suppressed.

As described above, the present inventors have succeeded in suppressing the variation in the microstructure at the cross-sectional observation position and the longitudinal-sectional observation position in steel materials having the above-mentioned chemical composition, and thereby suppressing the variation in the timing of occurrence of martensitic transformation during quenching to some extent. However, by setting F1 to less than 0.800, on the premise that a minute period in which martensite-transformed portions and martensite-untransformed portions coexist during quenching, excellent machinability can be achieved. It has been found that it has excellent bending fatigue strength and excellent surface fatigue strength after gas carburizing treatment, and can sufficiently suppress heat treatment deformation after gas carburizing treatment.

The steel material according to this embodiment, which was completed based on the above knowledge, has the following configuration.

[1]
A steel material,
The chemical composition is in mass%,
C: 0.20-0.25%,
Si: 0.40 to 0.70%,
Mn: 0.50-0.90%,
Cr: 1.00-2.00%,
S: 0.005-0.050%,
N: 0.0050-0.0200%,
Al: 0.001-0.100%,
O: 0.0050% or less, and
P: Contains 0.030% or less,
the remainder consists of Fe and impurities, and satisfies formula (1),
In a cross section that is perpendicular to the longitudinal direction of the steel material and has a circular shape with a radius R,
The center position of the cross section, and the eight R/2 positions that are R/2 positions in the radial direction from the center of the cross section and are arranged at a pitch of 45° around the center of the cross section, When defined as nine cross-sectional observation positions,
The microstructure at each cross-sectional observation position contains ferrite, and the remainder consists of pearlite and/or bainite,
The arithmetic mean value of the area fraction of ferrite at the nine cross-sectional observation positions is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less,
Among the average grain sizes of ferrite at the nine cross-sectional observation positions, the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less,
In a longitudinal section that is parallel to the longitudinal direction of the steel material and includes the central axis of the steel material,
Three center axis positions arranged at an R/2 pitch on the center axis, and six R/2 positions arranged at R/2 positions in the radial direction from each center axis position. , when defined as nine longitudinal section observation positions,
The microstructure at each longitudinal section observation position contains ferrite, and the remainder consists of pearlite and/or bainite,
The arithmetic mean value of the area fraction of ferrite at the nine longitudinal section observation positions is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less,
Among the average grain sizes of ferrite at the nine longitudinal cross-sectional observation positions, the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less,
Steel material.
1-(0.5C+0.03Si+0.06Mn+0.01Cr+0.05Mo)<0.800 (1)
Here, the content (mass %) of the corresponding element is substituted for each element symbol in formula (1). If the corresponding element is not contained, "0" is assigned to the element symbol.

[2]
The steel material according to [1],
The chemical composition further includes, in place of a portion of the Fe,
Mo: 0.30% or less,
Nb: 0.050% or less,
Ti: 0.020% or less,
Cu: 0.50% or less,
Ni: 0.80% or less,
V: 0.30% or less,
Mg: 0.0035% or less,
Ca: 0.0030% or less, and
Rare earth element: Contains one or more elements selected from the group consisting of 0.0050% or less,
Steel material.

Hereinafter, the steel material of this embodiment will be explained in detail. "%" with respect to elements means mass % unless otherwise specified.

The chemical composition of the steel material of this embodiment contains the following elements.

C: 0.20-0.25%
Carbon (C) increases the strength of steel materials. If the C content is less than 0.20%, the above effects cannot be sufficiently obtained even if the contents of other elements are within the range of this embodiment.
On the other hand, if the C content exceeds 0.25%, the hardenability becomes excessively high even if the contents of other elements are within the range of this embodiment. In this case, the steel material after gas carburizing becomes hard. As a result, the machinability of the steel material decreases.
Therefore, the C content is 0.20-0.25%.
The lower limit of the C content is preferably 0.21%, more preferably 0.22%.
A preferable upper limit of the C content is 0.24%, more preferably 0.23%.

Si: 0.40~0.70%
Silicon (Si) improves the hardenability of steel materials and increases the strength of steel materials. Si further increases the temper softening resistance of the hardened layer of mechanical structural parts. Therefore, the surface fatigue strength of mechanical structural parts increases. If the Si content is less than 0.40%, the above effects cannot be sufficiently obtained even if the contents of other elements are within the range of this embodiment.
On the other hand, if the Si content exceeds 0.70%, even if the contents of other elements are within the range of this embodiment, the grain boundary oxidation layer after gas carburizing becomes excessively deep. In this case, the bending fatigue strength of the mechanical structural parts decreases.
Therefore, the Si content is 0.40-0.70%.
The lower limit of the Si content is preferably 0.41%, more preferably 0.42%, even more preferably 0.45%, even more preferably 0.47%, and even more preferably 0.50%. %.
A preferable upper limit of the Si content is 0.69%, more preferably 0.67%, still more preferably 0.65%, and still more preferably 0.63%.

Mn: 0.50-0.90%
Manganese (Mn) improves the hardenability of steel materials and increases the bending fatigue strength and surface fatigue strength of mechanical structural parts. If the Mn content is less than 0.50%, the above effects cannot be sufficiently obtained even if the contents of other elements are within the range of this embodiment.
On the other hand, if the Mn content exceeds 0.90%, even if the content of other elements is within the range of this embodiment, the formation of Mn oxides will be promoted on the surface layer of mechanical structural parts during gas carburizing treatment. be done. In this case, the grain boundary oxidation layer of the mechanical structural component becomes excessively deep. Therefore, the bending fatigue strength of mechanical structural parts decreases. Mn oxide formed on the surface layer of mechanical structural parts further causes surface-originated peeling. If surface-originated peeling occurs, the surface fatigue strength of mechanical structural parts will decrease.
Therefore, the Mn content is 0.50-0.90%.
The lower limit of the Mn content is preferably 0.51%, more preferably 0.52%, even more preferably 0.55%, and still more preferably 0.60%.
A preferable upper limit of the Mn content is 0.89%, more preferably 0.87%, and still more preferably 0.85%.

Cr:1.00~2.00%
Chromium (Cr) improves the hardenability of steel materials and increases the bending fatigue strength and surface fatigue strength of mechanical structural parts. If the Cr content is less than 1.00%, the above effects cannot be sufficiently obtained even if the contents of other elements are within the range of this embodiment.
On the other hand, if the Cr content exceeds 2.00%, the steel material becomes too hard even if the contents of other elements are within the range of this embodiment. In this case, the machinability of the steel material decreases.
Therefore, the Cr content is 1.00-2.00%.
The preferable lower limit of the Cr content is 1.10%, more preferably 1.20%, even more preferably 1.40%, still more preferably 1.60%, even more preferably 1.70%. %, more preferably 1.80%.
A preferable upper limit of the Cr content is less than 2.00%, more preferably 1.95%, and still more preferably 1.90%.

S: 0.005-0.050%
Sulfur (S) combines with Mn to form MnS. MnS improves the machinability of steel materials. If the S content is less than 0.005%, the above effects cannot be sufficiently obtained even if the contents of other elements are within the range of this embodiment.
On the other hand, if the S content exceeds 0.050%, an excessive amount of MnS will be formed even if the contents of other elements are within the range of this embodiment. In this case, the bending fatigue strength and surface fatigue strength of the mechanical structural parts decrease.
Therefore, the S content is 0.005 to 0.050%.
The preferable lower limit of the S content is 0.007%, more preferably 0.010%, still more preferably 0.013%, and still more preferably 0.015%.
A preferable upper limit of the S content is 0.049%, more preferably 0.045%, even more preferably 0.040%, still more preferably 0.035%, and even more preferably 0.025%. %.

N: 0.0050-0.0200%
Nitrogen (N) combines with Al and Nb to form AlN and NbN. AlN and NbN suppress coarsening of crystal grains during heating during gas carburizing treatment due to the pinning effect. If the N content is less than 0.0050%, the above effects cannot be sufficiently obtained even if the contents of other elements are within the range of this embodiment.
On the other hand, if the N content exceeds 0.0200%, even if the content of other elements is within the range of this embodiment, defects are likely to occur on the surface of the manufactured slab or ingot during the steelmaking process. .
Therefore, the N content is 0.0050-0.0200%.
The preferable lower limit of the N content is 0.0100%, more preferably 0.0120%, and still more preferably 0.0130%.
The upper limit of the N content is preferably less than 0.0200%, more preferably 0.0190%, even more preferably 0.0180%, and still more preferably 0.0150%.

Al: 0.001-0.100%
Aluminum (Al) deoxidizes steel. Al further combines with N to form AlN. Due to the pinning effect, AlN suppresses coarsening of crystal grains during heating during gas carburizing treatment. If the Al content is less than 0.001%, the above effects cannot be sufficiently obtained even if the contents of other elements are within the range of this embodiment.
On the other hand, if the Al content exceeds 0.100%, the formation of coarse Al oxides is promoted even if the contents of other elements are within the range of this embodiment. Coarse Al oxide reduces the bending fatigue strength of mechanical structural parts.
Therefore, the Al content is 0.001 to 0.100%.
The preferable lower limit of the Al content is 0.020%, more preferably 0.025%, still more preferably 0.027%, and even more preferably 0.030%.
A preferable upper limit of the Al content is 0.090%, more preferably 0.070%, even more preferably 0.050%, still more preferably 0.045%, and even more preferably 0.040%. %, more preferably 0.035%.

O (oxygen): 0.0050% or less Oxygen (O) is an impurity. O combines with other elements in the steel material to form coarse oxide-based inclusions. Coarse oxide inclusions reduce the bending fatigue strength of mechanical structural parts. If the O content exceeds 0.0050%, even if the contents of other elements are within the ranges of this embodiment, the bending fatigue strength of the mechanical structural component will decrease significantly.
Therefore, the O content is 0.0050% or less.
It is preferable that the O content is as low as possible. However, excessive reduction in O content increases manufacturing costs. Therefore, when considering normal industrial production, the preferable lower limit of the O content is more than 0%, more preferably 0.0001%, still more preferably 0.0005%, and still more preferably 0.0010%. %.
The upper limit of the O content is preferably 0.0040%, more preferably 0.0030%, even more preferably 0.0020%, and still more preferably 0.0015%.

P: 0.030% or less Phosphorus (P) is an impurity. P segregates at grain boundaries and reduces grain boundary strength. If the P content exceeds 0.030%, even if the contents of other elements are within the ranges of this embodiment, P will segregate excessively at the grain boundaries and the grain boundary strength will decrease. As a result, the bending fatigue strength and surface fatigue strength of mechanical structural parts decrease.
Therefore, the P content is 0.030% or less.
It is preferable that the P content is as low as possible. However, excessive reduction in P content increases manufacturing costs. Therefore, when considering normal industrial production, the preferable lower limit of the P content is more than 0%, more preferably 0.001%, even more preferably 0.005%, and even more preferably 0.010%. %.
A preferable upper limit of the P content is 0.025%, more preferably 0.020%, and even more preferably 0.015%.

The remainder of the chemical composition of the steel material according to this embodiment consists of Fe and impurities. Here, impurities are those that are mixed in from ores used as raw materials, scraps, or the manufacturing environment during industrial manufacturing of steel materials, and to the extent that they do not adversely affect the steel materials of this embodiment. means permissible. The impurities mentioned here include B, Pb, W, Sb, Bi, Co, Ta, Sn, In, Zr, Te, Se, and Zn. The total content of impurities other than O and P is 0.01% or less. Note that among the above impurities, the B content is 0.0003% or less.

