WO2022071420A1 - Matériau d'acier - Google Patents

Matériau d'acier Download PDF

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Publication number
WO2022071420A1
WO2022071420A1 PCT/JP2021/035935 JP2021035935W WO2022071420A1 WO 2022071420 A1 WO2022071420 A1 WO 2022071420A1 JP 2021035935 W JP2021035935 W JP 2021035935W WO 2022071420 A1 WO2022071420 A1 WO 2022071420A1
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Prior art keywords
steel material
ferrite
less
cross
section
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PCT/JP2021/035935
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English (en)
Japanese (ja)
Inventor
聡 志賀
豊 根石
雄介 河原木
誠 江頭
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日本製鉄株式会社
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Priority to CN202180066574.7A priority Critical patent/CN116234938A/zh
Priority to JP2022554054A priority patent/JP7385160B2/ja
Publication of WO2022071420A1 publication Critical patent/WO2022071420A1/fr

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    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C38/00—Ferrous alloys, e.g. steel alloys
    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C38/00—Ferrous alloys, e.g. steel alloys
    • C22C38/60—Ferrous alloys, e.g. steel alloys containing lead, selenium, tellurium, or antimony, or more than 0.04% by weight of sulfur
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D1/00—General methods or devices for heat treatment, e.g. annealing, hardening, quenching or tempering
    • C21D1/06—Surface hardening
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D8/00—Modifying the physical properties by deformation combined with, or followed by, heat treatment
    • C21D8/06—Modifying the physical properties by deformation combined with, or followed by, heat treatment during manufacturing of rods or wires
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D9/00—Heat treatment, e.g. annealing, hardening, quenching or tempering, adapted for particular articles; Furnaces therefor
    • C21D9/28—Heat treatment, e.g. annealing, hardening, quenching or tempering, adapted for particular articles; Furnaces therefor for plain shafts
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D9/00—Heat treatment, e.g. annealing, hardening, quenching or tempering, adapted for particular articles; Furnaces therefor
    • C21D9/32—Heat treatment, e.g. annealing, hardening, quenching or tempering, adapted for particular articles; Furnaces therefor for gear wheels, worm wheels, or the like

Definitions

  • This disclosure relates to steel materials, and more particularly to steel materials suitable for materials for machine structural parts manufactured by performing gas carburizing treatment.
  • the gas carburizing treatment also includes the gas carburizing nitriding treatment. Further, in the present specification, the gas carburizing treatment includes a gas carburizing step (including a gas carburizing nitriding step) and a quenching step after the gas carburizing step.
  • Mechanical structural parts are represented by, for example, gears and shafts of automobiles and construction vehicles.
  • alloy steel materials for machine structure represented by SCr420, SCM420, and SNCM420 specified in JIS G4053 (2016) are used.
  • These steel materials are manufactured into machine structural parts by, for example, the following manufacturing process. Forging (hot forging or cold forging) and / or cutting is performed on the steel material to produce an intermediate product having a desired shape. The intermediate product is subjected to heat treatment (quenching and tempering, carburizing treatment, carburizing nitriding treatment, etc.) to adjust the hardness and microstructure of the intermediate product.
  • Heat treatment quenching and tempering, carburizing treatment, carburizing nitriding treatment, etc.
  • the steel material used as the material for machine structural parts is required to have high machinability.
  • Gas carburizing treatment and gas carburizing nitriding treatment are known as methods for increasing bending fatigue strength and surface fatigue strength of mechanical structural parts.
  • a hardened layer (carburized layer or carburized nitriding layer) is formed on the surface layer of the mechanical structural component. This hardened layer improves bending fatigue strength and surface fatigue strength of mechanical structural parts.
  • gas carburizing treatment gas carburizing treatment and gas carburizing nitriding treatment
  • the mechanical structural parts are easily deformed.
  • the deformation of the mechanical structural parts during the gas carburizing process is referred to as heat treatment deformation. Due to heat treatment deformation, the shape of mechanical structural parts is distorted. Distortion of the shape of mechanical structural parts causes noise and vibration when driving 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.
  • Patent Document 1 JP-A-9-137266
  • Patent Document 2 JP-A-11-50191
  • the steel material disclosed in Patent Document 1 is C: 0.03 to 0.40%, Mn: 2.0% or less, Si: 2.0% or less, Al: 0.015 to 0.06 in mass%. %, N: 0.005 to 0.03%, P: 0 to 0.030%, balance: Fe and unavoidable impurities.
  • Patent Document 1 the surface integral of the proeutectoid ferrite of the structure of the core of the machine structural component after the carburizing treatment is set to 20 to 80% according to the above configuration. As a result, heat treatment deformation of the steel material is suppressed.
  • the carbonized shaft-shaped parts disclosed in Patent Document 2 have a mass% of C: 0.10 to 0.35%, Si: 0.02 to 0.50%, Mn: 0.30 to 1.80%, and S: 0.005 to 0.15%, Al: 0.015 to 0.040%, Nb: 0.005 to 0.040%, N: 0.0060 to 0.0200%, P: 0.025%
  • Mo 0.02 to 1.0%
  • Ni 0.1. It contains one or more of ⁇ 3.5%
  • V 0.03 ⁇ 0.5%
  • the balance consists of iron and unavoidable impurities.
  • Nb (CN), AlN, or a composite precipitate of Nb (CN) and AlN having a diameter of 0.1 ⁇ m or less is dispersed in a total of 80 pieces / 100 ⁇ m 2 or more, and the austenite particle size. Is 8 or more.
  • Patent Document 2 coarse particles during carburizing are suppressed. As a result, heat treatment deformation of the steel material is suppressed.
  • Patent Document 3 International Publication No. 2014/0385848
  • Patent Document 4 Japanese Patent Application Laid-Open No. 2013-108144
  • Patent Document 5 Japanese Patent Application Laid-Open No. 2013-151719. It is proposed in Japanese Patent Publication No. 5 (Patent Document 5).
  • the steel material disclosed in Patent Document 3 is C: 0.20 to 0.30%, Si: 0.10 to 1.50%, Mn: 0.10 to 1.20%, P: 0 in mass%. .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 consists of the balance Fe and unavoidable impurities.
  • the martensitic transformation start temperature (Ms point) is 460 ° C. or lower.
  • the hardness at the position where the distance from the hardened end of the steel material measured by the Jominy type one-sided quenching method is 1.5 mm is defined as J1.5
  • the hardness at the position where the distance from the hardened end is 9 mm is defined as J1.5.
  • the hardness at a position of 11 mm from the quenching end is defined as J11
  • (J9 / J1.5) is 0.70 to 0.85
  • (J11 / J1. 5) is 0.67 to 0.78.
  • the Ms point is set low and the hardness is adjusted to a predetermined range. As a result, heat treatment deformation of the steel material is suppressed.
  • the steel material disclosed in Patent Document 4 is C: 0.10 to 0.25%, Si: 0.01 to 0.10%, Mn: 0.40 to 1.00%, S: 0 in mass%. .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% It is contained, and the balance is composed of Fe and impurities, and P, Ti and O (oxygen) in the impurities are P: 0.025% or less, Ti: 0.003% or less, O: 0.0020% or less, respectively. ..
  • the steel material disclosed in Patent Document 5 is, in mass%, C: 0.1 to 0.3%, Si: 0.01 to 0.6%, Mn: 0.4 to 1.0%, 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 balance is 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, respectively. be.
  • the difference value between the maximum value and the minimum value of the Ms points at 17 measurement positions in the cross section perpendicular to the longitudinal direction of the steel material is 10 or less.
  • the microstructure of this steel is composed of ferrite and pearlite and / or bainite. Further, in this steel material, the ratio of the maximum value to the minimum value of the average particle size of ferrite in the cross section is 2.0 or less.
  • Patent Document 4 and Patent Document 5 variation in the Ms point in the cross section of the steel material is suppressed. As a result, heat treatment deformation of the steel material is suppressed.
  • Japanese Unexamined Patent Publication No. 9-13726 Japanese Unexamined Patent Publication No. 11-50191 International Publication No. 2014/0385848 Japanese Unexamined Patent Publication No. 2013-108144 Japanese Unexamined Patent Publication No. 2013-151719
  • An object of the present disclosure is a steel material having excellent machinability, having excellent bending fatigue strength and surface fatigue strength after gas carburizing treatment, and capable of suppressing heat treatment deformation after gas carburizing treatment. Is to provide.
  • the steel material of the present disclosure has the following constitution.
  • the chemical composition is by mass%, C: 0.20 to 0.25%, Si: 0.40 to 0.70%, Mn: 0.50 to 0.90%, Cr: 1.00 to 2.00%, S: 0.005 to 0.050%, N: 0.0050-0.0200%, Al: 0.001 to 0.100%, O: 0.0050% or less, and P: Contains 0.030% or less,
  • the balance consists of Fe and impurities and satisfies the formula (1).
  • the microstructure at each cross-sectional observation position contains ferrite and the rest consists of pearlite and / or bainite.
  • the arithmetic mean value of the area fraction of the ferrite at the nine cross-sectional observation positions is 50 to 70%, and the standard deviation of the area fraction of the ferrite is 4.0% or less.
  • the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less.
  • Three central axis positions arranged at R / 2 pitch on the central axis, and six R / 2 positions arranged at R / 2 positions in the radial direction from each central axis position. When defined as 9 vertical cross-sectional observation positions, The microstructure at each longitudinal section observation position contains ferrite and the rest consists of pearlite and / or bainite.
  • the arithmetic mean value of the area fraction of ferrite at the nine vertical cross-sectional observation positions is 50 to 70%, and the standard deviation of the area fraction of the ferrite is 4.0% or less.
  • the ratio of the maximum average particle size to the minimum average particle size is 2.00 or less.
  • the content (mass%) of the corresponding element is substituted for each element symbol in the formula (1). If the corresponding element is not contained, "0" is substituted for 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. 2 is a schematic cross-sectional view of the steel material of the present embodiment, which is a cross section perpendicular to the longitudinal direction.
  • FIG. 3 is a schematic view of a vertical cross section that is parallel to the longitudinal direction of the steel material of the present embodiment and is a cross section including a central axis.
  • FIG. 4 is a schematic diagram of the band structure.
  • FIG. 5 is a diagram showing an example of heat patterns in the gas carburizing step and the quenching step.
  • FIG. 6 is a plan view of the Ono-type rotary bending test piece produced in the example.
  • FIG. 7 is a plan view of the test piece for the roller pitching fatigue test produced in the example.
  • FIG. 8 is a schematic diagram for explaining a roller pitching fatigue test.
