JP6211814B2 - Bearing parts and rolling bearings - Google Patents

Description

  The present invention relates to a bearing component and a rolling bearing, and more particularly, to a bearing component that is inexpensive and has improved yield strength and life, and a rolling bearing including the bearing component.

As a measure for improving the durability of bearing parts used for rolling bearings and the like, carbonitriding is known (see, for example, Patent Documents 1 and 2). Carbonitriding treatment, after the steel is heated to a temperature above the A ₁ transformation point of carbon and nitrogen infested diffuse into the steel, a heat treatment for hardening the steel. The carbonitriding process is effective for extending the life under lubrication with foreign matters, which is an important performance of rolling bearings.

  Another important function of the rolling bearing is to reduce the torque during the rotational movement of the machine. In order to achieve this, it is important to reduce energy loss during rotation. Causes of energy loss during the rotation of the rolling bearing include rolling viscous resistance, differential sliding, elastic hysteresis loss, or lubricating oil stirring resistance. Compared to ball bearings and bearings in rolling bearings, ball bearings have less energy loss due to the difference in rolling viscous resistance. Therefore, it can be said that the ball bearing is a more preferable structure from the viewpoint of reducing the torque during the rotational movement of the machine.

  Roller bearings have a larger contact area between bearing parts (bearing rings and balls) than ball bearings, and therefore contact pressure applied to the bearing parts is smaller. Therefore, a roller bearing is effective from the viewpoint of supporting a large load. On the other hand, if a large load is supported in the ball bearing, the contact surface pressure becomes excessive and plastic deformation occurs in the race and the ball. As a result, the rotational motion of the machine is increased in torque, and abnormal noise is generated and rotational accuracy is lowered. As a result, it becomes difficult to satisfy the function as a bearing. Thus, the excessive load (contact surface pressure) that leads to malfunction of the bearing is referred to as “static load capacity” of the rolling bearing. Therefore, it can be said that in reducing the torque of the rolling bearing, it is preferable to employ a ball bearing using a material that is difficult to plastically deform (high yield strength).

  A typical material that hardly undergoes plastic deformation includes a ceramic material such as silicon nitride. However, since this ceramic material is difficult to plastically deform but has difficult workability, there is a problem that when it is used as a bearing material, the processing cost increases. Therefore, in place of the ceramic material, it is required to develop a material having a low total cost including a processing cost and hardly causing plastic deformation. The “difficulty to cause plastic deformation” is not related to the hardness expressed by HV hardness or HRC hardness but to a region where the amount of plastic deformation close to the elastic limit, yield strength, etc. is minute.

JP 2007-277648 A JP 2008-267402 A

  Considering the recent demand for improving the durability of bearing parts, it may be difficult to impart sufficient durability depending on the application in the conventional carbonitriding process. Conventionally, in a ball bearing having a structure advantageous in reducing torque, it has been difficult to prevent plastic deformation without using a material with high processing cost such as silicon nitride.

  The present invention has been made in view of the above problems, and an object of the present invention is to provide a bearing component that is inexpensive and has improved yield hardness and life and a rolling bearing including the bearing component.

The bearing component according to the present invention comprises 0.95 mass% or more and 1.1 mass% or less of carbon, less than 0.3 mass% silicon, less than 0.5 mass% manganese, and 0.008 mass%. Less than sulfur and 1.4% by mass or more and less than 1.6% by mass of chromium, which is made of steel consisting of the remaining iron and impurities, and carburizes the surface layer part including the contact surface that is in contact with other parts This is a bearing component in which a nitride layer is formed. In the bearing component, an average nitrogen concentration in the surface layer portion is 0.3% by mass or more and 0.6% by mass or less, and a variation in nitrogen concentration in the surface layer portion is 0.1% by mass or less . Moreover, in the said bearing component, the amount of retained austenite in the said surface layer part is 8 volume% or less. Moreover, in the said bearing components, the particle size number of the prior austenite crystal grain in the inside in which the carbonitriding layer is not formed is JIS standard 9th or more and 11th or less.

  The present inventor has intensively studied measures for improving the yield strength and improving the life without using a material having a high processing cost. As a result, the following knowledge was obtained and the present invention was conceived.

  In a bearing part, damage such as a crack is likely to occur on a contact surface (for example, a rolling surface of a bearing ring, a rolling surface of a ball and a roller, or the like) that comes into contact with another component and directly below the contact surface. On the other hand, the durability of the bearing component can be improved by subjecting the contact surface to carbonitriding.

  According to the study of the present inventor, when the nitrogen concentration in the surface layer portion including the contact surface is less than 0.2% by mass, the life of the bearing component under the foreign matter mixed lubrication is reduced. Therefore, in order to suppress a decrease in the life of the bearing component, the nitrogen concentration in the surface layer portion needs to be at least 0.2% by mass or more. On the other hand, when the nitrogen concentration in the surface layer portion exceeds 0.7% by mass, the chromium in the matrix is almost lost, so that the hardenability is lowered, and as a result, incomplete quenching is likely to occur. Therefore, in order to suppress the deterioration of hardenability and the occurrence of incomplete quenching, the nitrogen concentration in the surface layer portion needs to be 0.7% by mass or less.

  The bearing component is manufactured by subjecting the formed steel material to a heat treatment such as carbonitriding or tempering, and then finishing the contact surface. The steel material may be deformed by the heat treatment (for example, the raceway may be elliptical and the roundness may be lost), and the grinding allowance during finishing may vary. Therefore, the conventional bearing component has a problem that the variation of the nitrogen concentration becomes large in the surface layer portion.

  On the other hand, in the bearing component according to the present invention, the average nitrogen concentration in the surface layer portion is 0.3% by mass or more and 0.6% by mass or less, and the variation in nitrogen concentration in the surface layer portion is 0.00. It is reduced to 1% by mass or less. For this reason, in the bearing component, the nitrogen concentration in the surface layer portion is 0.2% by mass or more and 0.7% by mass or less, and a decrease in the life under the contamination with foreign matters is suppressed. Moreover, in the said bearing component, since the steel structure is refined | miniaturized until the magnitude | size of the prior austenite crystal grain in the inside in which the carbonitriding layer is not formed becomes JIS standard 9th or less and 11th or less, durability is further improved. It has improved. Therefore, according to the bearing component according to the present invention, it is possible to more reliably provide a bearing component having an improved life.

  Further, according to the study of the present inventor, the amount of retained austenite in the surface layer portion is reduced to 8% by volume or less by increasing the heating temperature during the tempering process as compared with the conventional one, and as a result, the yield strength of the material is improved To do. That is, in the bearing component in which the amount of retained austenite in the surface layer portion is reduced to 8% by volume or less, plastic deformation of the material can be suppressed without using a material such as silicon nitride that has a high processing cost.

  Further, as described above, the life of the bearing component can be improved by increasing the nitrogen concentration in the surface layer portion. However, in conventional bearing parts, the yield strength of the material decreases as the nitrogen concentration in the surface layer increases, so it has been difficult to achieve both improved yield strength and improved life. On the other hand, according to the study by the present inventor, when the tempering temperature is made higher than before, the reciprocal relationship between the yield strength and the life is eliminated. That is, by raising the tempering temperature and reducing the amount of retained austenite in the surface layer portion to 8% by volume or less, it is possible to suppress a decrease in yield strength even when the nitrogen concentration in the surface layer portion is increased to the above range. Therefore, according to the bearing component according to the present invention, it is possible to provide a bearing component that is inexpensive and has improved yield strength and life.

  In the bearing component according to the present invention, the “surface layer portion” means a region from the contact surface to a depth of 20 μm in the thickness direction of the bearing component. Further, “average nitrogen concentration in the surface layer portion” and “variation in nitrogen concentration in the surface layer portion” are as defined in the embodiments of the present invention described later.

  Next, the reason why the component composition of the steel constituting the bearing part according to the present invention is set in the above range will be described.