[About optional elements]
The chemical composition of the steel material of this embodiment further includes, in place of a part of Fe,
Mo: 0.30% or less,
Nb: 0.050% or less,
Ti: 0.020% or less,
Cu: 0.50% or less,
Ni: 0.80% or less,
V: 0.30% or less,
Mg: 0.0035% or less,
Ca: 0.0030% or less, and
Rare earth elements: One or more elements selected from the group consisting of 0.0050% or less may be contained. These elements are optional elements, and all of them increase the bending fatigue strength and surface fatigue strength of mechanical structural parts.

Mo: 0.30% or less Molybdenum (Mo) is an optional element and may not be contained. That is, the Mo content may be 0%.
When contained, Mo increases the hardenability of the steel material and increases the bending fatigue strength and surface fatigue strength of mechanical structural parts. If even a small amount of Mo is contained, the above effects can be obtained to some extent.
However, if the Mo content exceeds 0.30%, the steel material becomes too hard even if the content of other elements is within the range of this embodiment. In this case, the machinability of the steel material decreases.
Therefore, the Mo content is 0 to 0.30%, and when contained, it is 0.30% or less (that is, more than 0 to 0.30%).
The lower limit of the Mo content is preferably 0.01%, more preferably 0.02%, even more preferably 0.05%, and still more preferably 0.10%.
The upper limit of the Mo content is preferably less than 0.30%, more preferably 0.25%, even more preferably 0.20%, and still more preferably 0.15%.

Nb: 0.050% or less Niobium (Nb) is an optional element and may not be contained. That is, the Nb content may be 0%.
When contained, Nb combines with C and/or N to form Nb precipitates (NbC, NbN, Nb(CN), etc.). Like AlN, Nb precipitates suppress coarsening of crystal grains during gas carburizing treatment due to the pinning effect. Therefore, the bending fatigue strength and surface fatigue strength of the mechanical structural parts are increased. If even a small amount of Nb is contained, the above effects can be obtained to some extent.
However, if the Nb content exceeds 0.050%, the Nb precipitates will become coarse even if the contents of other elements are within the range of this embodiment. In this case, coarsening of crystal grains during gas carburizing cannot be sufficiently suppressed. Therefore, the bending fatigue strength and surface fatigue strength of mechanical structural parts decrease.
Therefore, the Nb content is 0 to 0.050%, and when contained, it is 0.050% or less (that is, more than 0 to 0.050%).
The preferable lower limit of the Nb content is 0.001%, more preferably 0.010%, even more preferably 0.015%, still more preferably 0.020%, even more preferably 0.025%. %.
A preferable upper limit of the Nb content is less than 0.050%, more preferably 0.045%, still more preferably 0.040%, and still more preferably 0.035%.

Ti: 0.020% or less Titanium (Ti) is an optional element and may not be contained. That is, the Ti content may be 0%.
When contained, Ti forms Ti precipitates (TiC, TiN, Ti(CN), etc.) similarly to Nb. Due to the pinning effect, Ti precipitates suppress coarsening of crystal grains during gas carburizing treatment. Therefore, the bending fatigue strength and surface fatigue strength of the mechanical structural parts are increased. If even a small amount of Ti is contained, the above effects can be obtained to some extent.
However, if the Ti content exceeds 0.020%, the Ti precipitates will become coarse even if the contents of other elements are within the range of this embodiment. In this case, coarsening of crystal grains during gas carburizing cannot be sufficiently suppressed. Therefore, the bending fatigue strength and surface fatigue strength of mechanical structural parts decrease.
Therefore, the Ti content is 0 to 0.020%, and when contained, it is 0.020% or less (that is, more than 0 to 0.020%).
The lower limit of the Ti content is preferably 0.001%, more preferably 0.005%, and still more preferably 0.010%.
A preferable upper limit of the Ti content is 0.019%, more preferably 0.017%, and still more preferably 0.015%.

Cu: 0.50% or less Copper (Cu) is an optional element and does not need to be contained. That is, the Cu content may be 0%.
When contained, Cu improves the hardenability of the steel material and increases the bending fatigue strength and surface fatigue strength of mechanical structural parts. If even a small amount of Cu is contained, the above effects can be obtained to some extent.
However, if the Cu content exceeds 0.50%, the steel material becomes too hard even if the contents of other elements are within the range of this embodiment. In this case, the machinability of the steel material decreases.
Therefore, the Cu content is 0 to 0.50%, and if contained, it is 0.50% or less (that is, more than 0 to 0.50%).
The preferable lower limit of the Cu content is 0.01%, more preferably 0.05%, and still more preferably 0.10%. A preferable upper limit of the Cu content is 0.45%, more preferably 0.40%, still more preferably 0.30%, and still more preferably 0.25%.

Ni: 0.80% or less Nickel (Ni) is an optional element and does not need to be contained. That is, the Ni content may be 0%.
When contained, Ni increases the hardenability of the steel material and increases the bending fatigue strength and surface fatigue strength of mechanical structural parts. If even a small amount of Ni is contained, the above effects can be obtained to some extent.
However, if the Ni content exceeds 0.80%, the steel material becomes too hard even if the contents of other elements are within the range of this embodiment. In this case, the machinability of the steel material decreases.
Therefore, the Ni content is 0 to 0.80%, and if contained, it is 0.80% or less (that is, more than 0 to 0.80%).
The preferable lower limit of the Ni content is 0.01%, more preferably 0.05%, and still more preferably 0.10%.
A preferable upper limit of the Ni content is 0.70%, more preferably 0.60%, still more preferably 0.40%, and still more preferably 0.20%.

V: 0.30% or less Vanadium (V) is an optional element and does not need to be contained. That is, the V content may be 0%.
When contained, V forms V precipitates (VC, VN, V(CN), etc.) similarly to Nb. The V precipitates suppress coarsening of crystal grains during gas carburizing treatment due to the pinning effect. Therefore, the bending fatigue strength and surface fatigue strength of the mechanical structural parts are increased. If even a small amount of V is contained, the above effects can be obtained to some extent.
However, if the V content exceeds 0.30%, the steel material becomes too hard even if the contents of other elements are within the range of this embodiment. In this case, the machinability of the steel material decreases.
Therefore, the V content is 0 to 0.30%, and when contained, it is 0.30% or less (that is, more than 0 to 0.30%).
The lower limit of the V content is preferably 0.01%, more preferably 0.03%, and even more preferably 0.04%.
A preferable upper limit of the V content is 0.20%, more preferably 0.15%, and still more preferably 0.10%.

Mg: 0.0035% or less Magnesium (Mg) is an optional element and does not need to be contained. That is, the Mg content may be 0%.
When contained, Mg deoxidizes steel in the same way as Al. In this case, generation of coarse oxides is suppressed. Therefore, the bending fatigue strength and surface fatigue strength of the mechanical structural parts are increased. If even a small amount of Mg is contained, the above effects can be obtained to some extent.
However, if the Mg content exceeds 0.0035%, the formation of coarse Mg oxides in the steel material will be promoted even if the contents of other elements are within the range of this embodiment. In this case, the limit machining rate during hot working decreases.
Therefore, the Mg content is 0 to 0.0035%, and if contained, it is 0.0035% or less (that is, more than 0 to 0.0035%).
The preferable lower limit of the Mg content is 0.0001%, more preferably 0.0003%, and still more preferably 0.0005%.
A preferable upper limit of the Mg content is 0.0030%, more preferably 0.0028%, still more preferably 0.0025%, and still more preferably 0.0020%.

Ca: 0.0030% or less Calcium (Ca) is an optional element and does not need to be contained. That is, the Ca content may be 0%.
When contained, Ca refines the sulfides in the steel material. Ca further promotes spheroidization of sulfides in the steel material. Therefore, the bending fatigue strength and surface fatigue strength of the mechanical structural parts are increased. If even a small amount of Ca is contained, the above effects can be obtained to some extent.
However, if the Ca content exceeds 0.0030%, coarse Ca oxides will be generated in the steel material even if the contents of other elements are within the range of this embodiment. In this case, the bending fatigue strength and surface fatigue strength of the mechanical structural parts decrease.
Therefore, the Ca content is 0 to 0.0030%, and when contained, it is 0.0030% or less (that is, more than 0 to 0.0030%).
The lower limit of the Ca content is preferably 0.0001%, more preferably 0.0002%, even more preferably 0.0005%, even more preferably 0.0007%, and even more preferably 0.0010%. %.
A preferable upper limit of the Ca content is 0.0025%, more preferably 0.0022%, and still more preferably 0.0020%.

Rare earth element (REM): 0.0050% or less Rare earth element (REM) is an optional element and does not need to be contained. That is, the REM content may be 0%. When contained, REM forms a solid solution in the sulfide in the steel material and suppresses the stretching of MnS. As a result, the bending fatigue strength and surface fatigue strength of mechanical structural parts are increased. If even a small amount of REM is contained, the above effects can be obtained to some extent.
However, if the REM content exceeds 0.0050%, coarse oxides will be produced even if the contents of other elements are within the range of this embodiment. In this case, the bending fatigue strength and surface fatigue strength of the mechanical structural parts decrease.
Therefore, the REM content is 0 to 0.0050%, and if contained, it is 0.0050% or less (that is, more than 0 to 0.0050%).
The preferable lower limit of the REM content is 0.0001%, more preferably 0.0010%, and still more preferably 0.0020%.
A preferable upper limit of the REM content is 0.0045%, more preferably 0.0040%, still more preferably 0.0035%, and still more preferably 0.0030%.

In this specification, REM refers to scandium (Sc) with an atomic number of 21, yttrium (Y) with an atomic number of 39, and lanthanoids such as lanthanum (La) with an atomic number of 57 to lutetium (with an atomic number of 71). One or more elements selected from the group consisting of Lu). The REM content in this specification is the total content of these elements.

[About the microstructure of steel]
The microstructure of the steel material of this embodiment contains ferrite, the remainder being pearlite and/or bainite, and the area fraction of ferrite is 50 to 70%.

If the area fraction of ferrite is less than 50%, the area fraction of pearlite and/or bainite in the steel material is too high. In this case, the hardness of the steel increases excessively. As a result, the machinability of the steel material decreases.
On the other hand, if the area fraction of ferrite exceeds 70%, the crystal grain size tends to vary during gas carburizing treatment. Therefore, excessive heat treatment deformation occurs during gas carburizing treatment.

When the area fraction of ferrite is 50 to 70% and the remainder other than ferrite in the microstructure is pearlite and/or bainite, the machinability of the steel material is sufficiently increased. Furthermore, heat treatment deformation during gas carburizing treatment can be suppressed.

In the steel material of this embodiment, the microstructure at each cross-sectional observation position and each vertical cross-section observation position contains 50 to 70% ferrite in terms of area fraction, and the remainder consists of pearlite and/or bainite.

A preferable lower limit of the area fraction of ferrite at each observation position (each cross section observation position, each longitudinal section observation position) is 52%, more preferably 55%, and even more preferably 57%.
A preferable upper limit of the area fraction of ferrite at each observation position (each cross section observation position, each longitudinal section observation position) is 68%, more preferably 65%, and even more preferably 63%.