  • FIG. 9 is a front view of the large roller test piece produced in the example.
  • FIG. 10A is a perspective view of the gear simulation test piece produced in the example.
  • FIG. 10B is a perspective view of the through hole in FIG. 10A.
  • the present inventors have excellent machinability, have excellent bending fatigue strength and surface fatigue strength when subjected to gas carburizing treatment to obtain mechanical structural parts, and after gas carburizing treatment.
  • the present inventors first examined a steel material having excellent machinability and further having excellent bending fatigue strength and surface fatigue strength after gas carburizing treatment from the viewpoint of chemical composition.
  • the chemical composition was C: 0.20 to 0.25%, Si: 0.40 to 0.70%, Mn: 0.50 to 0.90%, Cr: 1.00 in mass%. ⁇ 2.00%, S: 0.005 to 0.050%, N: 0.0050 to 0.0200%, Al: 0.001 to 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%, A 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 being Fe and impurities. If so, it is considered that it has excellent machinability and may 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 at each part of the steel material is as uniform as possible, specifically, if the variation in the phase composition of the microstructure at each part in the steel material and the variation in the crystal grains are suppressed, the 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 composition and the crystal grain size at each part of the steel material.
  • the present inventors first focused on the variation in microstructure in the cross section, which is the cross section perpendicular to the longitudinal direction of the steel material.
  • the cross-sectional observation position which is the observation position of the microstructure in the cross section.
  • the center position of the cross section and the position of R / 2 in the radial direction from the center of the cross section are arranged at a pitch of 45 ° around the center of the cross section 8
  • the R / 2 position of the location is defined as the cross-sectional observation position of 9 locations.
  • the present inventors investigated and examined the microstructure at each cross-sectional observation position. As a result of the examination, it was found that the heat treatment deformation after the gas carburizing treatment is suppressed if the microstructure at the cross-sectional observation position meets the following requirements.
  • the microstructure at each cross-sectional observation position contains ferrite, and the balance consists of pearlite and / or bainite.
  • 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.
  • the ratio of the maximum average particle size to the minimum average particle size is 2.00 or less.
  • the present inventors paid attention not only to the variation in the microstructure of the cross section of the steel material but also to the variation of the microstructure of the vertical cross section of the steel material. Then, in order to quantify the variation of the microstructure in the vertical section, the vertical section observation position, which is the observation position of the microstructure in the vertical section, is defined as follows.
  • the present inventors investigated and examined the microstructure at each vertical cross-sectional observation position. As a result of the examination, if the microstructure at the cross-sectional observation position meets the above requirements and the microstructure at the vertical cross-section observation position meets the following requirements, the heat treatment deformation after the gas carburizing treatment is sufficiently suppressed. There was found.
  • the microstructure at each vertical cross-sectional observation position contains ferrite, and the balance consists of pearlite and / or bainite.
  • the arithmetic mean value of the area fraction of ferrite at nine vertical cross-sectional observation positions is 50 to 70%, and the standard deviation of the area fraction of ferrite is 4.0% or less.
  • the ratio of the maximum average particle size to the minimum average particle size is 2.00 or less.
  • the present inventors focused on martensitic transformation after gas carburizing treatment. Then, the present inventors investigated in detail the mechanism of occurrence of martensitic transformation during gas carburizing and quenching.
  • Patent Documents 3 to 5 heat treatment deformation is suppressed by suppressing the transformation time of martensite from being varied depending on each part in the steel material during gas carburizing and quenching. Specifically, in Patent Document 3, by setting the Ms point to 460 ° C. or lower, it is possible to prevent the martensitic transformation time from being significantly deviated at each site of the steel material. In Patent Documents 4 and 5, by suppressing the variation in the Ms point at each part of the steel material, it is possible to prevent the martensitic transformation time from being significantly deviated at each part of the steel material.
  • the present inventors first used a steel material having the above-mentioned chemical composition and, as in Patent Documents 3 to 5, set the same martensitic transformation time at each site of the steel material to perform heat treatment deformation. I tried to suppress it. Specifically, it is possible to suppress heat treatment deformation by suppressing variations in the microstructure at each part of the steel material (cross-section observation position, vertical cross-section observation position) and by suppressing variations in the Ms point of each part as much as possible. I tried.
  • the microstructural changes of the steel material during the vacuum carburizing treatment occur as follows.
  • quenching time quenching time
  • martensitic transformation starts in a part of the inside of the steel material first. After that, as time progresses, martensitic transformation progresses from the central part toward the surface layer part. That is, the martensitic transformation occurs not from the surface layer of the steel material but from the inside of the steel material.
  • 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 on the surface layer of the steel material is lower than the Ms point inside the steel material. Further, even if it is possible to make the Ms points uniform in each part inside the steel material, the cooling rates of each part are not completely the same due to the shape of the steel material. Therefore, when the quenching time is divided into minute times, the martensitic transformation starts from each part of the steel material where the cooling rate inside the steel material is high. Therefore, at the time of quenching of the gas carburizing treatment, a minute time zone in which the martensitic transformed portion and the martensitic untransformed portion coexist always occurs.
  • the present inventors do not suppress heat treatment deformation by making the martensitic transformation time as similar as possible as in the technical idea disclosed in Patent Documents 3 to 5, but gas carburizing treatment.
  • the means for suppressing the heat treatment deformation was investigated.
  • the untransformed part of martensite is softer than the transformed part of martensite.
  • the martensitic transformational 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 part of the steel material undergoes martensitic transformation during quenching, and the martensitic transformed portion and the martensitic untransformed portion coexist, the martensitic untransformed portion is distorted. It is considered that this strain causes heat treatment deformation.
  • the present inventors assume that there is a minute time zone in which the martensite transformed portion and the martensite untransformed portion coexist during the gas carburizing treatment, and when the martensite transformed portion is generated, the present inventors It was considered that if the strength of the untransformed martensite portion could be kept high, the occurrence of distortion in the untransformed martensite portion could be suppressed, and as a result, the heat treatment deformation could be suppressed.
  • the present inventors further investigated a means for maintaining high strength of the martensitic untransformed portion when the martensitic transformed portion is generated during quenching of the gas carburizing treatment.
  • the martensitic untransformed portion is strengthened in the temperature range where the martensitic transformed portion is generated. It is effective to appropriately contain the elements to be used.
  • the present inventors considered that C, Si, Mn, Cr and Mo are effective as elements for increasing the strength of the martensitic untransformed portion in the temperature range where the martensitic transformed portion is generated. .. Therefore, the relationship between these elements and the amount of heat treatment deformation during quenching of the gas carburizing treatment was further investigated. As a result, it was found that the heat treatment deformation was remarkably suppressed by further satisfying the following formula (1) in the steel material having the above-mentioned chemical composition.
  • 1- 0.5C + 0.03Si + 0.06Mn + 0.01Cr + 0.05Mo
  • the content (mass%) of the corresponding element is substituted for each element symbol in the formula (1). If the corresponding element is not contained, "0" is substituted for the element symbol.
  • FIG. 1 shows the F1 value and the maximum in a steel material in which the content of each element in the chemical composition is within the above range and the variation in microstructure at the cross-sectional observation position and the vertical cross-sectional observation position satisfies the above-mentioned requirements. It is a figure which shows the relationship with the deformation amount ratio (%).
  • the maximum deformation 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 later.
  • the content of each element in the chemical composition is within the above range, and the microstructure at the cross-sectional observation position and the vertical cross-sectional observation position satisfies the above-mentioned conditions (1) to (6).
  • the maximum deformation amount ratio decreases as F1 decreases.
  • F1 is less than 0.800
  • the present inventors suppress the variation in the microstructure of the cross-sectional observation position and the vertical section observation position in the steel material having the above-mentioned chemical composition, and suppress the variation in the occurrence timing of martensitic transformation during quenching to some extent.
  • F1 is set to less than 0.800 to have excellent machinability. 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 the present embodiment completed based on the above knowledge has the following constitution.
  • the microstructure at each cross-sectional observation position contains ferrite and the rest consists of pearlite and / or bainite.
  • the arithmetic mean value of the area fraction of the ferrite at the nine cross-sectional observation positions is 50 to 70%, and the standard deviation of the area fraction of the ferrite is 4.0% or less.
  • the ratio of the maximum average grain size to the minimum average grain size is 2.00 or less.
  • Three central axis positions arranged at R / 2 pitch on the central axis, and six R / 2 positions arranged at R / 2 positions in the radial direction from each central axis position. When defined as 9 vertical cross-sectional observation positions, The microstructure at each longitudinal section observation position contains ferrite and the rest consists of pearlite and / or bainite.
  • the arithmetic mean value of the area fraction of ferrite at the nine vertical cross-sectional observation positions is 50 to 70%, and the standard deviation of the area fraction of the ferrite is 4.0% or less.
  • the ratio of the maximum average particle size to the minimum average particle size is 2.00 or less.
  • the content (mass%) of the corresponding element is substituted for each element symbol in the formula (1). If the corresponding element is not contained, "0" is substituted for the element symbol.
  • the chemical composition of the steel material of this embodiment contains the following elements.
  • Carbon (C) increases the strength of the steel material. If the C content is less than 0.20%, the above effect cannot be sufficiently obtained even if the content of other elements is within the range of the present embodiment. On the other hand, if the C content exceeds 0.25%, the hardenability becomes excessively high even if the content of other elements is within the range of the present embodiment. In this case, the hardness of the steel material after the gas carburizing treatment becomes hard. As a result, the machinability of the steel material is reduced. Therefore, the C content is 0.20 to 0.25%.
  • the lower limit of the C content is preferably 0.21%, more preferably 0.22%.
  • the preferred upper limit of the C content is 0.24%, more preferably 0.23%.
  • Si 0.40 to 0.70%
  • Silicon (Si) enhances the hardenability of the steel material and enhances the strength of the steel material. Si also enhances the temper softening resistance of the hardened layer of mechanical structural parts. Therefore, the surface fatigue strength of the mechanical structural parts is increased. If the Si content is less than 0.40%, the above effect cannot be sufficiently obtained even if the content of other elements is within the range of the present embodiment. On the other hand, if the Si content exceeds 0.70%, the intergranular oxide layer after the gas carburizing treatment becomes excessively deep even if the content of other elements is within the range of the present embodiment. In this case, the bending fatigue strength of the mechanical structural parts is reduced. Therefore, the Si content is 0.40 to 0.70%.
  • the preferred lower limit of the Si content is 0.41%, more preferably 0.42%, still more preferably 0.45%, still more preferably 0.47%, still more preferably 0.50. %.