Carbon: 0.95 mass% or more and 1.1 mass% or less Carbon content has a big influence on the hardness of a bearing component and the amount of carbides after quench hardening. When the carbon content of the steel is 0.95% by mass or more, sufficient hardness and carbide content can be achieved without introducing a large amount of carbon into the steel by heat treatment. On the other hand, when the carbon content exceeds 1.1% by mass, a large carbide is formed at the time of manufacturing the steel, which may adversely affect the durability of the bearing component. Therefore, the carbon content is set to 0.95 mass% or more and 1.1 mass% or less.

Silicon: Less than 0.3% by mass Silicon increases the hydrogen storage amount in steel and promotes hydrogen embrittlement. When the silicon content of steel is 0.3% by mass or more, exfoliation due to hydrogen embrittlement is likely to occur in applications where hydrogen easily enters steel. For this reason, in the above bearing component, the silicon content of steel was set to a low value of less than 0.3% by mass.

Manganese: Less than 0.5 mass% Manganese contributes to the hardenability of the steel and the hardness of the steel before quenching. However, when the manganese content is 0.5% by mass or more, the hardness of the material before quenching is increased, and the workability in the cold process is lowered. Therefore, the manganese content is set to less than 0.5% by mass.

Sulfur: Less than 0.008% by mass Sulfur chemically bonds with manganese and forms non-metallic inclusions such as manganese sulfide. This non-metallic inclusion can adversely affect the life of the bearing. Therefore, in the said bearing component, the sulfur content of steel was set low to less than 0.008 mass%.

Chromium: 1.4 mass% or more and less than 1.6 mass% Chromium contributes to the improvement of hardenability of steel. Further, in the bearing component according to the present invention, the hardenability is lowered because the silicon content is low in order to prevent peeling due to hydrogen embrittlement. Therefore, in order to compensate for the decrease in hardenability due to the lowering of the silicon content, the chromium content of the steel is set to be higher than 1.4% by mass and lower than 1.6% by mass in the bearing component.

  In the bearing component, a residual austenite amount in the surface layer portion may be 5% by volume or less.

  When the tempering temperature is further increased, the amount of retained austenite in the surface layer portion is reduced to 5% by volume or less. Thereby, the yield strength of the material can be further improved.

  In the bearing component, the inclination of the nitrogen concentration in the thickness direction of the bearing component may be −15 (1 / m) or more. The slope of the nitrogen concentration is measured as described in the examples described later. Thereby, the dispersion | variation in the nitrogen concentration in the said surface layer part after finishing a finishing process to the said contact surface can be reduced easily.

  The “nitrogen concentration gradient” may be the gradient of nitrogen concentration before finishing such as grinding on the contact surface, or nitrogen after finishing the contact surface (that is, the product state). It may be a gradient of density. That is, in the bearing component, the slope of the nitrogen concentration may be −15 (1 / m) or more before finishing the contact surface, or the slope of the nitrogen concentration is − after finishing the finish. It may be 15 (1 / m) or more, and the slope of the nitrogen concentration may be -15 (1 / m) or more before and after the finishing.

In the bearing component, five or more carbonitrides having a diameter of 0.3 μm or more and 0.5 μm or less may be present per 100 μm ² in the surface layer portion.

According to the study of the present inventor, when 5 or more carbon nitrides having a diameter of 0.3 μm or more and 0.5 μm or less exist in the surface layer portion per 100 μm ² , the bearing parts are statically strengthened by precipitation strengthening of the carbonitride. Load capacity is improved. Therefore, by defining the abundance of the carbonitride in the surface layer within the above range, the static load capacity of the bearing component can be further improved. In this case, the carbon concentration in the surface layer portion is 0.9% by mass or more and 1.1% by mass or less.

Here, “there are 5 or more carbon nitrides having a diameter of 0.3 μm or more and 0.5 μm or less in the surface layer portion per 100 μm ² ” is obtained by cutting the bearing component in a cross section perpendicular to the contact surface. When the surface layer portion of the cross section is observed with a microscope, 5 or more carbonitrides having a diameter of 0.3 μm or more and 0.5 μm or less are confirmed per 100 μm ² . The “carbonitride” refers to iron carbide or a part of carbon of the carbide substituted with nitrogen, and includes Fe—C compounds and Fe—C—N compounds. Moreover, this carbonitride may contain the alloy elements contained in steel, such as chromium.

  In the bearing component, a nitrogen concentration in a non-grinding portion including a non-grinding surface other than the contact surface may be less than 0.7% by mass.

  According to the study of the present inventor, when the nitrogen concentration in the non-grinding portion is 0.7% by mass or more, the hardenability is lowered and an incompletely hardened structure is easily generated. Therefore, in order to suppress the deterioration of hardenability and the generation of an incompletely hardened structure, the nitrogen concentration in the non-ground part is preferably less than 0.7% by mass. The “non-ground portion” means a region from the non-ground surface to a depth of 20 μm in the thickness direction of the bearing component. In this case, the hardness at a depth of 0.1 mm from the non-ground surface is 700 HV or more.

  In the bearing component, after heat treatment at a heating temperature of 500 ° C. and a holding time of 1 hour, the Vickers hardness at a position of a depth of 0.4 (mm) from the contact surface is the thickness of the bearing component. It may be 80 HV or more higher than the Vickers hardness in the region where the carbonitrided layer is not formed.

  Thereby, it can be assured that the nitrogen concentration at the contact surface is 0.4 mass% or more.

  The rolling bearing according to the present invention comprises the bearing component according to the present invention with improved yield strength and life. Therefore, according to the rolling bearing according to the present invention, it is possible to provide a rolling bearing with improved durability.

  As is apparent from the above description, according to the bearing component according to the present invention, it is possible to provide a bearing component that is inexpensive and has improved yield strength and life. Moreover, according to the rolling bearing according to this invention, the rolling bearing which improved durability can be provided.

It is a schematic sectional drawing which shows the structure of the deep groove ball bearing which concerns on this Embodiment. It is the schematic for demonstrating the measuring method of the nitrogen concentration in the bearing component which concerns on this Embodiment. It is a graph which shows the measurement result of the nitrogen concentration in the bearing component which concerns on this Embodiment. It is a flowchart for demonstrating the manufacturing method of the bearing component which concerns on this Embodiment. It is the schematic for demonstrating the detail of the hardening hardening process (S20) in the manufacturing method of the bearing components which concerns on this Embodiment. It is a schematic diagram for explaining the undecomposed NH ₃ minutes pressure control step included in the atmosphere control step of FIG. It is a diagram for explaining the H ₂ partial pressure control step included in the atmosphere control step of FIG. It is a figure which shows an example of the heating pattern in the heating pattern control process included in the carbonitriding process of FIG. Is a graph showing the relationship between the nitrogen concentration and L ₁₀ life of the surface layer portion in the indentation-originated flaking life test. It is a graph showing the relationship between the variation and L ₁₀ life of the nitrogen concentration in the surface layer portion of the clean oil life test. It is a graph which shows nitrogen concentration distribution in the surface layer vicinity of an inner ring. It is a cross-sectional SEM photograph of the test piece of a comparative example. It is a cross-sectional SEM photograph of the test piece of an Example. It is a graph which shows the influence which presence of carbonitride has on indentation depth. It is the schematic for demonstrating the measuring method of the nitrogen concentration in a sample. It is a graph which shows the relationship between tempering temperature and a cross-sectional hardness difference. It is a graph which shows the relationship between nitrogen concentration and a cross-sectional hardness difference. It is a graph which shows the relationship between nitrogen concentration in the range whose nitrogen concentration is 0.1 mass% or less, and cross-sectional hardness difference. It is a graph which shows nitrogen concentration distribution in steel after a carbonitriding process. It is a graph which shows nitrogen concentration distribution in steel after a nitrogen diffusion process. It is a figure which shows the relationship between nitrogen concentration, tempering temperature, and residual indentation depth. It is a figure which shows the Weibull plot of an indentation origin type | mold peeling life. It is a figure which shows the rapid acceleration / deceleration pattern in a hydrogen resistance life test. It is a figure which shows the Weibull plot of a hydrogen-resistant lifetime. It is a figure which shows the relationship between tempering temperature and a retained austenite amount. It is a figure which shows the relationship between tempering temperature and the area ratio of a precipitate. It is a photograph of the precipitate when the tempering temperature is 180 ° C. It is a photograph of the precipitate when the tempering temperature is 210 ° C. It is a photograph of the precipitate when the tempering temperature is 240 ° C. It is a photograph of the precipitate when the tempering temperature is 260 ° C. It is a photograph of prior austenite crystal grains in an unnitrided region.