[About variations in microstructure in the cross section of steel materials]
Furthermore, in the steel material of this embodiment, variations in the microstructure are sufficiently suppressed in a cross section that is a cross section perpendicular to the longitudinal direction of the steel material. This point will be explained below.

FIG. 2 is a schematic cross-sectional view of the steel material of this embodiment, which is a cross section perpendicular to the longitudinal direction. Referring to FIG. 2, the cross section CS of the steel material has a circular shape with a radius R. In this cross-section CS, the center position C1 of the cross-section CS, and 8 8s arranged at a position R/2 in the radial direction from the center position C1 of the cross-section CS at a pitch of 45° around the center of the cross-section CS. The R/2 positions C2 to C9 are defined as nine "cross section observation positions" C1 to C9.

The microstructure at the cross-sectional observation positions C1 to C9 satisfies the following (A) and (B).
(A) The arithmetic mean value of the area fraction of ferrite at the cross-sectional observation positions C1 to C9 is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less.
(B) Among the average grain sizes of ferrite at cross-sectional observation positions C1 to C9, the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less.
Hereinafter, (A) and (B) will be explained in detail.

[About (A)]
As described in (A) above, in the steel material of this embodiment, the arithmetic mean value of the area fraction of ferrite at the cross-sectional observation positions C1 to C9 is 50 to 70%, and the standard deviation of the area fraction of ferrite is is 4.0% or less.

Since the standard deviation of the ferrite area fraction is 4.0% or less, variations in the phase fraction of the microstructure at each cross-sectional observation position C1 to C9 are sufficiently suppressed. Therefore, during the gas carburizing process, it is possible to suppress variations in the timing of occurrence of martensitic transformation at each of the cross-sectional observation positions C1 to C9.

If the standard deviation of the area fraction of ferrite at the cross-sectional observation positions C1 to C9 exceeds 4.0%, the variation in the phase fraction at each cross-sectional observation position C1 to C9 is large. In this case, heat treatment deformation during gas carburizing cannot be sufficiently suppressed.
Therefore, the standard deviation of the area fraction of ferrite at the cross-sectional observation positions C1 to C9 is 4.0% or less.

The upper limit of the standard deviation of the area fraction of ferrite is preferably 3.8%, more preferably 3.5%, and even more preferably 3.0%. The lower limit of the standard deviation of the area fraction of ferrite is not particularly limited.
The lower limit of the standard deviation of the area fraction of ferrite is not particularly limited. The lower limit of the standard deviation of the area fraction of ferrite is preferably 0.1%, more preferably 0.5%, still more preferably 1.0%, and still more preferably 1.5%.

[About (B)]
Among the average grain sizes of ferrite at the cross-sectional observation positions C1 to C9, the ratio of the maximum average grain size to the minimum average grain size is referred to as "ferrite average grain size ratio." The ferrite average grain size ratio in the cross section is defined by the following formula.
Ferrite average grain size ratio = (maximum value of ferrite average grain size in C1 to C9) / (minimum value of ferrite average grain size in C1 to C9)

In the steel material of this embodiment, the ferrite average grain size ratio at the cross-sectional observation positions C1 to C9 is 2.00 or less. In this case, variations in the average grain size of ferrite at each of the cross-sectional observation positions C1 to C9 are sufficiently suppressed. In other words, the ferrite grains at each position are aligned. Therefore, variations in the occurrence of martensitic transformation during carburizing treatment can be sufficiently suppressed. Therefore, heat treatment deformation of the steel material during carburizing treatment can be suppressed.

When the ferrite average grain size ratio exceeds 2.00, the ferrite grains at each cross-sectional observation position C1 to C9 are dispersed. In this case, heat treatment deformation of the steel material during gas carburizing treatment cannot be sufficiently suppressed.
Therefore, the ferrite average grain size ratio is 2.00 or less.

A preferable upper limit of the ferrite average particle size ratio is 1.95, more preferably 1.90, and still more preferably 1.80.
The lower limit of the ferrite average particle size ratio is not particularly limited. A preferable lower limit of the ferrite average particle size ratio is 1.10, more preferably 1.20, still more preferably 1.30, and still more preferably 1.40.

[About the variation in microstructure in the longitudinal section of steel materials]
Furthermore, in the steel material of this embodiment, variations in the microstructure are sufficiently suppressed not only in the above-mentioned cross section but also in the longitudinal section, which is a cross section parallel to the longitudinal direction of the steel material and including the central axis of the steel material. . In the steel material of this embodiment, variation in the microstructure not only in the cross section but also in the longitudinal section is sufficiently suppressed, so that heat treatment deformation that occurs three-dimensionally can be sufficiently suppressed. In the following, suppression of microstructure variations in a longitudinal section will be explained.

FIG. 3 is a schematic diagram of a longitudinal section of the steel material of this embodiment, which is parallel to the longitudinal direction and includes the central axis. Referring to FIG. 3, in the longitudinal section LS of the steel material, there are three central axis positions L1 to L3 arranged at an R/2 pitch on the central axis CL1 of the steel material, and R in the radial direction from each central axis position. The six R/2 positions L4 to L9 arranged at the /2 position are defined as nine "longitudinal section observation positions" L1 to L9.

The microstructures at a total of nine longitudinal section observation positions L1 to L9 described above satisfy the following (C) and (D).
(C) The arithmetic mean value of the area fraction of ferrite at longitudinal section observation positions L1 to L9 is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less.
(D) Among the average grain sizes of ferrite at longitudinal section observation positions L1 to L9, the ratio of the maximum average grain size to the minimum average grain size (ferrite average grain size ratio) is 2.00 or less.
Hereinafter, (C) and (D) will be explained in detail.

[About (C)]
As described in (C) above, in the steel material of this embodiment, the arithmetic mean value of the area fraction of ferrite at the longitudinal section observation positions L1 to L9 is 50 to 70%, and the standard deviation of the area fraction of ferrite is is 4.0% or less.

Since the standard deviation of the area fraction of ferrite is 4.0% or less, variations in the phase fraction of the microstructure at each longitudinal section observation position L1 to L9 are sufficiently suppressed. Therefore, during the gas carburizing process, it is possible to suppress variations in the timing at which martensitic transformation occurs at each of the longitudinal section observation positions L1 to L9.

If the standard deviation of the area fraction of ferrite at the longitudinal section observation positions L1 to L9 exceeds 4.0%, the variation in the phase fraction at each longitudinal section observation position L1 to L9 is large. In this case, heat treatment deformation during gas carburizing cannot be sufficiently suppressed.
Therefore, the standard deviation of the area fraction of ferrite at the longitudinal section observation positions L1 to L9 is 4.0% or less.

The upper limit of the standard deviation of the area fraction of ferrite is preferably 3.8%, more preferably 3.5%, and still more preferably 3.0%.
The lower limit of the standard deviation of the area fraction of ferrite is not particularly limited. The lower limit of the standard deviation of the area fraction of ferrite is preferably 0.1%, more preferably 0.5%, still more preferably 1.0%, and still more preferably 1.5%.

[About (D)]
Among the average grain sizes of ferrite at longitudinal section observation positions L1 to L9, the ratio of the maximum average grain size to the minimum average grain size is referred to as "ferrite average grain size ratio". The ferrite average grain size ratio in the longitudinal section is defined by the following formula.
Ferrite average grain size ratio = (maximum value of ferrite average grain size in L1 to L9) / (minimum value of ferrite average grain size in L1 to L9)

In the steel material of this embodiment, the ferrite average grain size ratio at longitudinal section observation positions L1 to L9 is 2.00 or less. In this case, variations in the average grain size of ferrite at each longitudinal section observation position L1 to L9 are sufficiently suppressed. In other words, the ferrite grains at each position are aligned. Therefore, variations in the occurrence of martensitic transformation during carburizing treatment can be sufficiently suppressed. Therefore, heat treatment deformation of the steel material during carburizing treatment can be suppressed.

When the ferrite average grain size ratio exceeds 2.00, the ferrite grains at each longitudinal section observation position L1 to L9 are dispersed. In this case, heat treatment deformation of the steel material during gas carburizing treatment cannot be sufficiently suppressed. Therefore, the ferrite average grain size ratio at nine longitudinal cross-sectional observation positions L1 to L9 is 2.00 or less.

A preferable upper limit of the ferrite average particle size ratio is 1.95, more preferably 1.90, and still more preferably 1.80.
The lower limit of the ferrite average particle size ratio is not particularly limited. A preferable lower limit of the ferrite average particle size ratio is 1.10, more preferably 1.20, still more preferably 1.30, and still more preferably 1.40.

[Method for observing microstructure at each observation position, method for measuring ferrite area fraction and ferrite average particle size ratio]
The method of observing the microstructure and the method of measuring the area fraction of ferrite and the average ferrite grain size ratio at the cross-sectional observation positions C1 to C9 and the vertical cross-section observation positions L1 to L9 of the steel material of this embodiment are as follows. be.

[Method for observing microstructure of cross section CS]
The method for observing the microstructure of the cross section CS is as follows. A sample including each cross-sectional observation position C1 to C9 is collected from the steel material. Among the surfaces of the sample, the surface corresponding to the cross section CS is defined as the observation surface. In the observation plane, the observation field including the cross-sectional observation position is 0.5 mm x 1.0 mm.

After polishing the observation surface of the sample, the observation surface is etched using 3% nitric acid alcohol (nital etching liquid). The observation field (0.5 mm x 1.0 mm) of the etched observation surface is observed using a 100x optical microscope.

In the observation field, each phase such as ferrite, pearlite, and bainite has a different contrast. Specifically, in the observation field, ferrite is observed to be white, and bainite and pearlite are observed to be darker than ferrite. Therefore, ferrite is easily distinguishable from other phases (pearlite and bainite). Identify ferrite based on contrast.

[About (A)]
The area (μm ² ) of ferrite in each observation field (each cross-sectional observation position) is determined. The area fraction (%) of ferrite in each observation field (each cross-sectional observation position) is determined using the area of ferrite and the area of the observation field.

[How to find the arithmetic mean value of ferrite area fraction]
The arithmetic mean value of the ferrite area fraction (%) in the nine observation fields (cross-sectional observation positions) is the arithmetic mean value (%) of the ferrite area fraction at the nine cross-sectional observation positions C1 to C9. Define.

[How to find the standard deviation of the area fraction of ferrite]
The standard deviation (%) of the ferrite area fraction at nine cross-sectional observation positions C1 to C9 is calculated from the ferrite area fraction (%) at nine observation fields (cross-sectional observation positions). The standard deviation here is the sample standard deviation.

[About (B)]
The area (μm ² ) of each ferrite grain observed in each of the above-mentioned observation fields (each cross-sectional observation position C1 to C9) is measured. Find the arithmetic mean value of the area of each ferrite grain. The circle-equivalent diameter of the arithmetic mean value of the obtained area is defined as the average grain size (μm) of ferrite at each cross-sectional observation position C1 to C9. Here, the equivalent circle diameter means the diameter (μm) of a circle having the same area as the arithmetic mean value of the areas of ferrite grains.