  • the preferred upper limit of the Si content is 0.69%, more preferably 0.67%, still more preferably 0.65%, still more preferably 0.63%.
  • Mn 0.50 to 0.90%
  • Manganese (Mn) enhances the hardenability of steel materials and enhances the bending fatigue strength and surface fatigue strength of mechanical structural parts. If the Mn content is less than 0.50%, the above effect cannot be sufficiently obtained even if the content of other elements is within the range of the present embodiment. On the other hand, if the Mn content exceeds 0.90%, the formation of Mn oxide is promoted on the surface layer of the mechanical structural parts during the gas carburizing treatment even if the content of other elements is within the range of this embodiment. Will be done. In this case, the grain boundary oxide layer of the mechanical structural component becomes excessively deep. Therefore, the bending fatigue strength of the mechanical structural parts is reduced.
  • the Mn oxide formed on the surface layer of the mechanical structural component further causes surface origin peeling. If surface origin peeling occurs, the surface fatigue strength of mechanical structural parts decreases. Therefore, the Mn content is 0.50 to 0.90%.
  • the preferred lower limit of the Mn content is 0.51%, more preferably 0.52%, still more preferably 0.55%, still more preferably 0.60%.
  • the preferred upper limit of the Mn content is 0.89%, more preferably 0.87%, still more preferably 0.85%.
  • Chromium (Cr) enhances the hardenability of steel materials and enhances bending fatigue strength and surface fatigue strength of mechanical structural parts. If the Cr content is less than 1.00%, the above effect cannot be sufficiently obtained even if the content of other elements is within the range of the present embodiment. On the other hand, if the Cr content exceeds 2.00%, the steel material becomes too hard even if the content of other elements is within the range of the present embodiment. In this case, the machinability of the steel material is reduced. Therefore, the Cr content is 1.00 to 2.00%.
  • the preferred lower limit of the Cr content is 1.10%, more preferably 1.20%, still more preferably 1.40%, still more preferably 1.60%, still more preferably 1.70%. %, More preferably 1.80%.
  • the preferred upper limit of the Cr content is less than 2.00%, more preferably 1.95%, still more preferably 1.90%.
  • S 0.005 to 0.050%
  • Sulfur (S) combines with Mn to form MnS.
  • MnS enhances the machinability of steel materials. If the S content is less than 0.005%, the above effect cannot be sufficiently obtained even if the content of other elements is within the range of the present embodiment. On the other hand, if the S content exceeds 0.050%, an excessively large amount of MnS is formed even if the content of other elements is within the range of the present embodiment. In this case, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are reduced. Therefore, the S content is 0.005 to 0.050%.
  • the lower limit of the S content is preferably 0.007%, more preferably 0.010%, still more preferably 0.013%, still more preferably 0.015%.
  • the preferred upper limit of the S content is 0.049%, more preferably 0.045%, still more preferably 0.040%, still more preferably 0.035%, still 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 the coarsening of crystal grains during heating in the gas carburizing treatment due to the pinning effect. If the N content is less than 0.0050%, the above effect cannot be sufficiently obtained even if the content of other elements is within the range of the present embodiment. On the other hand, if the N content exceeds 0.0200%, scratches are likely to occur on the surface of the manufactured slab or ingot in the steelmaking process even if the content of other elements is within the range of the present embodiment. .. Therefore, the N content is 0.0050 to 0.0200%.
  • the lower limit of the N content is preferably 0.0100%, more preferably 0.0120%, still more preferably 0.0130%.
  • the preferred upper limit of the N content is less than 0.0200%, more preferably 0.0190%, still more preferably 0.0180%, still more preferably 0.0150%.
  • Al 0.001 to 0.100%
  • Aluminum (Al) deoxidizes steel. Al further combines with N to form AlN. AlN suppresses the coarsening of crystal grains during heating in the gas carburizing treatment due to the pinning effect. If the Al content is less than 0.001%, the above effect cannot be sufficiently obtained even if the content of other elements is within the range of the present embodiment. On the other hand, if the Al content exceeds 0.100%, the formation of a coarse Al oxide is promoted even if the content of other elements is within the range of the present embodiment. The coarse Al oxide reduces the bending fatigue strength of mechanical structural parts. Therefore, the Al content is 0.001 to 0.100%.
  • the lower limit of the Al content is preferably 0.020%, more preferably 0.025%, still more preferably 0.027%, still more preferably 0.030%.
  • the preferred upper limit of the Al content is 0.090%, more preferably 0.070%, still more preferably 0.050%, still more preferably 0.045%, still more preferably 0.040. %, More preferably 0.035%.
  • Oxygen (O) is an impurity. O combines with other elements in the steel to form coarse oxide inclusions. Coarse oxide-based inclusions reduce the bending fatigue strength of mechanical structural parts. If the O content exceeds 0.0050%, the bending fatigue strength of the mechanical structural parts is significantly reduced even if the content of other elements is within the range of the present embodiment. Therefore, the O content is 0.0050% or less. It is preferable that the O content is as low as possible. However, excessive reduction of O content raises manufacturing costs. Therefore, when considering normal industrial production, the preferred lower limit of the O content is more than 0%, more preferably 0.0001%, still more preferably 0.0005%, still more preferably 0.0010. %. The preferred upper limit of the O content is 0.0040%, more preferably 0.0030%, still more preferably 0.0020%, still more preferably 0.0015%.
  • Phosphorus (P) is an impurity. P segregates at the grain boundaries and lowers the grain boundary strength. If the P content exceeds 0.030%, even if the content of other elements is within the range of the present embodiment, P is excessively segregated at the grain boundaries and the grain boundary strength is lowered. As a result, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are lowered. Therefore, the P content is 0.030% or less. It is preferable that the P content is as low as possible. However, excessive reduction of P content raises manufacturing costs. Therefore, when considering normal industrial production, the preferred lower limit of the P content is more than 0%, more preferably 0.001%, still more preferably 0.005%, still more preferably 0.010. %. The preferred upper limit of the P content is 0.025%, more preferably 0.020%, still more preferably 0.015%.
  • the balance of the chemical composition of the steel material according to this embodiment consists of Fe and impurities.
  • the impurities are mixed from ore, scrap, or the manufacturing environment as a raw material when the steel material is industrially manufactured, and are within a range that does not adversely affect the steel material of the present embodiment. Means what is acceptable.
  • the impurities referred to here are B, Pb, W, Sb, Bi, Co, Ta, Sn, In, Zr, Te, Se, Zn and the like.
  • the total content of impurities other than O and P is 0.01% or less. Of the above impurities, the B content is 0.0003% or less.
  • the chemical composition of the steel material of the present embodiment is replaced with 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
  • Rare earth element It may contain one or more elements selected from the group consisting of 0.0050% or less. These elements are arbitrary elements, and all of them enhance the bending fatigue strength and the surface fatigue strength of mechanical structural parts.
  • Mo Molybdenum
  • Mo Molybdenum
  • Mo is an optional element and may not be contained. That is, the Mo content may be 0%.
  • Mo enhances the hardenability of steel materials and enhances bending fatigue strength and surface fatigue strength of mechanical structural parts. If Mo is contained even in a small amount, the above effect 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 is reduced. Therefore, the Mo content is 0 to 0.30%, and when it is 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%, still more preferably 0.05%, still more preferably 0.10%.
  • the preferred upper limit of the Mo content is less than 0.30%, more preferably 0.25%, still more preferably 0.20%, still more preferably 0.15%.
  • Niobium (Nb) is an optional element and may not be contained. That is, the Nb content may be 0%.
  • Nb binds to C and / or N to form Nb precipitates (NbC, NbN, Nb (CN), etc.). Similar to AlN, the Nb precipitate suppresses the coarsening of crystal grains in the gas carburizing treatment due to the pinning effect. Therefore, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are increased. If even a small amount of Nb is contained, the above effect can be obtained to some extent.
  • the Nb content is 0 to 0.050%, and when it is contained, it is 0.050% or less (that is, more than 0 to 0.050%).
  • the preferred lower limit of the Nb content is 0.001%, more preferably 0.010%, still more preferably 0.015%, still more preferably 0.020%, still more preferably 0.025. %.
  • the preferred upper limit of the Nb content is less than 0.050%, more preferably 0.045%, still more preferably 0.040%, still more preferably 0.035%.
  • 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.) as well as Nb. The Ti precipitate suppresses the coarsening of crystal grains in the gas carburizing treatment due to the pinning effect. Therefore, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are increased. If even a small amount of Ti is contained, the above effect can be obtained to some extent. However, if the Ti content exceeds 0.020%, the Ti precipitate will be coarsened even if the content of other elements is within the range of this embodiment.
  • the Ti content is 0 to 0.020%, and when it is 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%, still more preferably 0.010%.
  • the preferred upper limit of the Ti content is 0.019%, more preferably 0.017%, still more preferably 0.015%.
  • Cu 0.50% or less Copper (Cu) is an optional element and may not be contained. That is, the Cu content may be 0%. When contained, Cu enhances the hardenability of steel materials and enhances bending fatigue strength and surface fatigue strength of mechanical structural parts. If even a small amount of Cu is contained, the above effect can be obtained to some extent. However, if the Cu content exceeds 0.50%, 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 is reduced. Therefore, the Cu content is 0 to 0.50%, and when it is contained, it is 0.50% or less (that is, more than 0 to 0.50%).
  • the lower limit of the Cu content is preferably 0.01%, more preferably 0.05%, still more preferably 0.10%.
  • the preferred upper limit of the Cu content is 0.45%, more preferably 0.40%, still more preferably 0.30%, still more preferably 0.25%.
  • Nickel (Ni) is an optional element and may not be contained. That is, the Ni content may be 0%. When contained, Ni enhances the hardenability of steel materials and enhances the bending fatigue strength and surface fatigue strength of mechanical structural parts. If even a small amount of Ni is contained, the above effect can be obtained to some extent. However, if the Ni content exceeds 0.80%, the steel material becomes too hard even if the content of other elements is within the range of the present embodiment. In this case, the machinability of the steel material is reduced. Therefore, the Ni content is 0 to 0.80%, and when it is contained, it is 0.80% or less (that is, more than 0 to 0.80%).
  • the lower limit of the Ni content is preferably 0.01%, more preferably 0.05%, still more preferably 0.10%.
  • the preferred upper limit of the Ni content is 0.70%, more preferably 0.60%, still more preferably 0.40%, still more preferably 0.20%.