  Hereinafter, embodiments of the present invention will be described with reference to the drawings. In the following drawings, the same or corresponding parts are denoted by the same reference numerals, and description thereof will not be repeated.

  First, with reference to FIG. 1, the structure of the deep groove ball bearing 1 as a rolling bearing which concerns on this Embodiment is demonstrated. The deep groove ball bearing 1 includes an annular outer ring 11, an annular inner ring 12 disposed inside the outer ring 11, and a rolling element that is disposed between the outer ring 11 and the inner ring 12 and is held by an annular retainer 14. And a plurality of balls 13. An outer ring rolling surface 11 </ b> A is formed on the inner circumferential surface of the outer ring 11, and an inner ring rolling surface 12 </ b> A is formed on the outer circumferential surface of the inner ring 12. The inner ring 12 is disposed inside the outer ring 11 so that the inner ring rolling surface 12A faces the outer ring rolling surface 11A. The plurality of balls 13 are in contact with the outer ring rolling surface 11A and the inner ring rolling surface 12A on the rolling surface 13A, and are arranged at a predetermined pitch in the circumferential direction by the cage 14. Thereby, the plurality of balls 13 are held on the annular raceway of the outer ring 11 and the inner ring 12 so as to be freely rollable. With such a configuration, the outer ring 11 and the inner ring 12 of the deep groove ball bearing 1 are rotatable relative to each other. Moreover, the outer ring | wheel 11, the inner ring | wheel 12, and the ball | bowl 13 are bearing components which concern on this Embodiment mentioned later.

  Next, the structure of the bearing component (the outer ring 11, the inner ring 12, and the ball 13) according to the present embodiment will be described. The bearing component comprises 0.95 mass% or more and 1.1 mass% or less of carbon, less than 0.3 mass% silicon, less than 0.5 mass% manganese, less than 0.008 mass% sulfur, And 1.4% by mass or more and less than 1.6% by mass of chromium, and is made of steel consisting of the remaining iron and impurities. The bearing component has contact surfaces (outer ring rolling surface 11A, inner ring rolling surface 12A, rolling surface 13A) that come into contact with other components, and a carbonitriding layer is formed on the surface layer portion including the contact surface. Is formed.

  In the bearing component, the average nitrogen concentration in the surface layer portion is 0.3 mass% or more and 0.6 mass% or less, and the variation in nitrogen concentration in the surface layer portion is 0.1 mass% or less. . Thereby, in the said bearing components, the lifetime under the foreign material mixing lubrication is improved, and generation | occurrence | production of the incompletely hardened structure | tissue is also suppressed. Moreover, in the said bearing component, the steel structure is refined | miniaturized until the prior austenite crystal grain in the inside in which the carbonitriding layer is not formed becomes JIS standard 9th or more and 11th or less. Therefore, the durability of the bearing component is further improved. In the bearing component, the amount of retained austenite in the surface layer portion is 8% by volume or less (preferably 5% by volume or less). In the bearing component, the area ratio of precipitates in the inside (non-nitrided region) where the carbonitrided layer is not formed is 11% or more (preferably 12% or more). Thereby, the yield strength of the material of the bearing part is improved. Therefore, the bearing parts (the outer ring 11, the inner ring 12, and the balls 13) have improved yield strength and life, and the deep groove ball bearing 1 having the bearing parts has improved durability.

  In the bearing component, “average nitrogen concentration in the surface layer portion” and “variation in nitrogen concentration in the surface layer portion” are measured as follows. Here, the case where the inner ring 12 is measured will be described as an example.

  Referring to FIG. 2, first, measurement point S <b> 1 is set at an arbitrary location on the contact surface (inner ring rolling surface 12 </ b> A) of inner ring 12. Next, the measurement point S2 shifted by θ (30 °) in the circumferential direction as viewed from the measurement point S1, the measurement point S3 shifted by θ (30 °) in the circumferential direction as viewed from the measurement point S2, and the measurement point S3 Measurement point S4 shifted by θ (30 °) in the circumferential direction when viewed from the side, measurement point S5 shifted by θ (30 °) in the circumferential direction when viewed from the measurement point S4, and circumferential direction when viewed from measurement point S5 And a measurement point S6 shifted by θ (30 °). In this way, a plurality of measurement points S1 to S6 that are shifted by 30 ° along the circumferential direction are set on the contact surface of the inner ring 12. Note that the measurement points S1 to S6 are set on the axially central portion on the contact surface of the inner ring 12.

  The races such as the inner ring 12 may be deformed into an oval shape by heat treatment and the roundness may be lost, which may cause variations in the nitrogen concentration in the surface layer after grinding. On the other hand, when the measurement points S1 to S6 that are shifted by 30 ° along the circumferential direction are set, the measurement points are distributed and arranged in a substantially half-circumferential region in the circumferential direction. The measurement points S1 to S6 can include a maximum value and a minimum value of the nitrogen concentration. Therefore, by performing the evaluation based on the measurement values at the measurement points S1 to S6, the “average nitrogen concentration in the surface layer portion” and “the variation in the nitrogen concentration in the surface layer portion” can be more accurately evaluated.

  FIG. 3 shows the nitrogen concentration (vertical axis) of the surface layer measured at the measurement points S1 to S6 (horizontal axis). The average value of each nitrogen concentration shown on the vertical axis in FIG. 3 can be referred to as “average nitrogen concentration in the surface layer portion”. The largest value among the differences between the “average nitrogen concentration in the surface layer portion” and the measurement values at the measurement points S1 to S6 can be defined as “the variation in the nitrogen concentration in the surface layer portion”.

  In the bearing parts (the outer ring 11, the inner ring 12, and the ball 13), nitrogen is applied in the thickness direction before finishing the contact surfaces (the outer ring rolling surface 11A, the inner ring rolling surface 12A, and the rolling surface 13A). The gradient of density may be −15 (1 / m) or more. Thereby, after finishing the contact surface, variation in the nitrogen concentration in the surface layer portion can be reduced to 0.1 mass% or less. In the bearing component, even after finishing the contact surface, the slope of the nitrogen concentration in the thickness direction may be −15 (1 / m) or more.

Further, in the bearing component (outer ring 11, inner ring 12, ball 13), 5 or more carbonitrides having a diameter of 0.3 μm or more and 0.5 μm or less may exist in the surface layer portion per 100 μm ² . Thereby, the static load capacity of the bearing component can be further improved.

  In the bearing parts (outer ring 11, inner ring 12, ball 13), non-ground surfaces 11B and 12B, which are surfaces other than the contact surfaces (outer ring rolling surface 11A, inner ring rolling surface 12A, rolling surface 13A), are provided. The nitrogen concentration in the non-grinding part to include may be less than 0.7 mass%. Thereby, the fall of hardenability and generation | occurrence | production of incomplete hardened structure | tissue can be suppressed.

  The bearing parts (outer ring 11, inner ring 12, ball 13) are subjected to heat treatment with a heating temperature of 500 ° C. and a holding time of 1 hour, and then the contact surface (outer ring rolling surface 11A, inner ring rolling). The Vickers hardness at a depth of 0.4 (mm) from the surface 12A and the rolling surface 13A) is 80HV or more higher than the Vickers hardness in the region where the carbonitriding layer is not formed in the thickness direction of the bearing component. May be. Thereby, it can be assured that the nitrogen concentration at the contact surface is 0.4 mass% or more.