The average grain size of ferrite at nine cross-sectional observation positions C1 to C9 is determined. Then, among the average grain sizes of these ferrites, the maximum average grain size (μm) and the minimum average grain size (μm) of ferrite are specified. The ratio of the maximum average grain size to the specified minimum average grain size (ferrite average grain size ratio) is determined.

[Method for observing microstructure of longitudinal section LS]
The method for observing the microstructure of the longitudinal section LS is as follows. A sample including each longitudinal section observation position L1 to L9 is collected from the steel material. Among the surfaces of the sample, the surface corresponding to the longitudinal section LS is defined as the observation surface. On the observation plane, the observation field including the longitudinal section observation position is 0.5 mm x 1.0 mm. More specifically, the length of the observation field of 0.5 mm is defined as the radial direction of the steel material, and the length of 1.0 mm is defined as the longitudinal direction of the steel material.

After polishing the observation surface of the sample, the observation surface is etched using 3% nitric acid alcohol (nital etching liquid). The observation field (0.5 mm x 1.0 mm) of the etched observation surface is observed using a 100x optical microscope. Each phase in the observation field is identified using the same method as the microstructure observation of the cross section CS.

[About (C)]
Among the phases identified by the above method, the area (μm ² ) of ferrite in each observation field (each longitudinal section observation position) is determined. The area fraction (%) of ferrite in each observation field (each vertical section observation position) is determined using the area of ferrite and the area of the observation field.

[How to find the arithmetic mean value of the area fraction of ferrite]
The arithmetic mean value of the ferrite area fraction (%) in the nine observation fields (longitudinal section observation positions) is the arithmetic mean value (%) of the ferrite area fraction at the nine longitudinal section observation positions L1 to L9. Define.

[How to find the standard deviation of the area fraction of ferrite]
The standard deviation (%) of the ferrite area fraction at the nine longitudinal section observation positions L1 to L9 is calculated from the ferrite area fraction (%) at the nine observation fields (vertical section observation positions).

[About (D)]
The area (μm ² ) of each ferrite grain observed in each of the above-mentioned observation fields (each longitudinal section observation position L1 to L9) is measured. Find the arithmetic mean value of the area of each ferrite grain. The circle-equivalent diameter of the arithmetic mean value of the obtained area is defined as the average grain size (μm) of ferrite at each longitudinal section observation position L1 to L9.

The average grain size of ferrite at nine longitudinal section observation positions L1 to L9 is determined. Then, among the average grain sizes of these ferrites, the maximum average grain size (μm) and the minimum average grain size (μm) of ferrite are specified. The ratio of the maximum average grain size to the specified minimum average grain size (ferrite average grain size ratio) is determined.

[About formula (1)]
As described above, the steel material of this embodiment has a microstructure as uniform as possible not only in the cross section CS but also in the longitudinal section LS. In the steel material of this embodiment, furthermore, by satisfying formula (1) on the premise that a minute period in which martensite-transformed portions and martensite-untransformed portions coexist during quenching, martensite-untransformed portions are suppresses the occurrence of heat treatment distortion. As a result, heat treatment deformation can be sufficiently suppressed while maintaining sufficient machinability, sufficient bending fatigue strength and sufficient surface fatigue strength in mechanical structural parts. Formula (1) will be explained below.

The chemical composition of the steel material of this embodiment further satisfies the following formula (1) on the premise that the content of each element in the chemical composition is within the above-mentioned range.
1-(0.5C+0.03Si+0.06Mn+0.01Cr+0.05Mo)<0.800 (1)
Here, the content (mass %) of the corresponding element is substituted for each element symbol in formula (1). If the corresponding element is not contained, "0" is assigned to the element symbol.

In the steel material of this embodiment, not only the cross section CS but also the microstructure of the longitudinal section LS is made uniform. However, the microstructures at the cross-sectional observation positions C1 to C9 on the cross-section CS satisfy (A) and (B), and the microstructures at the longitudinal cross-section observation positions L1 to L9 on the longitudinal cross-section LS satisfy (C) and (B). Even if the microstructure is made uniform by satisfying (D), as described above, during quenching in gas carburizing treatment, a minute period in which martensite-transformed portions and martensite-untransformed portions coexist will always occur. If the amount of heat treatment distortion in the untransformed martensite portion is large during this minute time period, heat treatment deformation will occur. Therefore, the steel material of this embodiment further satisfies formula (1).

Define F1=1-(0.5C+0.03Si+0.06Mn+0.01Cr+0.05Mo). F1 is an index related to the amount of heat treatment deformation of steel material in gas carburizing treatment. Among the elements in the chemical composition mentioned above, C, Si, Mn, Cr, and Mo contained in F1 are particularly important in the formation of martensite during the microscopic time period in which the martensite-transformed portion and the martensite-untransformed portion coexist during quenching. Increases the strength of untransformed parts.

Referring to FIG. 1, as F1 decreases, the maximum deformation amount ratio decreases, and the heat treatment deformation amount decreases. When F1 becomes less than 0.800, the maximum deformation amount ratio decreases significantly. In other words, the maximum deformation amount ratio to F1 has an inflection point near F1=0.800.

Therefore, on the premise that the content of each element is within the range of this embodiment, if F1 satisfies formula (1), that is, if F1 is less than 0.800, the steel material during gas carburizing treatment The heat treatment deformation of can be sufficiently suppressed.

A preferable upper limit of F1 is 0.799, more preferably 0.797, and still more preferably 0.795. The lower limit of F1 is not particularly limited. However, considering the upper limit of the content of each element in the chemical composition of this embodiment, the lower limit of F1 is preferably 0.765, more preferably 0.770, and still more preferably 0.775. The numerical value of F1 is the value obtained by rounding off to the fourth decimal place.

In the steel material of this embodiment having the above configuration, the content of each element in the chemical composition is within the range of this embodiment, F1 satisfies formula (1), and cross-sectional observation positions C1 to C9 and longitudinal section The microstructures at surface observation positions L1 to L9 are within the scope of this embodiment. Therefore, the machinability of the steel material of this embodiment after hot working is excellent. Furthermore, when the steel material of this embodiment is subjected to gas carburizing treatment, the mechanical structural component has excellent bending fatigue strength and surface fatigue strength, and heat treatment deformation can be sufficiently suppressed.

[About the microstructure of steel]
The steel material of this embodiment is a so-called as-rolled material (azurol material). Therefore, in the steel material of this embodiment, a so-called band structure is observed in the observation field of the longitudinal section observation positions L1 to L9. Here, the band structure is a well-known microstructure, and as shown in FIG. 4, it consists of ferrite (ferrite band) F extending in the longitudinal direction of the steel material and non-ferrite (non-ferrite band) NF extending in the longitudinal direction of the steel material. refers to a structure in which layers are alternately stacked in the radial direction. Non-ferrites are pearlite and/or bainite.

[Applications of steel materials]
As mentioned above, the steel material of this embodiment is suitable as a material for mechanical structural parts. The steel material of this embodiment is particularly suitable for applications such as gears or shafts for automobiles, construction machines, industrial machines, and the like.

[Manufacturing method of steel materials]
An example of the method for manufacturing steel materials of this embodiment will be described. The method for manufacturing steel materials described below is an example for manufacturing the steel materials of this embodiment. Therefore, the steel material having the above-mentioned configuration may be manufactured by a manufacturing method other than the manufacturing method described below. However, the manufacturing method described below is a preferable example of the method for manufacturing the steel material of this embodiment.

An example of the method for manufacturing steel materials of this embodiment includes the following steps.
(Process 1) Process of preparing materials (material preparation process)
(Process 2) Process of manufacturing steel products by hot processing materials (hot processing process)
Each step will be explained below.

[(Process 1) Material preparation process]
In the material preparation step, a material for the steel material of this embodiment is prepared. Specifically, molten steel is produced in which the content of each element in the chemical composition is within the range of this embodiment and F1 satisfies formula (1). The refining method is not particularly limited, and any known method may be used. For example, molten metal produced by a well-known method is subjected to refining (primary refining) in a converter. Well-known secondary refining is performed on the molten steel tapped from the converter. In secondary refining, the content of alloying elements in molten steel is adjusted to produce molten steel having a chemical composition in which the content of each element is within the range of this embodiment and F1 satisfies formula (1). .

Using the molten steel produced by the above-mentioned refining method, a material is produced by a well-known casting method. For example, an ingot may be manufactured by an ingot-forming method using molten steel. Alternatively, a bloom or a billet may be manufactured by a continuous casting method using molten steel. A material (ingot, bloom, or billet) is manufactured by the above method. When using a continuous casting method, reduction may be applied to the slab during solidification.

[(Step 2) Hot processing step]
In the hot working step, hot working is performed on the material (ingot, bloom, or billet) prepared in the material preparation step to manufacture the steel material of this embodiment. Although the shape of the steel material is not particularly limited, it is, for example, a steel bar or a wire rod. In the following description, a case where the steel material is a steel bar will be described as an example. However, even if the steel material has a shape other than a steel bar, it can be manufactured using the same hot working process.

The hot working process includes the following steps.
(Step 21) Blooming rolling step Heating temperature: 1250 to 1300°C
Holding time: 10 hours or more (Step 22) Finish rolling process Heating temperature: 1150-1200℃
Holding time: 1.5-3.0 hours Finishing temperature: 950-1000℃
(Step 23) Temperature holding step Average cooling rate at 900-800°C: 0.05°C/second or less (Step 24) Cooling step Average cooling rate at 800-300°C: 0.10-1.00°C/second Each step will be explained below.

[(Step 21) Blooming rolling step]
In the blooming process, a billet is manufactured by hot rolling a material. Specifically, in the blooming process, a billet is manufactured by hot rolling (blending) the material using a blooming mill. When a continuous rolling mill is installed downstream of the blooming mill, the billet after blooming is further hot-rolled using the continuous mill to produce a billet with a smaller size. It's okay. In a continuous rolling mill, horizontal stands having a pair of horizontal rolls and vertical stands having a pair of vertical rolls are alternately arranged in a line. As described above, in the blooming rolling process, a material is manufactured into a billet using a blooming mill or a blooming mill and a continuous rolling mill.

The conditions in the blooming rolling process are as follows.
Heating temperature: 1250-1300℃
Holding time: 10 hours or more The heating temperature in the heating furnace in the blooming process is 1250 to 1300°C. The holding time at the heating temperature (1250 to 1300°C) is 10 hours or more. If the heating temperature in the heating furnace during the blooming rolling process is 1250 to 1300°C, and the holding time at the heating temperature (1250 to 1300°C) is 10 hours or more, other manufacturing conditions are satisfied. The premise is that solidification segregation in the material that occurs during the material preparation process can be sufficiently alleviated. Therefore, the standard deviation of the area fraction of ferrite at each of the cross section observation positions C1 to C9 and each of the longitudinal section observation positions L1 to L9 is 4.0% or less. The upper limit of the holding time at the heating temperature is not particularly limited. However, in consideration of manufacturing costs, the preferable upper limit of the holding time at the heating temperature is 30 hours.

Note that the billet manufactured by the blooming process is allowed to cool (air-cool) to room temperature before the finish rolling process.