  • V 0.30% or less Vanadium (V) is an optional element and may not be contained. That is, the V content may be 0%. When contained, V forms V precipitates (VC, VN, V (CN), etc.), similar to Nb. The V precipitate suppresses the coarsening of crystal grains in the gas carburizing treatment due to the pinning effect. Therefore, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are increased. If V is contained even in a small amount, the above effect can be obtained to some extent. However, if the V content exceeds 0.30%, the steel material becomes too hard even if the content of other elements is within the range of the present embodiment. In this case, the machinability of the steel material is reduced.
  • the V content is 0 to 0.30%, and when it is 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%, still more preferably 0.04%.
  • the preferred upper limit of the V content is 0.20%, more preferably 0.15%, still more preferably 0.10%.
  • Mg 0.0035% or less
  • Magnesium (Mg) is an optional element and may not be contained. That is, the Mg content may be 0%. When contained, Mg deoxidizes steel, similar to Al. In this case, the formation of coarse oxides is suppressed. Therefore, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are increased. If even a small amount of Mg is contained, the above effect can be obtained to some extent. However, if the Mg content exceeds 0.0035%, the formation of coarse Mg oxides in the steel material is promoted even if the content of other elements is within the range of the present embodiment. In this case, the limit machining rate during hot machining decreases.
  • the Mg content is 0 to 0.0035%, and when it is 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%, still more preferably 0.0005%.
  • the preferred upper limit of the Mg content is 0.0030%, more preferably 0.0028%, still more preferably 0.0025%, still more preferably 0.0020%.
  • Ca 0.0030% or less Calcium (Ca) is an optional element and may not be contained. That is, the Ca content may be 0%.
  • Ca refines sulfides in steel. Ca further promotes spheroidization of sulfides in steel. Therefore, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are increased. If even a small amount of Ca is contained, the above effect can be obtained to some extent. However, if the Ca content exceeds 0.0030%, coarse Ca oxides are formed in the steel material even if the content of other elements is within the range of this embodiment. In this case, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are reduced.
  • the Ca content is 0 to 0.0030%, and when it is contained, it is 0.0030% or less (that is, more than 0 to 0.0030%).
  • the preferred lower limit of the Ca content is 0.0001%, more preferably 0.0002%, still more preferably 0.0005%, still more preferably 0.0007%, still more preferably 0.0010. %.
  • the preferred upper limit of the Ca content is 0.0025%, more preferably 0.0022%, still more preferably 0.0020%.
  • Rare earth element (REM) 0.0050% or less
  • Rare earth element (REM) is an optional element and may not be contained. That is, the REM content may be 0%. When contained, the REM dissolves in the sulfide in the steel material and suppresses the stretching of MnS. As a result, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are increased. If even a small amount of REM is contained, the above effect can be obtained to some extent. However, if the REM content exceeds 0.0050%, coarse oxides will be produced even if the content of other elements is within the range of this embodiment. In this case, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are reduced.
  • the REM content is 0 to 0.0050%, and when contained, it is 0.0050% or less (that is, more than 0 to 0.0050%).
  • the preferred lower limit of the REM content is 0.0001%, more preferably 0.0010%, still more preferably 0.0020%.
  • the preferred upper limit of the REM content is 0.0045%, more preferably 0.0040%, still more preferably 0.0035%, still more preferably 0.0030%.
  • the REMs are scandium (Sc) having an atomic number of 21, yttrium (Y) having an atomic number of 39, and lanthanum (La) having an atomic number of 57 to lutetium having an atomic number of 71 (Lutetium). It is one or more elements selected from the group consisting of Lu).
  • the REM content in the present specification is the total content of these elements.
  • the microstructure of the steel material of the present embodiment contains ferrite, the balance is pearlite and / or bainite, and the surface integral of ferrite is 50 to 70%.
  • the surface integral of ferrite is less than 50%, the surface integral of pearlite and / or bainite is too high in the steel material. In this case, the hardness of the steel material is excessively increased. As a result, the machinability of the steel material is reduced. On the other hand, if the surface integral of the ferrite exceeds 70%, the crystal grain size tends to vary during the gas carburizing treatment. Therefore, heat treatment deformation occurs excessively during the gas carburizing treatment.
  • the surface integral of ferrite is 50 to 70% and the balance other than ferrite in the microstructure is pearlite and / or bainite, the machinability of the steel material is sufficiently enhanced. Further, heat treatment deformation during gas carburizing treatment can be suppressed.
  • the microstructure at each cross-sectional observation position and each vertical cross-sectional observation position contains 50 to 70% ferrite in area fraction, and the balance is composed of pearlite and / or bainite.
  • the preferable lower limit of the surface integral of ferrite at each observation position is 52%, more preferably 55%, still more preferably 57%.
  • the preferable upper limit of the surface integral of ferrite at each observation position is 68%, more preferably 65%, still more preferably 63%.
  • FIG. 2 is a schematic cross-sectional view of the steel material of the present embodiment, which is a cross section perpendicular to the longitudinal direction.
  • the cross-sectional CS of the steel material has a circular shape with a radius R.
  • the center position C1 of the cross-section CS and the position of R / 2 in the radial direction from the center position C1 of the cross-section CS are arranged around the center of the cross-section CS at a pitch of 45 °.
  • the R / 2 positions C2 to C9 at the locations are defined as the "cross-sectional observation positions" C1 to C9 at the nine locations.
  • 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.
  • 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.
  • the standard deviation of the ferrite area fraction is 4.0% or less, the variation in the phase fraction of the microstructure at each cross-sectional observation position C1 to C9 is sufficiently suppressed. Therefore, it is possible to suppress variations in the occurrence timing of martensitic transformation at each cross-sectional observation positions C1 to C9 during the gas carburizing treatment.
  • the standard deviation of the area fraction of ferrite at the cross-sectional observation positions C1 to C9 exceeds 4.0%, the phase fraction varies greatly at each of the cross-sectional observation positions C1 to C9. In this case, the heat treatment deformation during the gas carburizing treatment cannot be sufficiently suppressed. Therefore, the standard deviation of the surface integral of ferrite at the cross-sectional observation positions C1 to C9 is 4.0% or less.
  • the preferred upper limit of the standard deviation of the surface integral of ferrite is 3.8%, more preferably 3.5%, still more preferably 3.0%.
  • the lower limit of the standard deviation of the surface integral of ferrite is not particularly limited.
  • the lower limit of the standard deviation of the surface integral of ferrite is not particularly limited.
  • the preferred lower limit of the standard deviation of the surface integral of ferrite is 0.1%, more preferably 0.5%, still more preferably 1.0%, still more preferably 1.5%.
  • ferrite average grain size ratio (maximum value of ferrite average particle size in C1 to C9) / (minimum value of ferrite average particle size in C1 to C9)
  • the ferrite average particle size ratio at the cross-sectional observation positions C1 to C9 is 2.00 or less.
  • the variation in the average particle size of the ferrite at each of the cross-sectional observation positions C1 to C9 is sufficiently suppressed. That is, the ferrite grains at each position are aligned. Therefore, it is possible to sufficiently suppress the variation in the occurrence of martensitic transformation during the carburizing treatment. Therefore, it is possible to suppress heat treatment deformation of the steel material during the carburizing treatment.
  • the ferrite average particle size ratio exceeds 2.00, the ferrite grains at the respective cross-sectional observation positions C1 to C9 are scattered. In this case, the heat treatment deformation of the steel material during the gas carburizing treatment cannot be sufficiently suppressed. Therefore, the ferrite average particle size ratio is 2.00 or less.
  • the preferred upper limit of the ferrite average particle size ratio is 1.95, more preferably 1.90, and even more preferably 1.80.
  • the lower limit of the ferrite average particle size ratio is not particularly limited.
  • the preferred lower limit of the ferrite average particle size ratio is 1.10, more preferably 1.20, still more preferably 1.30, and even more preferably 1.40.
  • the variation in microstructure is sufficiently suppressed not only in the above-mentioned cross section but also in the vertical cross section which is parallel to the longitudinal direction of the steel material and includes the central axis of the steel material. ..
  • the variation in the microstructure not only in the cross section but also in the vertical section is sufficiently suppressed, so that the heat treatment deformation generated three-dimensionally can be sufficiently suppressed.
  • the suppression of the variation in the microstructure in the vertical cross section will be described.
  • FIG. 3 is a schematic view of a vertical cross section that is parallel to the longitudinal direction of the steel material of the present embodiment and is a cross section including the central axis.
  • the six R / 2 positions L4 to L9 arranged at the / 2 position are defined as the nine “longitudinal section observation positions” L1 to L9.
  • the microstructures at the above-mentioned nine vertical cross-sectional observation positions L1 to L9 satisfy the following (C) and (D).
  • C The arithmetic mean value of the area fraction of ferrite at the vertical cross-sectional 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 particle diameters of ferrites at the vertical cross-sectional observation positions L1 to L9, the ratio of the maximum average particle size to the minimum average particle size (ferrite average particle size ratio) is 2.00 or less.
  • (C) and (D) will be described in detail.
  • the arithmetic mean value of the area fraction of ferrite at the vertical cross-sectional observation positions L1 to L9 is 50 to 70%, and the standard deviation of the area fraction of ferrite. Is 4.0% or less.
  • the standard deviation of the area fraction of ferrite at the vertical section observation positions L1 to L9 exceeds 4.0%, the phase fraction varies greatly at each vertical section observation positions L1 to L9. In this case, the heat treatment deformation during the gas carburizing treatment cannot be sufficiently suppressed. Therefore, the standard deviation of the surface integral of ferrite at the vertical cross-sectional observation positions L1 to L9 is 4.0% or less.
  • the preferred upper limit of the standard deviation of the surface integral of ferrite is 3.8%, more preferably 3.5%, still more preferably 3.0%.
  • the lower limit of the standard deviation of the surface integral of ferrite is not particularly limited.
  • the preferred lower limit of the standard deviation of the surface integral of ferrite is 0.1%, more preferably 0.5%, still more preferably 1.0%, still more preferably 1.5%.
  • ferrite average grain size ratio (maximum value of ferrite average particle size in L1 to L9) / (minimum value of ferrite average particle size in L1 to L9)
  • the ferrite average particle size ratio at the vertical cross-sectional observation positions L1 to L9 is 2.00 or less.
  • the variation in the average particle size of the ferrite at each of the vertical cross-sectional observation positions L1 to L9 is sufficiently suppressed. That is, the ferrite grains at each position are aligned. Therefore, it is possible to sufficiently suppress the variation in the occurrence of martensitic transformation during the carburizing treatment. Therefore, it is possible to suppress heat treatment deformation of the steel material during the carburizing treatment.