  Next, a method for manufacturing a bearing component according to the present embodiment will be described. In the bearing component manufacturing method according to the present embodiment, the bearing components (the outer ring 11, the inner ring 12, and the ball 13) according to the present embodiment can be manufactured.

  Referring to FIG. 4, first, a steel material preparation step is performed as a step (S10). In this step (S10), first, carbon of 0.95 mass% to 1.1 mass%, silicon of less than 0.3 mass%, manganese of less than 0.5 mass%, and 0.008 mass% The steel material which contains less iron and 1.4 mass% or more and less than 1.6 mass% chromium, and consists of remainder iron and impurities is prepared. And the said steel material is shape | molded by the schematic shape of a bearing component. For example, a steel bar, steel wire or the like is used as a raw material, and the steel bar, steel wire or the like is subjected to processing such as cutting, forging, turning, etc., so that the outer ring 11, inner ring 12 and ball 13 which are bearing parts are roughly outlined. A steel material formed into a shape is prepared.

Next, a quench hardening process is implemented as process (S20). In this step (S20), after the carbonitriding treatment and the nitrogen diffusion treatment are sequentially performed on the steel material prepared in the step (S10), the temperature of the steel material is equal to or lower than the M _s point (martensitic transformation start point). Cooled to. This step (S20) will be described in detail later.

Next, a tempering step is performed as a step (S30). In this step (S30), with respect to quench hardened steel in the step (S20), heat-treated at a temperature of less than ₁ point A is performed. More specifically, after the step (S20) is completed, the steel is kept at a temperature of 240 ° C. or higher, preferably 240 ° C. or higher and 260 ° C. or lower, which is a temperature of A ₁ point or lower, for a predetermined time (eg, 2 hours). The steel material is tempered by being held. Thereafter, the steel material is cooled by air at room temperature (air cooling). Thereby, the toughness etc. of steel materials can be improved.

  Next, a finishing step is performed as a step (S40). In this step (S40), a grinding process is performed on the contact surfaces (the outer ring rolling surface 11A, the inner ring rolling surface 12A, and the rolling surface 13A) of the tempered steel material. Thereby, the outer ring 11, the inner ring 12, and the ball 13 (see FIG. 1), which are bearing parts according to the present embodiment, are manufactured, and the manufacturing method of the bearing part according to the present embodiment is completed. And the deep groove ball bearing 1 (refer FIG. 1) is manufactured by combining the manufactured outer ring | wheel 11, the inner ring | wheel 12, and the ball | bowl 13. FIG.

Next, the quench hardening step (S20) will be described in detail with reference to FIGS. FIG. 5 is a diagram for explaining the quench hardening process (S20) in detail. FIG. 6 is a diagram for explaining an undecomposed ammonia (NH ₃ ) partial pressure control step included in the atmosphere control step of FIG. FIG. 7 is a diagram for explaining a hydrogen (H ₂ ) partial pressure control step included in the atmosphere control step of FIG. Moreover, FIG. 8 is a figure which shows an example of the heating pattern (temperature history) in the heating pattern control process included in the carbonitriding process of FIG. In FIG. 8, the horizontal direction indicates time, and the time has passed as it goes to the right.

Referring to FIG. 5, in the quench hardening process (S20), first, a carbonitriding process is performed in which the steel material prepared in the above process (S10) is carbonitrided. Next, a nitrogen diffusion step for diffusing nitrogen that has entered the steel in the carbonitriding step is performed. And after a nitrogen diffusion process is completed, the cooling process which cools steel materials to the temperature below _Ms point is implemented. In the carbonitriding step, the steel material is heated in an atmosphere containing ammonia, carbon monoxide, carbon dioxide, and hydrogen.

The carbonitriding process includes an atmosphere control process 30 in which the atmosphere in the heat treatment furnace is controlled, and a heating pattern control process 40 in which the temperature history applied to the steel material that is the object to be processed in the heat treatment furnace is controlled. . The atmosphere control process 30 and the heating pattern control process 40 can be performed independently and in parallel. The atmosphere control step 30 includes an undecomposed NH ₃ partial pressure control step 31 in which the undecomposed ammonia partial pressure in the heat treatment furnace is controlled, and an H ₂ partial pressure control step 32 in which the hydrogen partial pressure in the heat treatment furnace is controlled. And a CO / CO ₂ partial pressure control step 33 in which the partial pressure of at least one of carbon monoxide and carbon dioxide in the heat treatment furnace is controlled.

In the CO / CO ₂ partial pressure control step 33, with reference to the following formula (1), the carbon activity is controlled by controlling the partial pressure of at least one of carbon monoxide and carbon dioxide in the heat treatment furnace. ( _Ac ^* ) is controlled. Strictly speaking, a _c > 1 is not satisfied in the definition of activity. Therefore, when a _c ^* ≦ 1, it is assumed that a _c ^* = _ac , and when a _c ^* > 1 (for example, the partial pressure of carbon monoxide (P _CO ) is high and the partial pressure of carbon dioxide (P _CO2 ) Is low), it is assumed that a _c ^* is a variable according to the following equation (1).

In the atmosphere control step 30, a _c ^* defined by the above formula (1) is 0.88 or more and 1.27 or less (preferably 0.9 or more and 1.1 or less), and the following formula ( 2) Undecomposed NH ₃ partial pressure control step 31, H ₂ partial pressure so that the value of α represented by 2) is in the range of 0.012 to 0.020 (preferably 0.013 to 0.018). A control step 32 and a CO / CO ₂ partial pressure control step 33 are performed. In formula (2), P _N (atm) is the partial pressure of undecomposed ammonia, and P _H (atm) is the partial pressure of hydrogen.

Specifically, referring to FIG. 6, in the undecomposed NH ₃ partial pressure control step 31, first, an undecomposed NH ₃ partial pressure measuring step (S11) for measuring the undecomposed ammonia partial pressure in the heat treatment furnace is performed. Is done. The measurement of the undecomposed ammonia partial pressure can be performed using, for example, a gas chromatograph or an infrared analyzer. Based on the undecomposed ammonia partial pressure measured in the step (S11), it is determined whether or not the NH ₃ supply amount adjustment step (S13) for increasing or decreasing the supply amount of ammonia gas to the heat treatment furnace is necessary. A decomposition NH ₃ partial pressure determination step (S12) is performed. The determination is made by comparing the target undecomposed ammonia partial pressure, which is determined in advance so that the value of α is in the range of 0.012 to 0.020, and the measured undecomposed ammonia partial pressure. The determination is made by determining whether the undecomposed ammonia partial pressure is the target undecomposed ammonia partial pressure.

  When the undecomposed ammonia partial pressure is not equal to the target undecomposed ammonia partial pressure, after the step (S13) for increasing or decreasing the undecomposed ammonia partial pressure in the heat treatment furnace is performed, the step (S11) is performed. Will be implemented again. The step (S13) includes, for example, a mass flow controller in which the amount of ammonia (amount of ammonia gas) flowing into the heat treatment furnace per unit time from an ammonia gas cylinder connected to the heat treatment furnace via a pipe is attached to the pipe. It can implement by adjusting with the flow control apparatus provided with. That is, when the measured partial pressure of undecomposed ammonia is higher than the target partial pressure of undecomposed ammonia, the step (S13) can be performed by decreasing the flow rate and increasing the flow rate when the partial pressure is low. . In this step (S13), when there is a predetermined difference between the measured undecomposed ammonia partial pressure and the target undecomposed ammonia partial pressure, it was experimentally determined in advance how much the flow rate should be increased or decreased. It can be determined based on the relationship between the increase / decrease in the flow rate of ammonia gas and the increase / decrease in the partial pressure of undecomposed ammonia.

  On the other hand, when the undecomposed ammonia partial pressure is the target undecomposed ammonia partial pressure, the step (S11) is performed again without performing the step (S13).