Note that the area reduction rate in the blooming process is 30% or more. Here, the area reduction rate (%) is defined by the following formula.
Area reduction rate (%) = (1 - Area of the cross section (cross section perpendicular to the longitudinal direction) of the steel material after blooming/Area of the cross section (cross section perpendicular to the longitudinal direction) of the material before blooming) ×100

If the area reduction rate in the blooming process is 30% or more, the area of ferrite at each cross-sectional observation position C1 to C9 and each longitudinal cross-section observation position L1 to L9 is calculated based on the premise that other manufacturing conditions are met. The standard deviation of the fraction is 4.0% or less.

[(Step 22) Finish rolling step]
In the finish rolling process, first, the billet, which has been cooled to room temperature, is heated using a heating furnace. The heated billet is hot rolled using a continuous rolling mill to produce a steel bar, which is a steel material.

The conditions in the finish rolling process are as follows.
Heating temperature: 1150-1200℃
Holding time: 1.5-3.0 hours Finishing temperature: 950-1000℃

[Heating temperature and holding time]
The heating temperature in the heating furnace in the finish rolling process is 1150 to 1200°C. The holding time at the heating temperature (1150 to 1200°C) is 1.5 to 3.0 hours. If the heating temperature of the heating furnace in the finish rolling process is 1150 to 1200°C and the holding time at the heating temperature (1150 to 1200°C) is 1.5 to 3.0 hours, other manufacturing conditions are satisfied. Assuming that, temperature variations within the steel material (steel bar) can be sufficiently suppressed. Therefore, the ferrite average grain size ratio at the cross section observation positions C1 to C9 and the longitudinal section observation positions L1 to L9 is 2.00 or less.

[Finishing temperature]
In the finish rolling process, hot rolling (finish rolling) is performed using a continuous rolling mill equipped with a plurality of rolling stands arranged in a row. In hot rolling using a continuous rolling mill, the temperature of the steel material at the exit side of the stand where the steel material is finally rolled is defined as the finishing temperature (°C). Note that the steel material temperature means the surface temperature of the steel material.

The finishing temperature is 950-1000°C. If the finishing temperature is 950 to 1000°C, variations in austenite grain size in the steel material (steel bar) can be sufficiently suppressed, provided that other manufacturing conditions are satisfied. Therefore, when austenite is transformed into ferrite in the temperature holding step and cooling step described later, variations in the average grain size of ferrite are sufficiently suppressed. Therefore, the ferrite average grain size ratio at the cross section observation positions C1 to C9 and the longitudinal section observation positions L1 to L9 is 2.00 or less.

[(Step 23) Temperature holding step]
In the temperature holding step, the temperature of the steel material is maintained after the finish rolling step and before the cooling step. The conditions in the temperature holding step are as follows.
Average cooling rate when the steel material temperature is 900 to 800°C: 0.05°C/second or less After the finish rolling process, the average cooling rate when the steel material temperature is 900 to 800°C is suppressed to 0.05°C/second or less. For example, for a steel material whose temperature is 900 to 800°C after the finish rolling process, an annealing cover, a heat insulation cover, or a temperature holding furnace is used to reduce the average cooling rate to 0.05°C/sec. Keep it below.

If the average cooling rate at a steel material temperature of 900 to 800° C. is 0.05° C./sec or less, temperature variations in the axial direction (longitudinal direction) of the steel material can be suppressed on the premise that other manufacturing conditions are satisfied. Therefore, variations in the timing of ferrite transformation in the axial direction of the steel material can be suppressed. Therefore, variation in the growth of ferrite grains in the axial direction (longitudinal section) of the steel material can be particularly suppressed. Specifically, the following mechanism works.

In the steel material after the finish rolling process, austenite gradually transforms into ferrite as the steel material temperature decreases. If the temperature of the steel material is in the range of 900 to 800°C, and there is temperature variation in the axial direction of the steel material, ferrite formed at a relatively early stage and ferrite formed at a relatively late stage will coexist after the finish rolling process. Put it away. In this case, ferrite grains generated at an early stage tend to be coarser than ferrite grains transformed at a later stage. As a result, the variation in ferrite grains becomes large, especially in the axial direction (longitudinal section) of the steel material.

If the average cooling rate at a steel material temperature of 900 to 800° C. is fast, the temperature variation in the axial direction (longitudinal section) of the steel material becomes large. Therefore, the ferrite average grain size ratio at the longitudinal section observation positions L1 to L9 becomes large.

Therefore, in this embodiment, the average cooling rate when the steel material temperature is 900 to 800°C is suppressed to 0.05°C/sec or less. In this case, temperature variations in the axial direction (longitudinal section) of the steel material can be suppressed. Therefore, a shift in the timing of ferrite generation (transformation) in the longitudinal section of the steel material is suppressed. As a result, the ferrite average grain size ratio at longitudinal section observation positions L1 to L9 can be made 2.00 or less, provided that other manufacturing conditions are met.

[(Step 24) Cooling step]
In the cooling process, the temperature of the steel material after the temperature holding process is cooled. The conditions in the cooling process are as follows.
Average cooling rate for steel materials with a temperature of 800 to 300°C: 0.10 to 1.00°C/sec Average cooling rate of 0.10 to 1.00°C/sec for steel materials with a temperature of 800 to 300°C Cool it down. If the average cooling rate at a steel material temperature of 800 to 300°C is 0.10 to 1.00°C/sec, assuming that other manufacturing conditions are met, the cross-sectional observation positions C1 to C9 and the longitudinal cross-sectional observation positions The arithmetic mean value of the area fraction of ferrite in L1 to L9 is 50 to 70%.

Through the above manufacturing process, the steel material of this embodiment having the above-described configuration can be manufactured. Note that, as described above, the steel material of this embodiment is an as-rolled material.

The steel material of this embodiment is suitable as a material for mechanical structural parts manufactured by performing gas carburizing treatment. However, the steel material of this embodiment may be manufactured into mechanical structural parts by performing surface hardening heat treatment other than gas carburizing treatment. Examples of other surface hardening heat treatments include hardening and tempering, induction hardening and tempering, and nitriding treatment (nitriding hardening and tempering).

[About machine structural parts]
Machine structural parts are used, for example, in automobiles and construction vehicles. Examples of mechanical structural parts include gears and shafts used in steering mechanisms.

The mechanical structural component made of steel according to this embodiment is manufactured by a well-known manufacturing method. For example, mechanical structural parts are manufactured by the following method.

An example of a method for manufacturing mechanical structural parts includes the following steps.
- Hot processing process - Cutting process - Heat treatment process Each process will be explained below.

[Hot processing process]
In the hot working step, hot working is performed on the steel material of this embodiment. The hot working is, for example, the well-known hot forging. The heating temperature in the hot working step is, for example, 1000 to 1300°C. After hot working, the steel material is left to cool (air-cooled). The steel material after being allowed to cool may be subjected to an annealing treatment, if necessary.

[Cutting process]
A cutting process is performed on the steel material after the hot working process to produce an intermediate product having a predetermined shape. During this cutting process, high machinability of the steel material is required. In the cutting process, a well-known cutting process is performed. Cutting allows the manufacture of mechanical structural parts with precise shapes that would be difficult to produce using hot working processes alone.

[Heat treatment process]
Heat treatment is performed on the intermediate product after cutting. Here, "heat treatment" includes a well-known gas carburizing process and a well-known tempering process. Note that, as described above, gas carburizing treatment also includes gas carbonitriding treatment.

The gas carburizing process includes a gas carburizing process and a quenching process. It is a technical matter well known to those skilled in the art that in gas carburizing treatment, the surface hardness, core hardness, and surface carbon concentration of mechanical structural parts can be appropriately adjusted by appropriately adjusting well-known conditions.
Hereinafter, a well-known gas carburizing process will be explained as an example of the heat treatment process. It is well known to those skilled in the art that the well-known gas carbonitriding process is also carried out in the same steps as the gas carburizing process.

[Gas carburizing treatment]
The gas carburizing process includes a gas carburizing process and a quenching process. The gas carburizing process and the quenching process will be explained below.

[Gas carburizing process]
FIG. 5 is a diagram showing an example of a heat pattern in the gas carburizing step S10 and the quenching step S20. The vertical axis in FIG. 5 is the treatment temperature (° C.) during gas carburizing treatment, and the horizontal axis is time (minutes). Referring to FIG. 5, gas carburizing step S10 includes a heating step S0, a carburizing step S1, and a diffusion step S2.

In the heating step S0, the intermediate product charged into the furnace is heated to a carburizing temperature Tc. The carburizing temperature Tc in the heating step S0 is, for example, 830 to 1100°C.

In the carburizing step S1, the intermediate product is held in an atmosphere with a predetermined carbon potential Cp1 and a carburizing temperature Tc for a predetermined time (holding time t1). The carbon potential Cp1 in the carburizing step S1 is, for example, 0.5 to 1.2%, and the holding time t1 at the carburizing temperature Tc is, for example, 60 minutes or more.

In the diffusion step S2, the carburizing temperature Tc is maintained for a predetermined time (holding time t2) in an atmosphere with a predetermined carbon potential Cp2. Here, the carbon potential Cp2 in the diffusion step S2 is, for example, 0.5 to 1.2%, and the holding time t2 at the carburizing temperature Tc is, for example, 30 minutes or more. The carbon potential Cp2 in the diffusion step S2 is preferably lower than the carbon potential Cp1 in the carburizing step S1.

[Quenching process]
A quenching step S20 is performed on the intermediate product after the gas carburizing step S10. In the hardening step S20, the intermediate product after the gas carburizing step S10 is held at a hardening temperature Ts of _Ar3 or higher, and then the intermediate product is rapidly cooled and hardened. The holding time t3 at the quenching temperature Ts is not particularly limited, but is, for example, 30 to 60 minutes. The quenching temperature Ts is preferably lower than the carburizing temperature Tc. The cooling method in the quenching process is oil cooling or water cooling. Specifically, the intermediate product maintained at the quenching temperature is immersed in a cooling bath containing oil or water as a cooling medium to rapidly cool it. The temperature of oil or water as a cooling medium is, for example, room temperature to 200°C. Further, sub-zero processing may be performed as necessary.

[Tempering process]
A well-known tempering process is performed on the intermediate product after the quenching process. The tempering temperature is, for example, 100 to 200°C. The holding time at the tempering temperature is, for example, 90 to 150 minutes.

Through the above steps, mechanical structural parts are manufactured using the steel material of this embodiment as a raw material.

[Other processes]
If necessary, the intermediate product after the tempering process may be further subjected to grinding or shot peening. When grinding is performed, a shape is given to the steel material by cutting. By performing cutting, a more precise shape can be given to the steel material. Furthermore, when shot peening is performed, compressive residual stress is introduced into the surface layer of the intermediate product after gas carburizing. Compressive residual stress suppresses the initiation and propagation of fatigue cracks. Therefore, the bending fatigue strength and surface fatigue strength of the mechanical structural parts are increased. The shot peening treatment may be performed using a well-known method. It is desirable that the shot peening treatment be performed using, for example, shot grains having a diameter of 0.7 mm or less and an arc height of 0.4 mm or more.

Steel materials having the chemical composition shown in Table 1 were prepared. Note that the steel type number A corresponded to SCr420H specified in JIS G 4052 (2016). Further, as a reference steel material, a steel material having a chemical composition corresponding to SCM420H specified in JIS G 4052 (2016) was used.