  • the ferrite average particle size ratio exceeds 2.00, the ferrite grains at each vertical cross-sectional observation position L1 to L9 are scattered. In this case, the heat treatment deformation of the steel material during the gas carburizing treatment cannot be sufficiently suppressed. Therefore, the ferrite average particle size ratio at the nine vertical cross-sectional observation positions L1 to L9 is 2.00 or less.
  • the preferred upper limit of the ferrite average particle size ratio is 1.95, more preferably 1.90, and even more preferably 1.80.
  • the lower limit of the ferrite average particle size ratio is not particularly limited.
  • the preferred lower limit of the ferrite average particle size ratio is 1.10, more preferably 1.20, still more preferably 1.30, and even more preferably 1.40.
  • Method of observing microstructure at each observation position Method of measuring surface integral of ferrite and average grain size ratio of ferrite
  • the method for observing the microstructure at the cross-sectional observation positions C1 to C9 and the vertical cross-sectional observation positions L1 to L9 of the steel material of the present embodiment, and the method for measuring the area fraction of ferrite and the average grain size ratio of ferrite are as follows. be.
  • the method of observing the microstructure of the cross-sectional CS is as follows. A sample including each cross-sectional observation position C1 to C9 is collected from the steel material. Of the surfaces of the sample, the surface corresponding to the cross section CS is used as the observation surface. On the observation surface, the observation field of view including the cross-sectional observation position is 0.5 mm ⁇ 1.0 mm.
  • the contrast of each phase such as ferrite, pearlite, and bainite is different for each phase.
  • ferrite is observed to be white, and bainite and pearlite are observed to be blacker than ferrite. Therefore, ferrite can be easily distinguished from other phases (pearlite and bainite). Identify ferrite based on contrast.
  • the arithmetic mean value of the ferrite area fraction (%) at the nine observation fields (cross-section observation positions) is the arithmetic mean value (%) of the ferrite area fraction at the nine cross-section observation positions C1 to C9. Define.
  • the standard deviation (%) of the ferrite area fractions at the nine cross-sectional observation positions C1 to C9 is calculated from the ferrite area fractions (%) at the nine observation fields (cross-section observation positions).
  • the standard deviation here is the sample standard deviation.
  • the average particle size of the ferrites at the cross-sectional observation positions C1 to C9 at 9 locations are obtained. Then, among the average particle diameters of these ferrites, the maximum average particle diameter ( ⁇ m) and the minimum average particle diameter ( ⁇ m) of the ferrites are specified. The ratio of the maximum average particle size to the specified minimum average particle size (ferrite average particle size ratio) is obtained.
  • the method of observing the microstructure of the vertical cross section LS is as follows. A sample including each vertical cross-sectional observation position L1 to L9 is taken from the steel material. Of the surface of the sample, the surface corresponding to the vertical cross section LS is used as the observation surface. On the observation surface, the observation field of view including the vertical cross-sectional observation position is 0.5 mm ⁇ 1.0 mm. More specifically, the length of 0.5 mm of the observation field of view is defined as the radial direction of the steel material, and 1.0 mm is defined as the longitudinal direction of the steel material.
  • the observation field of view (0.5 mm ⁇ 1.0 mm) of the etched observation surface is observed with a 100x optical microscope.
  • Each phase in the observation field is identified by the same method as the microstructure observation of the cross-sectional CS.
  • the arithmetic mean value of the ferrite area fraction (%) in the nine observation fields (vertical cross-section observation positions) is the arithmetic mean value (%) of the ferrite area fraction in the nine vertical cross-section observation positions L1 to L9. Define.
  • the standard deviation (%) of the ferrite area fractions at the nine vertical cross-sectional observation positions L1 to L9 is calculated from the ferrite area fractions (%) at the nine observation fields (vertical cross-sectional observation positions).
  • the chemical composition of the steel material of the present embodiment further satisfies the following formula (1) on the premise that the content of each element in the chemical composition is within the above range.
  • 1- 0.5C + 0.03Si + 0.06Mn + 0.01Cr + 0.05Mo
  • the content (mass%) of the corresponding element is substituted for each element symbol in the formula (1). If the corresponding element is not contained, "0" is substituted for the element symbol.
  • the steel material of the present embodiment not only the cross-sectional CS but also the microstructure of the vertical cross-sectional LS is made uniform.
  • the microstructures of the cross-sectional observation positions C1 to C9 in the cross-section CS satisfy (A) and (B)
  • the microstructures of the vertical cross-section observation positions L1 to L9 in the vertical cross-section LS satisfy (C) and.
  • (D) even if the microstructure is made uniform, as described above, a minute time zone in which the martensitic transformed portion and the martensitic untransformed portion coexist always occurs at the time of quenching of the gas carburizing treatment. If the amount of heat treatment strain in the martensite untransformed portion is large in this minute time zone, heat treatment deformation will occur. Therefore, the steel material of the present embodiment further satisfies the formula (1).
  • F1 1- (0.5C + 0.03Si + 0.06Mn + 0.01Cr + 0.05Mo).
  • F1 is an index relating to the amount of heat treatment deformation of the steel material in the gas carburizing treatment with respect to the steel material.
  • C, Si, Mn, Cr and Mo contained in F1 are particularly martensite in a minute time zone in which a martensitic transformed portion and a martensitic untransformed portion are mixed at the time of quenching. Increases the strength of untransformed parts.
  • the maximum deformation amount ratio decreases, and the heat treatment deformation amount decreases.
  • the preferred upper limit of F1 is 0.799, more preferably 0.797, and even 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 the present embodiment, the preferable lower limit of F1 is 0.765, more preferably 0.770, and even more preferably 0.775.
  • the numerical value of F1 is a value obtained by rounding off to the fourth decimal place.
  • the content of each element in the chemical composition is within the range of the present embodiment, F1 satisfies the formula (1), the cross-sectional observation positions C1 to C9 and the longitudinal section.
  • the microstructure at the surface observation positions L1 to L9 is within the scope of this embodiment. Therefore, the machinability after hot working on the steel material of the present embodiment is excellent. Further, when the steel material of the present embodiment is subjected to gas carburizing treatment, the mechanical structural parts have excellent bending fatigue strength and surface fatigue strength, and can sufficiently suppress heat treatment deformation.
  • the steel material of the present embodiment is a so-called as-rolled material (azurol material). Therefore, in the steel material of the present embodiment, a so-called band structure is observed in the above observation fields of the vertical cross-sectional observation positions L1 to L9.
  • the band structure is a well-known microstructure, and as shown in FIG. 4, a ferrite (ferrite band) F extending in the longitudinal direction of the steel material and a non-ferrite (non-ferrite band) NF extending in the longitudinal direction of the steel material are used. However, it means a structure that is alternately laminated in the radial direction. Non-ferrites are pearlite and / or bainite.
  • the steel material of the present embodiment is suitable as a material for mechanical structural parts.
  • the steel material of the present embodiment is particularly suitable for applications such as gears or shafts of automobile applications, construction machinery, industrial machinery and the like.
  • An example of the method for producing a steel material of the present embodiment includes the following steps.
  • Process of preparing materials (Material preparation process)
  • Process 2 A process of hot-working a material to manufacture a steel material (hot-working process)
  • each step will be described.
  • the steel material of the present embodiment is prepared. Specifically, a molten steel in which the content of each element in the chemical composition is within the range of the present embodiment and F1 satisfies the formula (1) is produced.
  • the refining method is not particularly limited, and a well-known method may be used. For example, refining in a converter (primary refining) is performed on hot metal produced by a well-known method. Well-known secondary refining will be carried out on the molten steel discharged from the converter.
  • the content of the alloying elements in the molten steel is adjusted to produce a molten steel having a chemical composition in which the content of each element is within the range of the present embodiment and F1 satisfies the formula (1). ..
  • the material is manufactured by a well-known casting method.
  • an ingot may be manufactured by an ingot method using molten steel.
  • bloom or billet may be produced by a continuous casting method using molten steel.
  • the material (ingot, bloom or billet) is manufactured by the above method.
  • reduction may be applied to the slab in the middle of solidification.
  • Step 2 Hot working process the material (ingot, bloom or billet) prepared in the material preparing step is hot-worked to produce the steel material of the present embodiment.
  • the shape of the steel material is not particularly limited, but is, for example, steel bar or wire rod. In the following description, a case where the steel material is steel bar will be described as an example. However, even if the steel material has a shape other than that of steel bar, it can be manufactured by the same hot working process.
  • the hot working process includes the following steps.
  • Step 21 Ingot rolling step Heating temperature: 1250 to 1300 ° C Holding time: 10 hours or more
  • Process 22 Finish rolling process Heating temperature: 1150 to 1200 ° C Holding time: 1.5 to 3.0 hours Finishing temperature: 950 to 1000 ° C
  • Step 23 Temperature holding step Average cooling rate at 900 to 800 ° C .: 0.05 ° C / sec or less
  • Step 24 Cooling step Average cooling rate at 800 to 300 ° C: 0.10 to 1.00 ° C / sec
  • each step will be described.
  • the material is hot-rolled to produce billets.
  • the material is hot-rolled (bulk-rolled) by a lump-rolling machine to manufacture billets.
  • a continuous rolling mill is located downstream of the lump rolling mill, hot rolling is further performed on the billet after lump rolling using the continuous rolling mill to produce a smaller billet.
  • horizontal stands having a pair of horizontal rolls and vertical stands having a pair of vertical rolls are alternately arranged in a row.
  • the slab rolling process the material is produced in billets using a slab rolling mill or using a shunt rolling mill and a continuous rolling mill.
  • the conditions in the lump rolling process are as follows. Heating temperature: 1250 to 1300 ° C Holding time: 10 hours or more The heating temperature in the heating furnace in the lump rolling process is 1250 to 1300 ° C. The holding time at the heating temperature (1250-1300 ° C.) is 10 hours or more. If the heating temperature in the heating furnace in the lump rolling process is 1250-1300 ° C. and the holding time at the heating temperature (1250-1300 ° C.) is 10 hours or more, other production conditions must be satisfied. As a premise, the solidification segregation in the material generated during the material preparation process can be sufficiently alleviated.
  • the standard deviation of the surface integral of the ferrite at each of the cross-sectional observation positions C1 to C9 and each of the vertical 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, considering the manufacturing cost, the preferable upper limit of the holding time at the heating temperature is 30 hours.
  • the billet manufactured by the lump-rolling process is allowed to cool (air-cooled) to room temperature before the finish rolling process.
  • the surface reduction rate in the ingot rolling process is 30% or more.
  • the reduction rate (%) is defined by the following equation.