The H ₂ partial pressure control step 32 is performed in the same manner as the undecomposed NH ₃ partial pressure control step 31 described above. That is, referring to FIG. 7, in the H ₂ partial pressure control step 32, first, an H ₂ partial pressure measurement step (S21) for measuring the hydrogen partial pressure in the heat treatment furnace is performed. The measurement of the hydrogen partial pressure can be performed using, for example, a heat conduction gas analyzer. Then, based on the hydrogen partial pressure measured in the step (S21), it is determined whether or not the H ₂ supply amount adjusting step (S23) for increasing or decreasing the supply amount of hydrogen gas to the heat treatment furnace is necessary. A determination step (S22) is performed. The determination is made by comparing the target hydrogen partial pressure determined in advance so that the value of α is in the range of 0.012 or more and 0.020 or less and the measured hydrogen partial pressure. Is carried out by determining whether or not is at the target hydrogen partial pressure.

  When the hydrogen partial pressure is not the target hydrogen partial pressure, the step (S23) for increasing or decreasing the hydrogen partial pressure in the heat treatment furnace is performed, and then the step (S21) is performed again. The step (S23) includes, for example, a mass flow controller in which the amount of hydrogen (flow rate of hydrogen gas) flowing into the heat treatment furnace per unit time from a hydrogen gas cylinder connected to the heat treatment furnace via a pipe is attached to the pipe It can implement by adjusting with the flow control apparatus provided with. That is, when the measured hydrogen partial pressure is higher than the target hydrogen partial pressure, the step (S23) can be performed by decreasing the flow rate, and when it is low, increasing the flow rate. In this step (S23), when there is a predetermined difference between the measured hydrogen partial pressure and the hydrogen partial pressure, how much the flow rate is increased or decreased is experimentally determined in advance as in the case of ammonia. It can be determined based on the relationship between the increase or decrease of the hydrogen gas flow rate and the increase or decrease of the hydrogen partial pressure.

  On the other hand, when the hydrogen partial pressure is the target hydrogen partial pressure, the step (S21) is performed again without performing the step (S23).

Referring to FIG. 5, in the CO / CO ₂ partial pressure control step 33, the supply amount of propane (C ₃ H ₈ ) gas, butane gas (C ₄ H ₁₀ ), or the like as an enriched gas is adjusted, so that CO 2 The partial pressure of at least one of the partial pressure of CO ₂ and CO ₂ is controlled, and a _c ^* is adjusted. Specifically, for example, the partial pressure P _CO2 partial pressure P _CO and carbon monoxide to carbon dioxide in the atmosphere by using an infrared gas concentration measurement device are measured. And based on the said measured value, propane (C as an enriched gas) so that a _c ^* defined by the above formula (1) becomes a target value within the range of 0.88 or more and 1.27 or less. The supply amount of ₃ H ₈ ) gas, butane gas (C ₄ H ₁₀ ), etc. is adjusted.

Here, the value of α is determined by the undecomposed NH ₃ partial pressure control step 31, the H ₂ partial pressure control step 32, and the CO / CO ₂ partial pressure control step 33 with reference to the above equation (2). It can be controlled by changing at least one of cracked ammonia partial pressure, hydrogen partial pressure, and a _c ^* . That is, the value of α is determined by, for example, the H ₂ partial pressure in a state where the undecomposed NH ₃ partial pressure control step 31 and the CO / CO ₂ partial pressure control step 33 keep the undecomposed ammonia partial pressure and a _c ^* constant. The control step 32 may control by changing the hydrogen partial pressure, or the hydrogen partial pressure and a _c ^* value are kept constant by the H ₂ partial pressure control step 32 and the CO / CO ₂ partial pressure control step 33. In this state, the partial pressure of undecomposed ammonia may be changed and controlled by the undecomposed NH ₃ partial pressure control step 31.

Furthermore, with reference to FIG. 5, in the heating pattern control process 40, the heating log | history provided to steel materials is controlled. Specifically, as shown in FIG. 8, the steel material in an atmosphere which is controlled by an atmosphere control step 30 described above, A ₁ transformation point or more in a 820 ° C. or higher 880 ° C. or less (preferably not more than 870 ° C. 830 ° C. or higher ) At a temperature of 180 minutes to 600 minutes (preferably 240 minutes to 480 minutes). When the holding time elapses, the heating pattern control process 40 ends, and at the same time, the atmosphere control process 30 ends.

Referring to FIG. 5, a nitrogen diffusion process is performed after the carbonitriding process is completed. In this step, the steel material is heated at a temperature equal to or lower than the treatment temperature in the carbonitriding step, and is maintained for 30 minutes to 120 minutes (preferably 45 minutes to 90 minutes). Thereby, the nitrogen which penetrate | invaded in steel can be diffused. In this step, a _c ^* is 0.88 to 1.27 (preferably 0.9 to 1.1), and α is 0.003 to 0.012 (preferably 0). 0.003 or more and 0.008 or less), the atmosphere in the heat treatment furnace is controlled. The control of the a _c ^* value and the α value can be performed in the same manner as in the carbonitriding step.

Referring to FIG. 5, the cooling process is performed after the nitrogen diffusion process is completed. In this step, the steel material is immersed in oil (oil-cooled) to be cooled to a temperature not higher than the _MS point. By performing the above steps (carbonitriding step, nitrogen diffusion step, and cooling step) in order, the surface layer portion of the steel material is carbonitrided and quenched and hardened.

Example 1
First, the influence of the average nitrogen concentration in the surface layer and the variation in nitrogen concentration on the durability of the bearing parts was investigated. Specifically, the indentation origin type peeling life and the cleaning oil lubrication life were evaluated. The experimental procedure is as follows.

The test was carried out using a deep groove ball bearing of JIS standard 6206 model number (inner diameter 30 mm, outer diameter 62 mm, width 16 mm, 9 rolling elements). First, an inner ring was produced by the same procedure as in the present embodiment (carbonitriding temperature: 850 ° C., tempering temperature: 240 ° C.). In the carbonitriding process, the concentration distribution of nitrogen entering the surface of the inner ring was controlled by adjusting the partial pressure of undecomposed ammonia, hydrogen partial pressure, carbon activity, heat treatment time, and quenching temperature. For comparison, an inner ring that does not perform the nitrogen diffusion step after the carbonitriding step was also produced.
(Indentation origin peel life test)
An indentation was formed by pressing an indenter for measuring the Rockwell hardness of a conical diamond with a load of 196 N in the center of the groove bottom of the rolling surface of the produced inner ring. Thirty indentations were formed per inner ring, and were formed at equal intervals in the circumferential direction (that is, every 12 ° of the central angle).

Next, a bearing was produced by combining the produced inner ring with the outer ring, rolling elements and retainer. And the indentation origin type peeling life test was done using the produced bearing. A tester having a structure in which a radial load is equally applied to two bearings was used. A test was performed by applying a load of about 3.04 GPa to one bearing and rotating the bearing at a rotational speed of 3000 rpm. Lubrication was performed by continuously flowing a certain amount of oil into the housing in which the test bearings were arranged.
(Clean oil life test)
A bearing was produced by combining the produced inner ring with the outer ring, rolling elements and cage. Here, the nitrogen concentration in the inner ring, the outer ring, and the surface layer portion of the rolling element was set to 0.4 mass%. And the clean oil life test was done using the produced bearing. A test was performed by applying a load of about 3.04 GPa to one bearing and rotating the bearing at a rotational speed of 2000 rpm. Lubrication was performed by continuously flowing a certain amount of oil into the housing in which the test bearings were arranged.

  The relationship between the nitrogen concentration in the surface layer portion of the inner ring and the life was examined by the indentation origin type peeling life test. In addition, when the nitrogen concentration of the inner ring, outer ring, and rolling element surface layer is constant (0.4% by mass), the relationship between the variation in nitrogen concentration in the surface layer part and the life is also investigated by the cleaning oil life test. did. The “variation in the nitrogen concentration in the surface layer portion” was measured by the same method as in the above embodiment (see FIGS. 2 and 3).