"-" in Table 1 means that the corresponding element content is 0% in significant figures (values to the smallest digit) specified in the embodiment. In other words, it means that the corresponding element content is 0% when the fraction is rounded off to the specified significant figures (values up to the smallest digit) in the above-described embodiment.
For example, the Mo content specified in this embodiment is specified as a numerical value to the second decimal place. Therefore, steel type number A in Table 1 means that the measured Mo content was 0% when rounded to the second decimal place.
Further, the Nb content specified in this embodiment is specified as a numerical value to the third decimal place. Therefore, steel type number A in Table 1 means that the measured Nb content was 0% when rounded to the fourth decimal place.
Note that rounding means rounding down if the digit (fraction) below the specified minimum digit is less than 5, and rounding up if it is 5 or more.

A steel material was manufactured by the following method. Molten steel was continuously cast to produce slabs (bloom). The bloom material was subjected to a hot working process under the conditions shown in Table 2.

The temperature described in the "Heating temperature (° C.)" column in the "Bulking rolling step" and "Finish rolling step" columns is the heating temperature (° C.). The time stated in the "Holding time (hours)" column in the "Bulking rolling process" and "Finish rolling process" columns is the holding time (hours) at the heating temperature. The temperature in the "Finishing temperature (℃)" column in the "Finish rolling process" column is the temperature of the steel material (surface temperature of the steel material) (℃) at the exit side of the stand where the last rolling was performed in the continuous rolling mill in the finish rolling process. It is. The speed described in the "Cooling rate (°C/sec)" column of the "Temperature holding step" column is the average cooling rate (°C/sec) when the steel material temperature is 900 to 800°C. The speed described in the "Cooling rate (°C/sec)" column of the "Cooling process" column is the average cooling rate (°C/sec) when the steel material temperature is 800 to 300°C.

In the blooming rolling step of the hot working step, the produced bloom was heated at the heating temperature and holding time shown in Table 2. Thereafter, the bloom was bloomed using a blooming mill to produce a billet. The produced billet was water-cooled to room temperature (25°C). The cross section perpendicular to the longitudinal direction of the billet was a rectangle measuring 162 mm x 162 mm. The heating temperature and holding time in the blooming process were as shown in Table 2. Note that the area reduction rate in the blooming process was 30% or more under all manufacturing conditions.

The billet after the blooming process was subjected to a finish rolling process under the conditions shown in Table 2 to produce a steel material (steel bar) with a diameter of 50 mm. Specifically, the billet was heated at the heating temperature (°C) and holding time (hours) shown in the finish rolling process column of Table 2. Finish rolling was performed on the heated billet to produce a steel bar. At this time, the finishing temperature (°C) was as shown in Table 2.

A temperature holding process was performed on the steel material (steel bar) after the finish rolling process. Manufacturing conditions a to i were adjusted so that the average cooling rate was 0.05° C./sec or less by using a slow cooling cover for steel materials with a steel material temperature of 900 to 800° C. On the other hand, in manufacturing condition j, the steel material whose temperature was 900 to 800° C. was allowed to cool without using a slow cooling cover. Therefore, the average cooling rate when the steel material temperature was 900 to 800°C was over 0.05°C/sec.

After the temperature holding step, a cooling step was performed. Specifically, under each manufacturing condition, the average cooling rate (°C/sec) at a steel material temperature of 800 to 300°C was as shown in the cooling process column of Table 2.

Steel materials whose temperature was 300° C. or lower were allowed to cool (air-cooled) to room temperature. Through the above manufacturing process, steel materials (steel bars) with test numbers 1 to 31 shown in Table 3 were manufactured. Note that test number 31 is an example using SCM420H, which is a reference steel, and used manufacturing condition a, which is one of the manufacturing methods generally used for steel materials having the chemical composition of SCM420H.

[Evaluation test]
The following items were determined for the steel materials (steel bars) of each test number manufactured through the above manufacturing process.
(A1) Observation of the microstructure of the cross section (A11) Arithmetic mean value of the area fraction of ferrite in the cross section (A12) Standard deviation of the area fraction of ferrite in the cross section (A13) Average grain size ratio of ferrite in the cross section ( B1) Observation of the microstructure in the longitudinal section (B11) Arithmetic mean value of the area fraction of ferrite in the longitudinal section (B12) Standard deviation of the area fraction of ferrite in the longitudinal section (B13) Average grain size ratio of ferrite in the longitudinal section The following evaluation tests were conducted on the steel materials with each test number.
(C1) Machinability evaluation test (C2) Bending fatigue strength evaluation test (C3) Surface fatigue strength evaluation test (C4) Heat treatment deformation evaluation test Details will be explained below.

[(A1) Microstructure observation of cross section]
Nine samples including each cross-sectional observation position C1 to C9 were collected from the steel material of each test number. Among the surfaces of each sample, the surface corresponding to the cross section CS was taken as the observation surface. On the observation plane, the observation field including the cross-sectional observation position was 0.5 mm x 1.0 mm.

After polishing the observation surface of the sample, the observation surface was etched using 3% nitric alcohol (nital etching solution). The observation field (0.5 mm x 1.0 mm) of the etched observation surface was observed using a 100x optical microscope. Phases were identified by contrast in the observation field.

The observed phases are shown in the "Phase" column of the "Cross Section" column in Table 3. In the "Phase" column of the "Cross section" column of Table 3, "○" is indicated when the microstructure at all cross section observation positions contains ferrite and the remainder consists of pearlite and/or bainite. In any test number, the microstructure of the cross section contained ferrite, and the remainder was pearlite and/or bainite.

[(A11) Arithmetic mean value of area fraction of ferrite in cross section]
The area (μm ² ) of ferrite in each observation field (each cross-sectional observation position) was determined. The area fraction (%) of ferrite in each observation field (each cross-sectional observation position) was determined using the area of ferrite and the area of the observation field.

The arithmetic mean value of the ferrite area fraction (%) in the nine observation fields (cross-sectional observation positions) is the arithmetic mean value (%) of the ferrite area fraction at the nine cross-sectional observation positions C1 to C9. defined. The arithmetic mean value of the obtained ferrite area fractions is shown in the "Ferrite area fraction (%)" column of the "Cross section" column of Table 3.

[(A12) Standard deviation of area fraction of ferrite in cross section]
The standard deviation (%) of the ferrite area fraction at nine cross-sectional observation positions C1 to C9 was calculated from the ferrite area fraction (%) at nine observation fields (cross-sectional observation positions). The obtained standard deviation is shown in the "Standard deviation of ferrite area fraction (%)" column in the "Cross section" column of Table 3.

[(A13) Ferrite average grain size ratio of cross section]
Furthermore, the area (μm ² ) of each ferrite grain observed in each of the above-mentioned observation fields (each cross-sectional observation position C1 to C9) was measured. The arithmetic mean value of the area of each ferrite grain was determined at each cross-sectional observation position C1 to C9. The circle-equivalent diameter of the arithmetic mean value of the obtained area was defined as the average grain size (μm) of ferrite at each cross-sectional observation position C1 to C9.

The average grain size of ferrite at nine cross-sectional observation positions C1 to C9 was determined. Then, among the average grain sizes of these ferrites, the maximum average grain size (μm) and the minimum average grain size (μm) of ferrite were specified. The ratio of the maximum average grain size to the specified minimum average grain size (ferrite average grain size ratio) was determined. The obtained ferrite average particle size ratio is shown in the "Ferrite particle size ratio" column of the "Cross section" column of Table 3.

[(B1) Observation of microstructure in longitudinal section]
Nine samples were collected from the steel materials of each test number, including the longitudinal section observation positions L1 to L9. Among the surfaces of each sample, the surface corresponding to the longitudinal section LS was used as the observation surface. On the observation surface, the observation field including the longitudinal section observation position was 0.5 mm x 1.0 mm.

After polishing the observation surface of the sample, the observation surface was etched using 3% nitric alcohol (nital etching solution). The observation field (0.5 mm x 1.0 mm) of the etched observation surface was observed using a 100x optical microscope. Phases were identified by contrast in the observation field.

The observed phases are shown in the "Phase" column of the "Longitudinal Section" column in Table 3. In the "phase" column of the "longitudinal section" column of Table 3, when the microstructure at all longitudinal section observation positions contains ferrite and the remainder consists of pearlite and/or bainite, "○" is indicated. In any test number, the microstructure of the longitudinal section contained ferrite, and the remainder was pearlite and/or bainite.

[(B11) Arithmetic mean value of area fraction of ferrite in longitudinal section]
The area (μm ² ) of ferrite in each observation field (each longitudinal section observation position) was determined. The area fraction (%) of ferrite in each observation field (each longitudinal section observation position) was determined using the area of ferrite and the area of the observation field.

The arithmetic mean value of the ferrite area fraction (%) in the nine observation fields (longitudinal section observation positions) is the arithmetic mean value (%) of the ferrite area fraction at the nine longitudinal section observation positions L1 to L9. defined. The arithmetic mean value of the obtained ferrite area fractions is shown in the "Ferrite area fraction (%)" column of the "Longitudinal section" column of Table 3.

[(B12) Standard deviation of area fraction of ferrite in longitudinal section]
The standard deviation (%) of the ferrite area fraction at the nine longitudinal section observation positions L1 to L9 was calculated from the ferrite area fraction (%) at the nine observation fields (vertical section observation positions). The obtained standard deviation is shown in the "Standard deviation of ferrite area fraction (%)" column in the "Vertical section" column of Table 3.

[(B13) Ferrite average grain size ratio in longitudinal section]
Furthermore, the area (μm ² ) of each ferrite grain observed in each of the above-mentioned observation fields (each longitudinal section observation position L1 to L9) was measured. The arithmetic mean value of the area of each ferrite grain was determined at each longitudinal section observation position L1 to L9. The circle-equivalent diameter of the arithmetic mean value of the obtained area was defined as the average grain size (μm) of ferrite at each longitudinal section observation position L1 to L9.

The average grain size of ferrite at nine vertical cross-sectional observation positions L1 to L9 was determined. Then, among the average grain sizes of these ferrites, the maximum average grain size (μm) and the minimum average grain size (μm) of ferrite were specified. The ratio of the maximum average grain size to the specified minimum average grain size (ferrite average grain size ratio) was determined. The obtained ferrite average particle size ratio is shown in the "Ferrite particle size ratio" column of the "Vertical section" column of Table 3.

[Evaluation test]
[(C1) Machinability evaluation test]
A machinability evaluation test was conducted using the following method. A steel bar with a diameter of 50 mm was subjected to heat treatment simulating hot forging and constant temperature annealing treatment. Specifically, a steel bar was heated to 1200°C and held at 1200°C for 30 minutes. Thereafter, the steel bar was allowed to cool to room temperature. Furthermore, it was heated at 950°C and held at 950°C for 1 hour. Furthermore, after holding at 650°C for 2 hours, it was allowed to cool to room temperature. After cooling, the steel bar was subjected to machining (cutting) to produce a test piece with a diameter of 45 mm and a length of 400 mm for machinability evaluation.