  • Surface reduction rate (%) (1-Area of cross section (cross section perpendicular to longitudinal direction) of steel material after lump rolling / Area of cross section (cross section perpendicular to longitudinal direction) of material before lump rolling) ⁇ 100
  • the surface reduction rate in the ingot rolling process is 30% or more, the area of ferrite at each cross-section observation position C1 to C9 and each longitudinal cross-section observation position L1 to L9, assuming that other manufacturing conditions are satisfied.
  • the standard deviation of the fraction is 4.0% or less.
  • the conditions in the finish rolling process are as follows. Heating temperature: 1150-1200 ° C Holding time: 1.5 to 3.0 hours Finishing temperature: 950 to 1000 ° C
  • the heating temperature in the heating furnace in the finish rolling step 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 (1150-1200 ° C.) is 1.5 to 3.0 hours, other manufacturing conditions are satisfied. Assuming that, the temperature variation in the steel material (steel bar) can be sufficiently suppressed. Therefore, the ferrite average particle size ratio at the cross-sectional observation positions C1 to C9 and the vertical cross-sectional observation positions L1 to L9 is 2.00 or less.
  • finish rolling In the finish rolling process, hot rolling (finish rolling) is carried out by a continuous rolling machine 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 on the outlet side of the stand where the steel material is finally rolled is defined as the finishing temperature (° C.).
  • the steel material temperature means the surface temperature of the steel material.
  • the finishing temperature is 950 to 1000 ° C.
  • the finishing temperature is 950 to 1000 ° C.
  • the variation in the austenite particle size in the steel material (steel bar) is sufficiently suppressed on the premise that other production conditions are satisfied. Therefore, when the austenite is transformed into ferrite in the temperature holding step and the cooling step described later, the variation in the average particle size of ferrite is sufficiently suppressed. Therefore, the ferrite average particle size ratio at the cross-sectional observation positions C1 to C9 and the vertical cross-sectional observation positions L1 to L9 is 2.00 or less.
  • Step 23 Temperature holding step
  • the temperature of the steel material is held after the finish rolling step and before the cooling step.
  • the conditions in the temperature holding process are as follows. Average cooling rate when the steel material temperature is 900 to 800 ° C: 0.05 ° C / sec or less
  • the average cooling rate when the steel material temperature is 900 to 800 ° C is suppressed to 0.05 ° C / sec or less.
  • the average cooling rate of the steel material having a steel material temperature of 900 to 800 ° C. is 0.05 ° C./sec using a slow cooling cover, a heat retaining cover, or a temperature holding furnace. Keep it below.
  • the average cooling rate at a steel material temperature of 900 to 800 ° C. is 0.05 ° C./sec or less, temperature variation in the axial direction (longitudinal direction) of the steel material can be suppressed on the premise that other manufacturing conditions are satisfied. Therefore, it is possible to suppress variations in the ferrite transformation timing in the axial direction of the steel material. Therefore, in particular, it is possible to suppress the growth variation of the ferrite grains in the axial direction (longitudinal section) of the steel material. Specifically, the following mechanism works.
  • austenite gradually transforms into ferrite as the steel material temperature decreases. If the temperature of the steel material varies in the axial direction in the range of 900 to 800 ° C., ferrite produced at a relatively early stage after the finish rolling process and ferrite produced at a relatively late stage coexist. It ends up. In this case, the ferrite grains produced at an early stage tend to be coarser than the ferrite grains transformed at a later stage. As a result, in particular, the variation of ferrite grains becomes large in the axial direction (longitudinal section) of the steel material.
  • the average cooling rate at a steel material temperature of 900 to 800 ° C. is high, the temperature variation in the axial direction (longitudinal section) of the steel material becomes large. Therefore, the ferrite average particle size ratio at the vertical cross-sectional observation positions L1 to L9 becomes large.
  • the average cooling rate when the steel material temperature is 900 to 800 ° C. is suppressed to 0.05 ° C./sec or less.
  • temperature variation in the axial direction (longitudinal cross section) of the steel material can be suppressed. Therefore, the deviation of the ferrite formation (transformation) timing in the vertical cross section of the steel material is suppressed.
  • the ferrite average particle size ratio at the vertical cross-sectional observation positions L1 to L9 can be set to 2.00 or less, provided that other manufacturing conditions are satisfied.
  • Step 24 Cooling step
  • the conditions in the cooling process are as follows. Average cooling rate at a steel temperature of 800 to 300 ° C: 0.10 to 1.00 ° C / sec An average cooling rate of 0.10 to 1.00 ° C / sec for a steel with a steel temperature of 800 to 300 ° C. Cool with. Assuming that the average cooling rate at a steel material temperature of 800 to 300 ° C. is 0.10 to 1.00 ° C./sec, the cross-sectional observation positions C1 to C9 and the vertical cross-sectional observation positions are assumed to satisfy other manufacturing conditions.
  • the arithmetic mean value of the area fraction of the ferrite in L1 to L9 is 50 to 70%.
  • the steel material of the present embodiment having the above-mentioned configuration can be manufactured.
  • the steel material of the present embodiment is a rolled material.
  • the steel material of this embodiment is suitable as a material for mechanical structural parts manufactured by performing gas carburizing treatment.
  • the steel material of the present embodiment may be manufactured as a mechanical structural part by performing a surface hardening heat treatment other than the gas carburizing treatment.
  • Other surface hardening heat treatments include, for example, quenching and tempering, induction hardening and tempering, and soaking treatment (quenching quenching and tempering).
  • Mechanical structural parts are used, for example, in automobiles, construction vehicles, and the like. Mechanical structural parts are, for example, gears and shafts used in steering mechanisms.
  • the mechanical structural parts made of the steel material of this embodiment are manufactured by a well-known manufacturing method.
  • mechanical structural parts are manufactured by the following method.
  • An example of a method for manufacturing mechanical structural parts includes the following steps. -Hot working process-Cutting process-Heat treatment process Each process will be described below.
  • Hot working process hot working is performed on the steel material of the present embodiment.
  • Hot working is, for example, well-known hot forging.
  • the heating temperature in the hot working step is, for example, 1000 to 1300 ° C.
  • the steel material after hot working is allowed to cool (air cooling). If necessary, the steel material after allowing to cool may be annealed.
  • a cutting process is performed on the steel material after the hot working process to manufacture an intermediate product having a predetermined shape. During this cutting process, high machinability of steel materials is required. In the cutting process, well-known cutting is performed. By cutting, it is possible to manufacture precision-shaped machine structural parts, which is difficult only with the hot working process.
  • Heat treatment is performed on the intermediate product after cutting.
  • the "heat treatment” includes a well-known gas carburizing treatment and a well-known tempering step.
  • the gas carburizing treatment also includes the gas carburizing nitriding treatment.
  • the gas carburizing process includes a gas carburizing step and a quenching step.
  • gas carburizing treatment it is a well-known technical matter to those skilled in the art that the surface hardness, core hardness, and surface carbon concentration of mechanical structural parts can be appropriately adjusted by appropriately adjusting well-known conditions.
  • a well-known gas carburizing treatment will be described as an example of the heat treatment step. It is well known to those skilled in the art that the well-known gas carburizing nitriding treatment is also carried out in the same process as the gas carburizing treatment.
  • the gas carburizing treatment includes a gas carburizing step and a quenching step.
  • gas carburizing process and the quenching process will be described.
  • 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 of FIG. 5 is the treatment temperature (° C.) during the gas carburizing treatment, and the horizontal axis is the time (minutes).
  • the gas carburizing step S10 includes a heating step S0, a carburizing step S1 and a diffusion step S2.
  • the intermediate product charged in the furnace is heated to the carburizing temperature Tc.
  • the carburizing temperature Tc in the heating step S0 is, for example, 830 to 1100 ° C.
  • the intermediate product is held for a predetermined time (holding time t1) at a predetermined atmosphere of carbon potential Cp1 and a carburizing temperature Tc.
  • 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.
  • the carburized temperature Tc is held for a predetermined time (holding time t2) in the atmosphere of the predetermined carbon potential Cp2.
  • the carbon potential Cp2 in the diffusion step S2 is, for example, 0.5 to 1.2%
  • the holding time t2 at the carburizing temperature Tc is, for example, 30 minutes or more. It is preferable that the carbon potential Cp2 in the diffusion step S2 is lower than the carbon potential Cp1 in the carburizing step S1.
  • the quenching step S20 is carried out on the intermediate product after the gas carburizing step S10.
  • the intermediate product after the gas carburizing step S10 is held at a quenching temperature Ts of Ar 3 points or more, and then the intermediate product is rapidly cooled and quenched.
  • 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 treatment is oil cooling or water cooling. Specifically, an intermediate product maintained at a quenching temperature is immersed in a cooling bath containing oil or water as a cooling medium and rapidly cooled.
  • the temperature of the oil or water as the cooling medium is, for example, room temperature to 200 ° C. Further, if necessary, sub-zero processing may be carried out.
  • tempering process A well-known tempering process is carried out for intermediate products 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.
  • the intermediate product after the tempering step may be further subjected to a grinding process or a shot peening process.
  • grinding is performed, cutting is performed to give the steel material a shape. By cutting, a more precise shape can be given to the steel material.
  • the shot peening treatment is carried out, the compressive residual stress is introduced into the surface layer portion of the intermediate product after the gas carburizing treatment. Compressive residual stress suppresses the generation and growth of fatigue cracks. Therefore, the bending fatigue strength and the surface fatigue strength of the mechanical structural parts are increased.
  • the shot peening process may be carried out by a well-known method. For example, it is desirable that the shot peening treatment is performed using shot grains having a diameter of 0.7 mm or less and having an arc height of 0.4 mm or more.
  • a steel material having the chemical composition shown in Table 1 was prepared.
  • the steel type number A corresponds to SCr420H specified in JIS G4052 (2016).
  • a steel material having a chemical composition corresponding to SCM420H specified in JIS G4052 (2016) was used as the reference steel material.
  • the steel grade number A in Table 1 means that the measured Nb content was 0% when rounded to the fourth decimal place.
  • rounding means that if the digit (fraction) below the specified minimum digit is less than 5, it is rounded down, and if it is 5 or more, it is rounded up.
  • the temperature described in the “heating temperature (° C.)” column of the “bulk rolling process” and the “finish rolling process” column is the heating temperature (° C.).
  • the time described in the “holding time (time)” column of the “lump rolling process” and the “finish rolling process” column is the holding time (hour) at the heating temperature.
  • the temperature in the “Finishing temperature (° C)” column in the “Finish rolling process” column is the steel material temperature (surface temperature of the steel material) (° C) on the outlet side of the last rolled stand in the continuous rolling mill in the finish rolling process. 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 step” column is the average cooling rate (° C./sec) when the steel material temperature is 800 to 300 ° C.