The test results are shown in FIG. 9 and FIG. 9, the nitrogen concentration of the inner ring of the surface layer portion (horizontal axis, mass%), shows the relationship between the L ₁₀ life of indentation-originated flaking life (vertical axis, h). Figure 10 is a variation of the nitrogen concentration of the inner ring of the surface layer portion (horizontal axis, mass%) and the lifetime of the L ₁₀ life (the vertical axis, h) shows the relationship between the.

As shown in FIG. 9, when the nitrogen concentration in the surface layer portion is less than 0.2 mass% (shown by the broken line in FIG. 9), the L ₁₀ life is less than that in the case of 0.4 mass%. It decreased to 2 or less. On the other hand, when nitrogen was added until it exceeded 0.7 mass%, since hardness fell to less than 650HV, the test could not be implemented. This is because the hardenability of the bearing is reduced and an incompletely hardened structure is generated.

Further, as shown in FIG. 10, while the variation of the nitrogen concentration of 0.1% by weight (shown in broken lines in FIG. 10) above a certain L ₁₀ life if less is ensured, 0 If more than .1% by weight _{L 10} life was reduced significantly. From these results, in order to suppress the life under the contamination with foreign matter and the decrease in the hardness of the contact surface, the nitrogen concentration of the surface layer portion should be 0.2% by mass or more and 0.7% by mass or less, that is, the surface layer It has been found that it is effective to set the average nitrogen concentration in the part to 0.3 mass% or more and 0.6 mass% or less, and the variation in the nitrogen concentration in the surface layer portion to 0.1 mass% or less.
(Example 2)
Next, the relationship between the variation in the nitrogen concentration in the surface layer and the slope of the nitrogen concentration was investigated. First, steps (S10) to (S30) were performed by the same procedure as in the present embodiment to produce an inner ring (Example). The time for the carbonitriding process was 4 hours, and the time for the nitrogen diffusion process was 1 hour. Moreover, the inner ring | wheel which does not implement a nitrogen diffusion process after a carbonitriding process was also produced for the comparison (comparative example). Then, the nitrogen concentration distribution in the vicinity of the surface layer was investigated for the inner ring produced before the finishing step (S40).

FIG. 11 shows the nitrogen concentration distribution in the depth direction of the produced inner ring. In FIG. 11, the horizontal axis indicates the depth (mm) of the inner ring, and the vertical axis indicates the nitrogen concentration (mass%). In FIG. 11, (A) shows the measurement result of the example, (A ′) shows an approximate curve for the measurement result of the example, (B) shows the measurement result of the comparative example, (B ′) The approximate curve with respect to the measurement result of a comparative example is shown. For example, when the slope of the nitrogen concentration is calculated at two points of a depth of 0.3% by mass and 0.1% by mass ((0.3−0.1) / distance (m)), The slope of the nitrogen concentration was larger than that of the comparative example (more than −15 (1 / m)). Further, when the finishing step (S40) is performed such that the deformation amount of the inner ring by heat treatment is 0.2 mm and the average nitrogen concentration in the surface layer portion is 0.4 mass%, in the comparative example, the variation in the nitrogen concentration in the surface layer portion is 0. It was 0.08 mass% (0.1 mass% or less) in the Example, whereas it was .25 mass%. From this result, it was found that performing the nitrogen diffusion step after the carbonitriding step is effective for reducing variation in the nitrogen concentration in the surface layer portion after finishing.
(Example 3)
Next, the effect of carbonitrides existing in the surface layer on the static load capacity of bearing parts was investigated. When steel containing chromium (Cr) is infiltrated into the steel by carbonitriding or the like, the chromium concentration in the base material decreases and the austenite single-phase region expands. To rise. As a result, when a high concentration carbonitriding process is performed without taking any special measures, carbonitrides are reduced or eliminated even if decarburization does not occur. Here, from the viewpoint of increasing the strength of the bearing component, it is considered preferable to leave the carbonitride and use the precipitation strengthening function of the carbonitride.

In the present embodiment, the value of carbon activity a _c ^* in the carbonitriding process is set to 0.88 or more and 1.27 or less, and carburization is performed earlier than the increase in the carbon solid solubility limit of the nitrogen-enriched layer. Thus, the disappearance of carbonitride is suppressed. An experiment was conducted to confirm the effect of the remaining carbonitride.

FIG. 12 is a cross-sectional SEM (Scanning Electron Microscope) photograph of the test piece when carbonitriding is performed by a conventional method (magnification 5000 times), and FIG. 13 is carbonitrided by the same procedure as in the present embodiment. It is a cross-sectional SEM photograph of the test piece in the case of (a _c ^* = 1) (magnification 5000 times). In the photograph of FIG. 12, carbonitrides have almost disappeared, whereas in the photograph of FIG. 13, there are at least 5 or more carbonitrides having a diameter of 0.3 μm to 0.5 μm per 100 μm ² . .

Next, in order to confirm the effect of the carbonitride, carbonitriding was performed on the test piece under different conditions, and a sample with a hardness of 750 HV was produced while changing the abundance (number density) of the carbide. An experiment was conducted to measure the depth of indentation formed by pressing a ball made of silicon nitride having a diameter (φ) of 9.525 mm on the surface of the sample. The experimental results are shown in FIG. In FIG. 14, the horizontal axis indicates the pressure (GPa) for pressing a silicon nitride ball, and the vertical axis indicates the depth (μm) of the impression formed by pressing the ball. In FIG. 14, the square mark is a sample from which carbonitride has disappeared (Comparative Example), and the diamond mark is a sample in which 5 or more carbonitrides having a diameter of 0.3 μm to 0.5 μm exist per 100 μm ² (Example) ) Shows the measurement results.

As shown in FIG. 14, the depth of the indentation is small in the sample in which 5 or more carbonitrides having a diameter of 0.3 μm or more and 0.5 μm or less exist per 100 μm ² as compared with the sample in which the carbonitride has disappeared. It was confirmed that From this result, in order to improve the static load capacity of bearing parts, it is effective that 5 or more carbonitrides having a diameter of 0.3 μm or more and 0.5 μm or less exist in 100 μm ² in the surface layer portion. I understood.
Example 4
Next, a method for determining a cross-sectional hardness measurement position and a cross-sectional hardness difference reference value for ensuring that the nitrogen concentration at the contact surface of the bearing component is 0.4 mass% or more will be described.

(1) About a test piece and an experimental method (1-1) Introduction First, it is necessary to determine the heating temperature and holding time in the high-temperature tempering having a high correlation with the nitrogen concentration. Here, since transformation by high-temperature tempering is a thermal activation process, increasing the heating temperature and increasing the holding time have the same meaning, and it is not meaningful to make them both variables. It is done. Therefore, in this embodiment, the holding time is fixed (1 hour), and the heating temperature is changed to 300 ° C., 400 ° C., 500 ° C., 600 ° C., and 700 ° C., and the difference in hardness becomes the clearest. The optimum heating temperature was determined by examining the heating temperature.

  In addition, differences in hardenability due to differences in the chemical composition of each material and differences in the cooling rate during quenching affect hardness after quenching, and also affect hardness after high-temperature tempering. It is done. Therefore, in this example, the absolute value of the cross-sectional hardness itself is not used, but the hardness at a deep position (core portion) from the surface layer that is not nitrided (here, the hardness at a depth of 1 mm from the outermost surface after heat treatment, for example) ) And the hardness difference (hardness difference) between the hardness at an arbitrary depth in the nitrided region was adopted as an index. That is, the chemical composition of the material may differ between material lots, and the hardness difference is for offsetting such a difference.

(1-2) Target test pieces Table 1 shows chemical components of the test specimens to be investigated. All the materials were within the above component ranges, and these were subjected to carbonitriding in various heat treatment furnaces and heat treatment atmospheres. The carbonitriding temperature was included in the range of 840 ° C. or higher and 860 ° C. or lower.