Perimeter turning was performed on the test piece of each test number, and tool life was evaluated. Specifically, outer circumferential turning was performed on the test pieces of each test number under the following conditions. The cutting tool used was an uncoated cemented carbide corresponding to P20 specified in JIS B 4053 (2013). The cutting speed was 250 m/min, the feed rate was 0.35 mm/rev, and the depth of cut was 1.0 mm. Water-soluble cutting oil was used during turning.

Perimeter turning was performed for 20 minutes under the above cutting conditions. Thereafter, the amount of flank wear (mm) of the cutting tool was measured.

The obtained flank wear amount (mm) is shown in the "wear amount (mm)" column of Table 3. When the amount of flank wear (mm) was less than 0.25 mm, it was determined that the machinability of the steel material was high. When the obtained flank wear amount (mm) was 0.25 mm or more, it was determined that the machinability of the steel material was low.

[(C2) Bending fatigue strength evaluation test]
From the steel materials (steel bars with a diameter of 50 mm) of each test number, intermediate products of Ono rotary bending test pieces for evaluating bending fatigue strength shown in FIG. 6 were processed. Numerical values in FIG. 6 indicate dimensions (unit: mm). "φ" in FIG. 6 means the diameter. "R1" means that the radius of curvature of the notch bottom is 1 mm.

Specifically, the steel materials (steel bars with a diameter of 50 mm) of each test number were heated at a heating temperature of 1200° C. and a holding time of 30 minutes. Thereafter, hot working (hot forging) was carried out at a finishing temperature of 950° C. or higher to produce a steel bar with a diameter of 35 mm. A steel bar with a diameter of 35 mm was machined (cutted) to produce an intermediate Ono rotary bending test piece. The diameter of the cross section of the intermediate product at the bottom of the notch was 8 mm. The intermediate product was subjected to carburizing treatment (gas carburizing treatment and tempering) to produce the Ono rotary bending test piece shown in FIG. The conditions of the carburizing treatment carried out are as follows.

[Gas carburizing treatment and tempering]
The test piece was heated at 950° C. for 240 minutes in an atmosphere with a carbon potential Cp1 of 0.8%. Subsequently, it was heated at 950° C. for 60 minutes in an atmosphere with a carbon potential Cp2 of 0.8%. Thereafter, it was heated at 850°C for 30 minutes and cooled with oil at 130°C. The oil-cooled test piece was tempered at a tempering temperature of 180° C. and a holding time of 120 minutes. After the holding time had elapsed, it was air cooled.

By the above gas carburizing method, the C concentration on the surface of the steel material (round bar) was adjusted to 0.80% by mass.

An Ono rotary bending fatigue test was conducted using the Ono rotary bending test piece after carburizing. Multiple test pieces were prepared for each test number. A fatigue test was conducted by changing the stress applied to each test piece, and after repeating 10 million times ( ¹⁰⁷ times), the highest stress that did not cause rupture was defined as the bending fatigue strength (MPa). In the Ono rotary bending fatigue test, the rotation speed was 3000 rpm and the stress ratio was varied.

The ratio of the bending fatigue strength of each test number to the bending fatigue strength of the reference steel was defined as the bending fatigue strength ratio. That is, the bending fatigue strength ratio (%) was determined using the following formula.
Bending fatigue strength ratio (%) = (Bending fatigue strength of each test number (MPa)/Bending fatigue strength of reference steel (MPa)) x 100

The obtained bending fatigue strength ratio (%) is shown in the "Bending fatigue strength ratio (%)" column of Table 3. It was determined that sufficient bending fatigue strength could be obtained if the obtained bending fatigue strength ratio was 110% or more. On the other hand, if the bending fatigue strength ratio was less than 110%, it was determined that the bending fatigue strength was low.

[(C3) Surface fatigue strength evaluation test]
Intermediate test pieces for the roller pitting fatigue test for the surface fatigue strength evaluation test shown in FIG. 7 were processed from the steel materials (steel bars with a diameter of 50 mm) of each test number. Numerical values in FIG. 7 indicate dimensions (unit: mm). "φ" in the figure means the diameter.

Specifically, the steel materials (steel bars with a diameter of 50 mm) of each test number were heated at a heating temperature of 1200° C. and a holding time of 30 minutes. Thereafter, hot working (hot forging) was carried out at a finishing temperature of 950° C. or higher to produce a steel bar with a diameter of 35 mm. A steel bar with a diameter of 35 mm was machined (cutting) to produce an intermediate product for a test piece for a roller pitting fatigue test. The intermediate product was subjected to carburizing treatment (gas carburizing treatment and tempering) under the above-mentioned carburizing treatment conditions to produce a test piece for roller pitting fatigue test (small roller test piece) shown in FIG.

FIG. 8 is a schematic diagram of a roller pitching fatigue test. As shown in FIG. 8, the small roller test piece 200 was rotated while pressing the large roller test piece 100 against the small roller test piece 200 with a surface pressure described below. The small roller test piece 200 was a test piece for a roller pitting fatigue test prepared by the above test piece method. The large roller test piece had the shape shown in FIG. Numerical values in FIG. 9 indicate dimensions (unit: mm). "R700" in the figure indicates that the radius of curvature of the outer peripheral surface was 700 mm.

The large roller test piece 100 was made of steel having a chemical composition corresponding to SCM420H specified in JIS G 4053 (2016), and the surface was polished after gas carburizing treatment under the same conditions as the small roller test piece 200. The diameter of the large roller test piece 100 was 130 mm.

In the roller pitting fatigue test, the large roller test piece 100 was pressed against the small roller test piece 200 with surface pressures of various Hertzian stresses. The circumferential speed direction of both roller test pieces at the contact part is the same direction, and the slip rate is -40% (the large roller test piece 100 has a circumferential speed of the contact part 40% higher than the small roller test piece 200). The test was conducted by rotating it. The oil temperature of ATF (lubricating oil for AT) supplied as a lubricating oil to the contact portion was 90° C., and the maximum surface pressure of the contact stress between the large roller test piece 100 and the small roller test piece 200 was 4000 MPa. The number of times the test was discontinued was 20 million times (2.0×10 ⁷ times). For each test number, after repeating 2.0×10 ⁷ times for a plurality of test pieces, the highest stress at which no pitting occurred was defined as surface fatigue strength (MPa).

The ratio of the surface fatigue strength of each test number to the surface fatigue strength of the reference steel was defined as the surface fatigue strength ratio. That is, the surface fatigue strength ratio (%) was determined using the following formula.
Surface fatigue strength ratio (%) = (surface fatigue strength (MPa) of each test number / surface fatigue strength (MPa) of reference steel) x 100

The obtained surface fatigue strength ratio (%) is shown in the "surface fatigue strength ratio (%)" column of Table 3. It was determined that sufficient surface fatigue strength could be obtained if the obtained surface fatigue strength ratio was 120% or more. On the other hand, if the surface fatigue strength ratio was less than 120%, it was determined that the surface fatigue strength was low.

[(C4) Heat treatment deformation evaluation test]
Gear simulation test pieces shown in FIG. 10A were produced from the steel materials (steel bars with a diameter of 50 mm) of each test number. Specifically, the steel materials (steel bars with a diameter of 50 mm) of each test number were heated at a heating temperature of 1200° C. and a holding time of 30 minutes. Thereafter, hot working (hot forging) was carried out at a finishing temperature of 950° C. or higher to produce a steel bar with a diameter of 35 mm. A steel bar with a diameter of 35 mm was machined (cutted) to produce a gear simulation test piece before gas carburizing treatment.

In FIG. 10A, the numerical value appended with "mm" indicates the dimension (unit: mm). "φ" in the figure means the diameter. The gear simulation test piece had a truncated cone shape. The gear simulation test piece had a circular upper surface with a diameter of 22 mm and a circular lower surface with a diameter of 34 mm. The gear simulation test piece had a cylindrical through hole TH including the central axis CL2. The diameter (inner diameter) of the through hole TH was 15 mm, and the central axis of the through hole TH coincided with the central axis of the gear simulating test piece.

The inner diameter (diameter) at each position in the longitudinal direction of the through hole TH of the produced gear simulation test piece before carburizing treatment was measured using a three-dimensional measuring machine. As a three-dimensional measuring machine, a CNC three-dimensional measuring machine (trade name: Crysta-Apex) manufactured by Mitutoyo Co., Ltd. was used.

Specifically, as shown in FIG. 10B, from the upper end to the lower end in the longitudinal direction of the through hole TH, in the range of 1.0 to 16.0 mm from the upper end, a total of 16 inner diameters are formed at 1.0 mm pitch positions. It was measured. Furthermore, the inner diameter was measured at a position of 0.5 mm from the upper end and at a position of 16.5 mm from the upper end in the longitudinal direction of the through hole TH from the upper end to the lower end. That is, the inner diameter of the through hole TH was measured at 18 measurement positions in the longitudinal direction of the through hole TH. Furthermore, at each measurement position, the inner diameter was measured at a total of 18 locations (points P1 to P18 in FIG. 10B) around the central axis CL2 at 10° pitches. Therefore, in the through hole TH, the inner diameter was measured at 18 measurement positions x 18 locations = 324 points.

After measuring the inner diameter, the gear simulation test piece was subjected to gas carburizing and tempering under the same conditions as the gas carburizing and tempering of the Ono rotary bending fatigue test piece. The inner diameter of the through hole TH of the gear simulating test piece after the carburizing process was measured using the same method as the method for measuring the inner diameter of the through hole TH of the gear simulating test piece before the carburizing process.

[Maximum deformation ratio of heat treatment]
At each point P1 to P18 at each measurement position of the through hole TH, the value obtained by subtracting the inner diameter after carburization (μm) from the inner diameter before carburization (μm) is determined by the heat treatment at each measurement point P1 to P18 at each measurement position. It was taken as the amount of deformation. For each test number, the maximum amount of heat treatment deformation was determined from the measurement results of a total of 324 points.

The ratio of the maximum heat treatment deformation of each test number to the maximum heat treatment deformation of the reference steel was defined as the "maximum deformation ratio." That is, the maximum deformation amount ratio (%) was determined using the following formula.
Maximum deformation ratio (%) = (Maximum heat treatment deformation of each test number (mm)/Maximum heat treatment deformation of reference steel (mm)) x 100

The obtained maximum deformation ratio (%) is shown in the "Maximum deformation ratio (%)" column of Table 3. If the obtained maximum deformation amount ratio was 90% or less, it was determined that the maximum deformation amount ratio was small. On the other hand, when the maximum deformation amount ratio exceeds 90%, it was determined that the maximum deformation amount ratio is large.

[Heat treatment deformation difference ratio]
For each test number, the maximum amount of heat treatment deformation and the minimum amount of heat treatment deformation were determined from the measurement results of a total of 324 points. The value obtained by subtracting the minimum heat treatment deformation amount from the obtained maximum heat treatment deformation amount was defined as the deformation amount difference (μm).

The ratio of the deformation difference of each test number to the deformation difference of the reference steel was defined as the deformation difference ratio. That is, the deformation amount difference ratio was determined using the following equation.
Deformation amount difference ratio (%) = (Deformation amount difference of each test number (μm) / Deformation amount difference of reference steel (μm)) × 100

The obtained deformation amount difference ratio (%) is shown in the "Deformation amount difference ratio (%)" column of Table 3. If the obtained deformation amount difference ratio was 90% or less, it was determined that the deformation amount difference ratio was small. On the other hand, when the deformation amount difference ratio exceeds 90%, it was determined that the deformation amount difference ratio is large.