  • the produced bloom was heated at the heating temperature and holding time shown in Table 2. Then, bloom was lump-rolled using a lump-rolling machine to produce billets.
  • the manufactured billet was water-cooled to room temperature (25 ° C.).
  • the cross section perpendicular to the longitudinal direction of the billet was a rectangle of 162 mm ⁇ 162 mm.
  • the heating temperature and holding time in the lump rolling process are as shown in Table 2.
  • the surface reduction rate in the bulk rolling process was 30% or more under all manufacturing conditions.
  • the billet after the ingot rolling process was subjected to a finishing rolling process under the conditions shown in Table 2 to produce a steel material (steel bar) having a diameter of 50 mm.
  • 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 carried out on the billets after heating to produce steel bars. At this time, the finishing temperature (° C.) was as shown in Table 2.
  • a temperature holding process was carried out on the steel material (steel bar) after the finish rolling process.
  • the production 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 the steel material having a steel material temperature of 900 to 800 ° C.
  • the steel material having a steel material temperature of 900 to 800 ° C. was allowed to cool without using a slow cooling cover. Therefore, the average cooling rate at a steel material temperature of 900 to 800 ° C. was over 0.05 ° C./sec.
  • the cooling process was carried out. Specifically, under each manufacturing condition, the average cooling rate (° C./sec) when the steel material temperature was 800 to 300 ° C. was as shown in the cooling process column of Table 2.
  • test number 31 is an example using SCM420H which is a reference steel, and the manufacturing condition a which is one of the manufacturing methods generally used for the steel material which has a chemical composition of SCM420H was used.
  • the observation surface of the sample was etched with 3% alcohol nitrate (Nital corrosive liquid).
  • the observation field of view (0.5 mm ⁇ 1.0 mm) of the etched observation surface was observed with a 100x optical microscope. In the observation field, the phase was identified by contrast.
  • the arithmetic mean value of the ferrite area fraction (%) at the nine observation fields (cross-section observation positions) is the arithmetic mean value (%) of the ferrite area fraction at the nine cross-section observation positions C1 to C9. Defined.
  • the arithmetic mean value of the obtained ferrite surface integral is shown in the "ferrite surface integral (%)" column of the "cross section” column of Table 3.
  • the average particle size of the ferrites at the cross-sectional observation positions C1 to C9 at 9 locations was determined. Then, among the average particle diameters of these ferrites, the maximum average particle diameter ( ⁇ m) and the minimum average particle diameter ( ⁇ m) of ferrite were specified. The ratio of the maximum average particle size to the specified minimum average particle size (ferrite average particle 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.
  • the observation surface of the sample was etched with 3% alcohol nitrate (Nital corrosive liquid).
  • the observation field of view (0.5 mm ⁇ 1.0 mm) of the etched observation surface was observed with a 100x optical microscope. In the observation field, the phase was identified by contrast.
  • the observed phase is shown in the "Phase” column of the "Vertical section” column of Table 3.
  • the microstructure at all the vertical section observation positions contains ferrite and the balance consists of pearlite and / or bainite, " ⁇ " is indicated.
  • the microstructure of the longitudinal section contained ferrite and the balance was pearlite and / or bainite.
  • the arithmetic mean value of the ferrite area fraction (%) in the nine observation fields (vertical cross-section observation positions) is the arithmetic mean value (%) of the ferrite area fraction in the nine vertical cross-section observation positions L1 to L9. Defined.
  • the arithmetic mean value of the obtained ferrite surface integral is shown in the "ferrite surface integral (%)" column of the "longitudinal section” column of Table 3.
  • the average particle size of ferrites at 9 vertical cross-sectional observation positions L1 to L9 was determined. Then, among the average particle diameters of these ferrites, the maximum average particle diameter ( ⁇ m) and the minimum average particle diameter ( ⁇ m) of ferrite were specified. The ratio of the maximum average particle size to the specified minimum average particle size (ferrite average particle size ratio) was determined. The obtained ferrite average particle size ratio is shown in the "ferrite particle size ratio" column of the "longitudinal section" column of Table 3.
  • the machinability evaluation test was carried out by the following method. A heat treatment simulating hot forging and a constant temperature annealing treatment were carried out on a steel bar having a diameter of 50 mm. Specifically, the steel bar was heated at 1200 ° C. and held at 1200 ° C. for 30 minutes. Then, the steel bar was allowed to cool to room temperature. Further, it was heated at 950 ° C. and kept at 950 ° C. for 1 hour. Further, after holding at 650 ° C. for 2 hours, the mixture was allowed to cool to room temperature. Machining (cutting) was carried out on the steel bar after cooling to prepare a test piece for machinability evaluation having a diameter of 45 mm and a length of 400 mm.
  • the outer circumference of the test piece of each test number was turned and the tool life was evaluated. Specifically, the test piece of each test number was subjected to outer peripheral lathe processing under the following conditions.
  • the cutting tool used was an uncoated cemented carbide equivalent 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.
  • the outer circumference was turned for 20 minutes under the above-mentioned cutting conditions. Then, the flank wear amount (mm) of the cutting tool was measured.
  • the obtained flank wear amount (mm) is shown in the "wear amount (mm)" column of Table 3.
  • the flank wear amount (mm) was less than 0.25 mm, it was judged that the machinability of the steel material was high.
  • the obtained flank wear amount (mm) was 0.25 mm or more, it was judged that the machinability of the steel material was low.
  • the steel material (steel bar with a diameter of 50 mm) of each test number was heated under the conditions of a heating temperature of 1200 ° C. and a holding time of 30 minutes. Then, hot working (hot forging) was performed at a finishing temperature of 950 ° C. or higher to produce a steel bar having a diameter of 35 mm.
  • a steel bar having a diameter of 35 mm was machined (cut) to process an intermediate product of the Ono type rotary bending test piece. The diameter of the cross section of the intermediate product at the notched bottom was 8 mm.
  • the intermediate product was carburized (gas carburized and tempered) to prepare the Ono-type rotary bending test piece shown in FIG.
  • the conditions of the carburizing treatment carried out are as follows.
  • the test piece was heated at 950 ° C. for 240 minutes in an atmosphere having a carbon potential of Cp1 of 0.8%. Subsequently, the mixture was heated at 950 ° C. for 60 minutes in an atmosphere having a carbon potential of Cp2 of 0.8%. Then, it was heated at 850 ° C. for 30 minutes and oil-cooled with oil at 130 ° C. The test piece after oil cooling 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.
  • the C concentration on the surface of the steel material (round bar) was adjusted to 0.80% by mass.
  • An Ono-type rotary bending fatigue test was performed using the Ono-type rotary bending test piece after carburizing. Multiple test pieces were prepared for each test number. A fatigue test was carried out by changing the stress applied to each test piece, and after repeating 10 million times ( 107 times), the highest stress that did not break was taken as the bending fatigue strength (MPa). In the Ono-type rotary bending fatigue test, the rotational speed was 3000 rpm and the stress ratio was double swing.
  • the obtained bending fatigue strength ratio (%) is shown in the "Bending fatigue strength ratio (%)" column of Table 3.
  • the bending fatigue strength ratio was 110% or more, it was judged that sufficient bending fatigue strength could be obtained.
  • the bending fatigue strength ratio is less than 110%, it is determined that the bending fatigue strength is low.
  • the steel material (steel bar with a diameter of 50 mm) of each test number was heated under the conditions of a heating temperature of 1200 ° C. and a holding time of 30 minutes. Then, hot working (hot forging) was performed at a finishing temperature of 950 ° C. or higher to produce a steel bar having a diameter of 35 mm.
  • a steel bar having a diameter of 35 mm was machined (cut) to process an intermediate product of a test piece for a roller pitching fatigue test.
  • the intermediate product was carburized (gas carburizing and tempering) under the above-mentioned carburizing conditions to prepare a test piece for roller pitching fatigue test (small roller test piece) shown in FIG. 7.
  • FIG. 8 is a schematic diagram of a roller pitching fatigue test.
  • 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 later.
  • the small roller test piece 200 was a test piece for a roller pitching fatigue test produced by the method of the above test piece.
  • the large roller test piece had the shape shown in FIG.
  • the numerical values in FIG. 9 indicate the 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 equivalent to SCM420H specified in JIS G4053 (2016), and the surface was polished after gas carburizing under the same conditions as the small roller test piece 200.
  • the diameter of the large roller test piece 100 was 130 mm.
  • the large roller test piece 100 was pressed against the small roller test piece 200 at a surface pressure of various Hertz stresses.
  • the peripheral speed direction of both roller test pieces at the contact portion is the same, and the slip ratio is -40% (the peripheral speed of the contact portion is 40% higher for the large roller test piece 100 than for the small roller test piece 200).
  • the test was performed by rotating.
  • the oil temperature of ATF (lubricating oil for AT) supplied to the contact portion as lubricating oil was 90 ° C.
  • 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 test terminations was set to 20 million (2.0 ⁇ 107 ). For each test number, the highest stress at which pitching did not occur after repeating 2.0 ⁇ 10 7 times for a plurality of test pieces was defined as the 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 obtained by the following equation.
  • Surface fatigue strength ratio (%) (surface fatigue strength (MPa) of each test number / surface fatigue strength of standard steel (MPa)) ⁇ 100
  • the obtained surface fatigue intensity ratio (%) is shown in the "surface fatigue intensity ratio (%)" column of Table 3.
  • the surface fatigue strength ratio was 120% or more, it was judged that sufficient surface fatigue strength could be obtained.
  • the surface fatigue strength ratio is less than 120%, it is determined that the surface fatigue strength is low.
  • a gear simulation test piece shown in FIG. 10A was produced from a steel material (steel bar having a diameter of 50 mm) having each test number. Specifically, the steel material (steel bar having a diameter of 50 mm) of each test number was heated under the conditions of a heating temperature of 1200 ° C. and a holding time of 30 minutes. Then, hot working (hot forging) was performed at a finishing temperature of 950 ° C. or higher to produce a steel bar having a diameter of 35 mm. A steel bar having a diameter of 35 mm was machined (cut) to prepare a gear simulation test piece before gas carburizing.
  • the numerical value accompanied by "mm” in FIG. 10A indicates the dimension (unit is mm). “ ⁇ ” in the figure means the diameter.
  • the gear simulation test piece had a truncated cone shape.
  • the gear simulation test piece includes a circular upper surface having a diameter of 22 mm and a circular lower surface having a diameter of 34 mm.
  • the gear simulation test piece had a columnar 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 simulation test piece.
  • the inner diameter (diameter) of the prepared gear simulation test piece before carburizing treatment at each position in the longitudinal direction of the through hole TH was measured with a three-dimensional measuring machine.