  Specifically, for specimen No. 1, the treatment temperature was 850 ° C., the treatment time was 120 minutes (min) (hereinafter referred to as “850 ° C. × 120 min”), and the undecomposed ammonia fraction: 0 The carbonitriding process was performed at 2% by volume and carbon activity: 0.9. For test piece No. 2, carbonitriding was performed at 840 ° C. × 70 min, undecomposed ammonia fraction: 0.1% by volume, and carbon activity: 0.85. For test piece number 3, carbonitriding was performed at 850 ° C. × 120 min, undecomposed ammonia fraction: 0.1% by volume, and carbon activity: 0.9. Further, for specimen No. 4, carbonitriding was performed at 850 ° C. × 90 min, undecomposed ammonia fraction: 0.1 vol%, and carbon activity: 0.9. For test piece No. 5, carbonitriding was performed at 850 ° C. × 90 min, undecomposed ammonia fraction: 0.1% by volume, and carbon activity: 0.9.

  For test piece No. 6, carbonitriding was performed at 850 ° C. × 90 min, undecomposed ammonia fraction: 0.13% by volume, and carbon activity: 0.9. For test piece No. 7, carbonitriding was performed at 850 ° C. × 150 min, undecomposed ammonia fraction: 0.1% by volume, and carbon activity: 0.85. Further, for specimen No. 8, carbonitriding was performed at 850 ° C. × 150 min, undecomposed ammonia fraction: 0.25 volume%, and carbon activity: 0.9. For test piece number 9, carbonitriding was performed at 850 ° C. × 180 min, undecomposed ammonia fraction: 0.3 vol%, and carbon activity: 0.95. For test piece number 10, carbonitriding was performed at 850 ° C. × 90 min, undecomposed ammonia fraction: 0.2% by volume, and carbon activity: 0.9.

(1-3) Nitrogen concentration measurement method In order to investigate the correlation between the cross-sectional hardness of the sample after high-temperature tempering and the nitrogen concentration, it is necessary to measure the nitrogen concentration distribution in the sample (steel). EPMA linear analysis was used to measure the nitrogen concentration in the steel after carbonitriding. The quantification was performed by analyzing a calibration test piece having a known nitrogen concentration and using the calibration curve. A schematic diagram of the sample and measurement method used for EPMA analysis (Electron Probe Micro Analysis) is as shown in FIG.

  As shown in FIG. 15, for example, a case where the inner ring 12 is used as a sample is considered. About the sample, the nitrogen concentration of the sample after carbonitriding was measured. Specifically, a test piece 12A as shown in FIG. 15 is cut out from the sample, and along the direction from the outer peripheral surface 12B to the inner peripheral surface 12C of the test piece, the central portion of the test piece 12A in the height direction ( EPMA line analysis was performed on the cut end face at a position having a half width.

(1-4) Method for Measuring Cross Section Hardness In the test piece 12A described in (1-3) above, the hardness was measured on the cut end face subjected to EPMA analysis. As a measuring method, Vickers hardness measurement was performed using a micro Vickers hardness meter.

(2) Search for holding temperature of high temperature tempering (2-1) Contents of experiment In order to search for a tempering temperature (heating temperature) having a high correlation with the nitrogen concentration, a heating temperature of 180 ° C. was used for 2 hours after carbonitriding. Five types of high-temperature tempering were performed on the test piece 12A subjected to tempering called holding time, with the holding time being 1 hour at each heating temperature of 300 ° C, 400 ° C, 500 ° C, 600 ° C, and 700 ° C. The atmosphere during high temperature tempering was an air atmosphere. And the cross-sectional hardness was measured about the test piece processed by each high temperature tempering conditions. In addition, it measured here about the test piece of the test piece numbers 8 and 9 of the carbonitriding process conditions considered that there is much nitrogen penetration | invasion amount.

(2-2) Experimental results A graph summarizing the experimental results is shown in FIG. The graph shown in FIG. 16 has a tempering temperature (° C.) as the horizontal axis, and a difference in cross-sectional hardness (that is, (maximum value of cross-sectional hardness) − (cross-sectional hardness at a depth of 1 mm from the outermost surface after heat treatment): The result of the experiment is arranged with the vertical axis (also denoted as ΔHV). As can be seen from FIG. 16, the difference ΔHV in the cross-sectional hardness was the largest after high-temperature tempering at a heating temperature of 500 ° C. and a holding time of 1 hour. The difference ΔHV in the cross-sectional hardness when the heating temperature was 500 ° C. was a value approximately twice the difference ΔHV in the cross-sectional hardness after high-temperature tempering at a heating temperature of 300 ° C. or 700 ° C. Therefore, the hardness after tempering, which has a relatively high correlation with the nitrogen concentration, is considered to be the hardness after tempering at a heating temperature of about 500 ° C. For this reason, in the following experiment, the cross-sectional hardness was measured on a test piece after high-temperature tempering with a heating temperature of 500 ° C. and a holding time of 1 hour.

(3) Investigation of relationship between nitrogen concentration and difference in cross-sectional hardness (ΔHV) Here, each test piece having the composition shown in Table 1 was subjected to carbonitriding, and further subjected to a high temperature tempering at a heating temperature of 500 ° C. and a holding time After performing the heat treatment for 1 hour, the nitrogen concentration of the test piece 12A was measured by EPMA analysis as described with reference to FIG. The carbonitriding treatment was performed under the conditions that the heating temperature was 850 ° C. and the carbon activity / undecomposed ammonia fraction (γ) value was 4.75. Moreover, about the said test piece 12A, the cross-sectional hardness in the depth direction was measured in the cut-out end surface shown in FIG. Then, the relationship between the cross-sectional hardness at a certain position in the depth direction and the cross-sectional hardness at a depth position of 1 (mm) from the outermost surface after heat treatment (cross-sectional hardness difference (ΔHV)) was investigated. The results are shown in FIGS.

  17 and 18, the horizontal axis represents the nitrogen concentration (mass%), and the vertical axis represents the cross-sectional hardness difference (ΔHV) (the unit is Vickers hardness). Moreover, FIG. 18 extracts the relationship between the nitrogen concentration and the cross-sectional hardness difference in the range where the nitrogen concentration is 0 to 0.1 mass% from FIG. From FIG. 17, in the range where the nitrogen concentration exceeds 0 and less than 0.1% by mass, the correlation between the nitrogen concentration and the difference in cross-sectional hardness is strong, while in the range where the nitrogen concentration exceeds 0.1% by mass, the nitrogen concentration It was found that the correlation with the difference in cross-sectional hardness was relatively weak. This is probably because incomplete quenching may occur in a region where the nitrogen concentration is high, and nitrogen dissolved in the test piece does not necessarily contribute to a decrease in the martensite decomposition rate. Further, when the correlation coefficient between the nitrogen concentration and the cross-sectional hardness difference is calculated in FIG. 18 in the range where the nitrogen concentration exceeds 0 and is equal to or less than 0.1% by mass, the correlation coefficient between them is as high as 0.8348. For this reason, it is considered that the nitrogen concentration can be predicted from the cross-sectional hardness difference within the range of 0 to 0.1% by mass. Therefore, in the following experiment, the nitrogen concentration is 0.06% by mass and the cross-sectional hardness difference is a substantially intermediate position in a region (0 to 0.1% by mass) in which the nitrogen concentration and the cross-sectional hardness difference have a positive correlation. We decided to use the relationship with 80ΔHV.

(4) Relationship between carbonitriding time and nitrogen concentration distribution In the case of a rolling bearing component, grinding is performed after quenching and tempering to adjust its shape. Therefore, when carbonitriding is performed under certain processing conditions, the nitrogen concentration on the outermost surface of the product (rolling surface or rolling surface) changes due to the machining allowance. For this reason, in order to keep the nitrogen concentration on the outermost surface of the product at 0.4% by mass or more, it is necessary to change the carbonitriding conditions by one-side grinding allowance.