When the maximum deformation amount ratio and the deformation amount difference ratio were both 90% or less, it was determined that heat treatment deformation was sufficiently suppressed three-dimensionally. When the maximum deformation amount ratio and/or the deformation amount difference ratio exceeds 90%, it was determined that heat treatment deformation was not sufficiently suppressed.

[Test results]
Table 3 shows the test results. Referring to Table 3, in the chemical compositions of the steel materials of test numbers 5 to 9, the content of each element was appropriate, and F1 satisfied formula (1). Furthermore, the manufacturing conditions for steel materials with test numbers 5 to 9 were also appropriate. Therefore, the microstructure of the steel material was appropriate. Specifically, the microstructures of the cross sections of Test Nos. 5 to 9 contained ferrite, with the remainder consisting of pearlite and/or bainite. Further, the arithmetic mean value of the area fraction of ferrite was 50 to 70%, the standard deviation of the area fraction of ferrite was 4.0% or less, and the ferrite average particle size ratio was 2.00 or less. Further, the microstructures of the longitudinal sections of Test Nos. 5 to 7 contained ferrite, with the remainder consisting of pearlite and/or bainite. Further, the arithmetic mean value of the area fraction of ferrite was 50 to 70%, the standard deviation of the area fraction of ferrite was 4.0% or less, and the ferrite average particle size ratio was 2.00 or less.

Therefore, in the machinability evaluation test, the amount of flank wear was less than 0.25 mm, indicating high machinability. Furthermore, the bending fatigue strength ratio was 110% or more, the surface fatigue strength ratio was 120% or more, and both the bending fatigue strength and the surface fatigue strength were excellent. Furthermore, the maximum deformation amount ratio and deformation amount difference ratio in heat treatment were 90% or less, and heat treatment deformation was sufficiently suppressed three-dimensionally.

On the other hand, in test number 1, the Si content was too low. Furthermore, F1 did not satisfy formula (1). Furthermore, the holding time of the blooming process was less than 10 hours. Therefore, the standard deviation of the area fraction of ferrite in the cross section and the longitudinal section exceeded 4.0%. As a result, the bending fatigue strength and surface fatigue strength were low. Furthermore, the maximum deformation amount ratio and deformation amount difference ratio in heat treatment exceeded 90%, and heat treatment deformation was not sufficiently suppressed.

In test numbers 2 to 4, the holding time in the blooming process was less than 10 hours. Therefore, the standard deviation of the area fraction of ferrite in the cross section and the longitudinal section exceeded 4.0%. As a result, the deformation amount difference ratio during heat treatment exceeded 90%, and heat treatment deformation was not sufficiently suppressed.

In test numbers 10 to 12, the heating temperature in the blooming process was too low. Therefore, the standard deviation of the area fraction of ferrite in the cross section and the longitudinal section exceeded 4.0%. As a result, the deformation amount difference ratio during heat treatment exceeded 90%, and heat treatment deformation was not sufficiently suppressed.

In test numbers 13 to 15, the heating temperature in the finish rolling process was too low. Therefore, the ferrite average grain size ratio of the cross section and the longitudinal section exceeded 2.00. As a result, the deformation amount difference ratio during heat treatment exceeded 90%, and heat treatment deformation was not sufficiently suppressed.

In test numbers 16 to 18, the holding time in the finish rolling process was too short. Therefore, the ferrite average grain size ratio of the cross section and the longitudinal section exceeded 2.00. As a result, the deformation amount difference ratio during heat treatment exceeded 90%, and heat treatment deformation was not sufficiently suppressed.

In test numbers 19 to 21, the finishing temperature in the finish rolling process was too high. Therefore, the ferrite average grain size ratio of the cross section and the longitudinal section exceeded 2.00. As a result, the deformation amount difference ratio during heat treatment exceeded 90%, and heat treatment deformation was not sufficiently suppressed.

In test numbers 22 to 24, the finishing temperature in the finish rolling process was too low. Therefore, the ferrite average grain size ratio of the cross section and the longitudinal section exceeded 2.00. As a result, the deformation amount difference ratio during heat treatment exceeded 90%, and heat treatment deformation was not sufficiently suppressed.

In test numbers 25 to 27, the cooling rate in the cooling process was too slow. Therefore, the arithmetic mean value of the area fraction of ferrite in the cross section and the longitudinal section exceeded 70%. Therefore, the deformation amount difference ratio during heat treatment exceeded 90%, and heat treatment deformation was not sufficiently suppressed.

In test numbers 28 and 29, the cooling rate in the cooling process was too fast. Therefore, the arithmetic mean value of the area fraction of ferrite in the cross section and the longitudinal section was less than 50%. Therefore, the flank wear amount was 0.25 mm or more. As a result, the machinability of the steel material was low.

In test number 30, the cooling rate in the temperature holding step was too fast. Therefore, in the microstructure of the longitudinal section, the ferrite average grain size ratio exceeded 2.00. Therefore, the deformation amount difference ratio during heat treatment exceeded 90%, and heat treatment deformation was not sufficiently suppressed.

Similarly to Example 1, steel materials having the chemical composition shown in Table 4 were prepared.

Steel materials were manufactured by the following method. Using manufacturing conditions b in Table 2 for molten steel, steel materials (steel bars) with test numbers 1 to 32 shown in Table 5 were manufactured in the same manner as in Example 1.

[Evaluation test]
The same measurements and evaluation tests as in Example 1 were carried out using the same method as in Example 1 on the steel material (steel bar) manufactured in the above manufacturing process. In the (C2) bending fatigue strength evaluation test, (C3) plane fatigue strength evaluation test, and (C4) heat treatment deformation evaluation test, the reference steels shown in Table 1 were used as reference steels.

[Test results]
Table 5 shows the test results. Referring to Table 5, in the chemical compositions of the steel materials of test numbers 1 to 17, the content of each element was appropriate, and F1 satisfied formula (1). Furthermore, the manufacturing conditions for the steel materials of test numbers 1 to 17 were also appropriate. Therefore, the microstructure of the steel material was appropriate. Specifically, the microstructure of the cross section of test numbers 1 to 17 consists of ferrite, pearlite, and/or bainite, the arithmetic mean value of the area fraction of ferrite is 50 to 70%, and the area fraction of ferrite is The standard deviation of was 4.0% or less, and the ferrite average particle size ratio was 2.00 or less. The microstructures of the longitudinal sections of test numbers 1 to 17 consist of ferrite, pearlite, and/or bainite, the arithmetic mean value of the area fraction of ferrite is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4. 0% or less, and the ferrite average particle size ratio was 2.00 or less. Therefore, the amount of flank wear was less than 0.25 mm, and machinability was high. Furthermore, the bending fatigue strength ratio was 110% or more, the surface fatigue strength ratio was 120% or more, and both the bending fatigue strength and the surface fatigue strength were excellent. Furthermore, the maximum deformation amount ratio and deformation amount difference ratio in heat treatment were 90% or less, and heat treatment deformation was sufficiently suppressed.

On the other hand, in test numbers 18 to 23, F1 was too high. Therefore, the maximum deformation amount ratio during heat treatment exceeded 90%, and heat treatment deformation was not sufficiently suppressed.

In test number 24, the C content was too high. Therefore, the flank wear amount was 0.25 mm or more, and machinability was low.

In test number 25, the Si content was too low. Therefore, the surface fatigue strength ratio was less than 120%, and the surface fatigue strength was low.

Test number 26 had too high a Si content. Therefore, the bending fatigue strength ratio was less than 110%, and the bending fatigue strength was low.

Test number 27 had too low Mn content. Therefore, the bending fatigue strength ratio was less than 110%, and the surface fatigue strength ratio was less than 120%. As a result, the bending fatigue strength and surface fatigue strength were low.

In test number 28, the Mn content was too high. Therefore, the bending fatigue strength ratio was less than 110%, and the surface fatigue strength ratio was less than 120%. As a result, the bending fatigue strength and surface fatigue strength were low.

Test number 29 had too low Cr content. Therefore, the bending fatigue strength ratio was less than 110%, and the surface fatigue strength ratio was less than 120%. As a result, both bending fatigue strength and surface fatigue strength were insufficient.

In test number 30, the Cr content was too high. Therefore, the flank wear amount was 0.25 mm or more, and machinability was low.

Test number 31 had too high Mo content. Therefore, the flank wear amount was 0.25 mm or more, and machinability was low.

In test number 32, the Nb content was too high. Therefore, the bending fatigue strength ratio was less than 110%, and the bending fatigue strength was low.

The embodiments of the present disclosure have been described above. However, the embodiments described above are merely examples for implementing the present disclosure. Therefore, the present disclosure is not limited to the embodiments described above, and the embodiments described above can be modified and implemented as appropriate without departing from the spirit thereof.

Claims (2)

A steel material,
The chemical composition is in mass%,
C: 0.20-0.25%,
Si: 0.40 to 0.70%,
Mn: 0.50-0.90%,
Cr: 1.00-2.00%,
S: 0.005-0.050%,
N: 0.0050-0.0200%,
Al: 0.001-0.100%,
O: 0.0050% or less, and
P: Contains 0.030% or less,
the remainder consists of Fe and impurities, and satisfies formula (1),
In a cross section that is perpendicular to the longitudinal direction of the steel material and has a circular shape with a radius R,
The center position of the cross section, and the eight R/2 positions that are R/2 positions in the radial direction from the center of the cross section and are arranged at a pitch of 45° around the center of the cross section, When defined as nine cross-sectional observation positions,
The microstructure at each cross-sectional observation position contains ferrite, and the remainder consists of pearlite and/or bainite,
The arithmetic mean value of the area fraction of ferrite at the nine cross-sectional observation positions is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less,
Among the average grain sizes of ferrite at the nine cross-sectional observation positions, the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less,
In a longitudinal section that is parallel to the longitudinal direction of the steel material and includes the central axis of the steel material,
Three center axis positions arranged at an R/2 pitch on the center axis, and six R/2 positions arranged at R/2 positions in the radial direction from each center axis position. , when defined as nine longitudinal section observation positions,
The microstructure at each longitudinal section observation position contains ferrite, and the remainder consists of pearlite and/or bainite,
The arithmetic mean value of the area fraction of ferrite at the nine longitudinal section observation positions is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less,
Among the average grain sizes of ferrite at the nine longitudinal cross-sectional observation positions, the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less,
Steel material.
1-(0.5C+0.03Si+0.06Mn+0.01Cr+0.05Mo)<0.800 (1)
Here, the content (mass %) of the corresponding element is substituted for each element symbol in formula (1). If the corresponding element is not contained, "0" is assigned to the element symbol. The steel material according to claim 1,
The chemical composition further includes, in place of a portion of the Fe,
Mo: 0.30% or less,
Nb: 0.050% or less,
Ti: 0.020% or less,
Cu: 0.50% or less,
Ni: 0.80% or less,
V: 0.30% or less,
Mg: 0.0035% or less,
Ca: 0.0030% or less, and
Rare earth element: Contains one or more elements selected from the group consisting of 0.0050% or less,
Steel material.

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