  • a three-dimensional measuring machine a CNC three-dimensional measuring machine (trade name: Crysta-Apex) manufactured by Mitutoyo Co., Ltd. was used.
  • the gear simulated test piece after the inner diameter measurement was subjected to gas carburizing and tempering under the same conditions as the gas carburizing and tempering with the Ono type rotary bending fatigue test piece.
  • the inner diameter of the through hole TH was measured for the gear simulated test piece after the carburizing treatment by the same method as the method for measuring the inner diameter of the through hole TH of the gear simulated test piece before the carburizing treatment.
  • the ratio of the maximum heat treatment deformation amount of each test number to the maximum heat treatment deformation amount of the reference steel was defined as the "maximum deformation amount ratio". That is, the maximum deformation amount ratio (%) was obtained by the following equation.
  • Maximum deformation amount ratio (%) (maximum heat treatment deformation amount (mm) of each test number / maximum heat treatment deformation amount (mm) of reference steel) ⁇ 100
  • the obtained maximum deformation amount ratio (%) is shown in the "maximum deformation amount ratio (%)" column of Table 3. If the obtained maximum deformation amount ratio is 90% or less, it is determined that the maximum deformation amount ratio is small. On the other hand, when the maximum deformation amount ratio exceeds 90%, it is determined that the maximum deformation amount ratio is large.
  • the ratio of the deformation amount difference of each test number to the deformation amount difference of the reference steel was defined as the deformation amount difference ratio. That is, the deformation amount difference ratio was obtained by the following equation.
  • Deformation amount difference ratio (%) (deformation amount difference of each test number ( ⁇ m) / deformation amount difference of reference steel ( ⁇ m)) ⁇ 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 is 90% or less, it is determined that the deformation amount difference ratio is small. On the other hand, when the deformation amount difference ratio exceeds 90%, it is determined that the deformation amount difference ratio is large.
  • both the maximum deformation amount ratio and the deformation amount difference ratio were 90% or less, it was judged that the heat treatment deformation could be sufficiently suppressed three-dimensionally.
  • the maximum deformation amount ratio and / or the deformation amount difference ratio exceeds 90%, it is judged that the heat treatment deformation cannot be sufficiently suppressed.
  • Table 3 shows the test results.
  • the content of each element was appropriate, and F1 satisfied the formula (1).
  • the production conditions of the steel materials of test numbers 5 to 9 were also appropriate. Therefore, the microstructure of the steel material was appropriate.
  • the microstructure of the cross section of Test Nos. 5 to 9 contained ferrite, and the balance was a structure composed 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.
  • the microstructure of the vertical cross section of Test Nos. 5 to 7 contained ferrite, and the balance was a structure composed 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.
  • the flank wear amount was less than 0.25 mm, and the machinability was high. Further, 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. Further, the maximum deformation amount ratio and the deformation amount difference ratio in the heat treatment were 90% or less, and the heat treatment deformation was sufficiently suppressed three-dimensionally.
  • test number 1 the Si content was too low. Furthermore, F1 did not satisfy equation (1). Further, the holding time of the bulk rolling step was less than 10 hours. Therefore, the standard deviation of the surface integral of the ferrite in the cross section and the vertical section exceeded 4.0%. As a result, the bending fatigue strength and the surface fatigue strength were low. Further, the maximum deformation amount ratio and the deformation amount difference ratio in the heat treatment exceeded 90%, and the heat treatment deformation was not sufficiently suppressed.
  • test numbers 2 to 4 the holding time of the lump rolling process was less than 10 hours. Therefore, the standard deviation of the surface integral of the ferrite in the cross section and the vertical section exceeded 4.0%. As a result, the deformation amount difference ratio in the heat treatment exceeded 90%, and the heat treatment deformation was not sufficiently suppressed.
  • test numbers 16-18 the holding time in the finish rolling process was too short. Therefore, the ferrite average particle size ratio in the cross section and the vertical section exceeded 2.00. As a result, the deformation amount difference ratio in the heat treatment exceeded 90%, and the heat treatment deformation was not sufficiently suppressed.
  • test numbers 22 to 24 the finish temperature of the finish rolling process was too low. Therefore, the ferrite average particle size ratio in the cross section and the vertical section exceeded 2.00. As a result, the deformation amount difference ratio in the heat treatment exceeded 90%, and the heat treatment deformation was not sufficiently suppressed.
  • test numbers 25 to 27 the cooling rate in the cooling process was too slow. Therefore, the arithmetic mean value of the surface integral of the ferrite in the cross section and the vertical section exceeded 70%. Therefore, the deformation amount difference ratio in the heat treatment exceeded 90%, and the heat treatment deformation was not sufficiently suppressed.
  • test number 30 the cooling rate in the temperature holding process was too fast. Therefore, the ferrite average particle size ratio exceeded 2.00 in the microstructure of the vertical cross section. Therefore, the deformation amount difference ratio in the heat treatment exceeded 90%, and the heat treatment deformation was not sufficiently suppressed.
  • Steel materials were manufactured by the following method. With respect to the molten steel, the steel materials (steel bars) of the test numbers 1 to 32 shown in Table 5 were manufactured in the same manner as in Example 1 using the manufacturing condition b in Table 2.
  • Table 5 shows the test results.
  • the content of each element was appropriate, and F1 satisfied the formula (1).
  • the manufacturing conditions of the steel materials of test numbers 1 to 17 were also appropriate. Therefore, the microstructure of the steel material was appropriate.
  • the microstructure of the cross section of test numbers 1 to 17 is composed of ferrite, pearlite and / or bainite, and the arithmetic mean value of the area fraction of ferrite is 50 to 70%, and the area fraction of ferrite. The standard deviation of was 4.0% or less, and the ferrite average particle size ratio was 2.00 or less.
  • the microstructure of the vertical 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 standard deviation of the area fraction of ferrite is 4. It was 0.0% or less, and the ferrite average particle size ratio was 2.00 or less. Therefore, the flank wear amount was less than 0.25 mm, and the machinability was high. Further, 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. Further, the maximum deformation amount ratio and the deformation amount difference ratio in the heat treatment were 90% or less, and the heat treatment deformation was sufficiently suppressed.
  • test numbers 18-23 F1 was too high. Therefore, the maximum deformation amount ratio in the heat treatment exceeded 90%, and the heat treatment deformation was not sufficiently suppressed.
  • test number 24 the C content was too high. Therefore, the flank wear amount was 0.25 mm or more, and the machinability was low.
  • Test number 25 had a Si content that 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 the Mn content was too low. 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 the surface fatigue strength were low.
  • 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 the surface fatigue strength were low.
  • Test number 29 had a Cr content that was too low. 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.
  • test number 30 the Cr content was too high. Therefore, the flank wear amount was 0.25 mm or more, and the machinability was low.
  • Test number 31 had too high Mo content. Therefore, the flank wear amount was 0.25 mm or more, and the machinability was low.
  • Test number 32 had too high an Nb content. Therefore, the bending fatigue strength ratio was less than 110%, and the bending fatigue strength was low.

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  • Chemical & Material Sciences (AREA)
  • Engineering & Computer Science (AREA)
  • Materials Engineering (AREA)
  • Mechanical Engineering (AREA)
  • Metallurgy (AREA)
  • Organic Chemistry (AREA)
  • Solid-Phase Diffusion Into Metallic Material Surfaces (AREA)
  • Heat Treatment Of Steel (AREA)
  • Heat Treatment Of Articles (AREA)

Abstract

L'invention concerne un matériau d'acier qui présente une excellente aptitude au coupage, une excellente résistance à la fatigue par flexion et une excellente résistance à la fatigue de surface même après avoir été soumis à un traitement de carburation au gaz ou similaire, et peut supprimer une déformation de traitement thermique. Le matériau d'acier selon le présent mode de réalisation répond à la formule (1) dans la description et a une composition chimique qui comprend de 0,20 à 0,25 % de carbone, de 0,40 à 0,70 % de silicium, de 0,50 à 0,90 % de manganèse, de 1,00 à 2,00 % de chrome, de 0,005 à 0,050 % de soufre, de 0,0050 à 0,0200 % d'azote, de 0,001 à 0,100 % d'aluminium, une proportion inférieure ou égale à 0,0050 % d'oxygène, et une proportion inférieure ou égale à 0,030 % de phosphore, le reste comprenant du fer et des impuretés. En outre, la microcomposition d'une section transversale horizontale et d'une section transversale verticale comprend de la ferrite, le reste comprenant de la perlite et/ou de la bainite ; la fraction surfacique de la ferrite est de 50 à 70 % ; l'écart-type de la fraction surfacique de la ferrite est inférieur ou égal à 4,0 % ; et le rapport de diamètre moyen des grains de la ferrite est inférieur ou égal à 2,00.
PCT/JP2021/035935 2020-09-30 2021-09-29 Matériau d'acier WO2022071420A1 (fr)

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Citations (4)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
WO2011055651A1 (fr) * 2009-11-05 2011-05-12 住友金属工業株式会社 Barre d'acier ou tige en fil métallique laminée à chaud
WO2013031587A1 (fr) * 2011-08-31 2013-03-07 新日鐵住金株式会社 Barre ou fil en acier laminé pour un forgeage à chaud
JP2013151719A (ja) * 2012-01-25 2013-08-08 Nippon Steel & Sumitomo Metal Corp 熱間鍛造用圧延棒鋼または線材
WO2019182054A1 (fr) * 2018-03-23 2019-09-26 日本製鉄株式会社 Matériau d'acier

Family Cites Families (2)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
JP2011225897A (ja) * 2010-04-15 2011-11-10 Sumitomo Metal Ind Ltd 冷間鍛造用熱間圧延棒鋼または線材
WO2015029553A1 (fr) * 2013-08-26 2015-03-05 新日鐵住金株式会社 Matériau en acier rond laminé pour une barre de crémaillère de direction et barre de crémaillère de direction

Patent Citations (4)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
WO2011055651A1 (fr) * 2009-11-05 2011-05-12 住友金属工業株式会社 Barre d'acier ou tige en fil métallique laminée à chaud
WO2013031587A1 (fr) * 2011-08-31 2013-03-07 新日鐵住金株式会社 Barre ou fil en acier laminé pour un forgeage à chaud
JP2013151719A (ja) * 2012-01-25 2013-08-08 Nippon Steel & Sumitomo Metal Corp 熱間鍛造用圧延棒鋼または線材
WO2019182054A1 (fr) * 2018-03-23 2019-09-26 日本製鉄株式会社 Matériau d'acier

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