  FIG. 19 shows a treatment time of 4 hours under the conditions that the heating temperature is 850 ° C. and the carbon activity / undecomposed ammonia fraction (γ) is 4.75. A)), 6 hours ((B) in the figure), 8 hours ((C) in the figure), 10 hours ((D) in the figure) nitrogen concentration distribution (high temperature tempering is performed) The previous). The horizontal axis in FIG. 19 indicates the depth (mm) from the surface, and the vertical axis indicates the nitrogen concentration (mass%). Here, when the carbonitriding process is performed under a condition where the value of γ is greater than 5, the nitrogen penetration amount decreases and the region where the nitrogen concentration is high is biased to the surface side. As a result, it becomes practically difficult to set the nitrogen concentration on the product surface to 0.4 mass% or more, except for a method in which the treatment time is very long. Further, when the carbonitriding temperature is 860 ° C. or higher, it is difficult to keep the value of γ at 5 or lower, and when it is 840 ° C. or lower, the diffusion rate of nitrogen into the steel becomes slow. The processing time becomes longer. For this reason, a temperature of about 850 ° C. is appropriate for the carbonitriding treatment of the steel material. In addition, the heating temperature at the time of carbonitriding can be determined by the size of the prior austenite crystal grains after quenching. When the heating temperature is 850 ° C., the size of the prior austenite crystal grains in the above steel material Is in the range of No. 9 to No. 11 in the JIS standard.

  From FIG. 19, when the one-side grinding allowance on the outermost surface of the product is 0.125 (mm), the carbonitriding time is 4 hours, and when it is 0.15 (mm), 6 hours, 0.175 ( mm) for 8 hours, and 0.2 (mm) for 10 hours, the nitrogen concentration on the outermost surface of the product may be 0.4% by mass or more. I understood.

(5) Relationship between Nitrogen Diffusion Treatment and Nitrogen Concentration Distribution It is effective to perform nitrogen diffusion treatment after carbonitriding to prevent the occurrence of incompletely hardened structure and hardness reduction due to excessive amount of retained austenite. . FIG. 20 shows the nitrogen concentration distribution (measured value and calculated value) in the steel after the nitrogen diffusion treatment. In FIG. 20, the horizontal axis indicates the depth (mm) from the surface, and the vertical axis indicates the nitrogen concentration (mass%). In FIG. 20, (A) is a calculated value when the carbonitriding treatment time is 6 hours and the nitrogen diffusion treatment time is 2 hours (the undecomposed NH ₃ concentration is 0.1% by volume). ) Is the calculated value when the carbonitriding treatment time is 6 hours and the nitrogen diffusion treatment time is 1 hour (undecomposed NH ₃ concentration is 0.05% by volume), and (C) is the carbonitriding treatment. Calculated value when the time for nitrogen diffusion treatment is 2 hours (undecomposed NH ₃ concentration is 0.05% by volume), (D) is the time for carbonitriding treatment for 4 hours, nitrogen diffusion The calculated value when the processing time of the processing is 2 hours (the undecomposed NH ₃ concentration is 0.1% by volume) is shown. These calculated values were calculated assuming that the diffusion coefficient of nitrogen was 1.2 × 10 ⁻⁶ (m ² / s). The calculated values shown in (A) to (D) almost coincided with the actually measured values.

Next, FEM analysis was performed by changing the carbonitriding time and the nitrogen diffusion time (carbonitriding time: 4, 5, 6, 7, 8, 9, 10 hours, nitrogen diffusion time: 1, 2 Time), the nitrogen concentration distribution under each treatment condition was calculated. And the regression formula which made the said calculation result the objective variable was computed. Further, nitrogen is diffused into 0.03 mm by the high temperature tempering (heating temperature: 500 ° C., holding time: 1 hour), and grinding allowance (0.1 to 0.2 mm) in finishing after heat treatment In consideration of the above, the following formulas (3) and (4) for determining the measurement position of the cross-sectional hardness difference after the high-temperature tempering were constructed. The following formula (3) shows the measurement position (x ₁ ) of the cross-sectional hardness for ensuring that the nitrogen concentration on the outermost surface of the product is 0.4% by mass or more, and the formula (4) is the outermost surface of the product. The measurement position (x ₂ ) of the cross-sectional hardness for ensuring that the nitrogen concentration is 0.3 mass% or more is shown. In this case, the heating temperature in the nitrogen diffusion treatment was 850 ° C., the undecomposed NH ₃ concentration was 0.06 vol%, and the carbon activity was 0.9.

(6) Quality Assurance Procedure From the examination results of (1) to (5) above, the procedure for assuring that the nitrogen concentration on the outermost surface of the product is 0.4% by mass or more after the heat treatment is as follows. First, calculate the carbonitriding time T _{1 (h),} the measurement position of the cross-sectional hardness after time nitrogen diffusion process T ₂ a _(h) back hot sintering are substituted into the equation ₍₃₎ x ₁ (mm) To do. Next, high temperature tempering is performed at a heating temperature of 500 ° C. and a holding time of 1 hour. Next, a test piece is cut out from the product after high-temperature tempering, the calculated measurement position x ₁ (mm) and the cross-sectional hardness in the non-nitrided inside are measured, and the cross-sectional hardness difference is calculated from the difference between the measured values. To do. And it is discriminate | determined whether the said cross-sectional hardness difference is 80 (DELTA) HV or more. Thereby, if the said cross-sectional hardness difference is 80 (DELTA) HV or more, it can ensure that the nitrogen concentration in the product outermost surface after grinding is 0.4 mass% or more.

When the carbonitriding time T ₁ is 6 hours and the nitrogen diffusion time T ₂ is 2 hours, the difference in cross-sectional hardness at a depth of 0.4 mm is 80 ΔHV or more from the above equation (3). Furthermore, it is guaranteed that the nitrogen concentration on the outermost surface of the product is 0.4% by mass or more. Further, carbonitriding time T ₁ of the treatment is less than 6 hours, also when the time T ₂ of the nitrogen diffusion process is less than 2 hours, similarly evaluated by cross-sectional hardness difference at a depth position of 0.4mm can do.
(Example 5)
The following experiment was conducted for the purpose of obtaining a bearing component that was inexpensive and improved in yield strength and life. First, a steel material within the above component range was prepared, and the steel material was sequentially subjected to carbonitriding, quenching, and tempering treatment, and thereafter subjected to grinding and finishing to produce a bearing part. And the following tests were done in the case where the nitrogen concentration and tempering temperature in the surface layer portion were changed.

  The atmosphere during the carbonitriding treatment was a value of γ of 4.75 and a heating temperature of 850 ° C. When the value of γ is larger than 5, the nitrogen intrusion rate decreases and the region where the nitrogen concentration is high tends to stay on the surface layer, and considering the machining allowance in grinding, the time for carbonitriding becomes very long and is not practical. Absent. In addition, when a steel material within the above component range is used, a large amount of ammonia is required to keep the undecomposed ammonia fraction high at a temperature significantly higher than 850 ° C., thereby increasing the cost of the process. On the other hand, at a temperature significantly lower than 850 ° C., the diffusion rate of nitrogen into the steel becomes slow and the treatment time becomes long. Therefore, it can be said that a temperature around 850 ° C. is appropriate in the carbonitriding treatment of the steel material.

(1) Relationship between the nitrogen concentration and tempering temperature in the surface layer portion and the residual indentation depth First, the effect of the nitrogen concentration and tempering temperature in the surface portion on the residual indentation depth was investigated. First, a flat test piece in which the nitrogen concentration and the tempering temperature in the surface layer portion were changed was produced. Specifically, test pieces having the nitrogen concentration of 0% by mass, 0.1% by mass, 0.25% by mass, and 0.4% by mass were prepared, and 180 ° C., 210 ° C., 240 ° C. for each test piece. And tempering at a temperature of 260 ° C. The residual indentation depth after pressing the ceramic sphere (size: 3/8 inch) against the plane of the test piece with a load having a maximum contact surface pressure of 4.5 GPa (assumed as a complete elastic body) and removing the load. investigated. The value of 4.5 GPa is almost the same value as the maximum value of the maximum contact surface pressure applied to the rolling bearing in the market.

  FIG. 21 shows the results of investigating the relationship between the nitrogen concentration and tempering temperature in the surface layer and the residual indentation depth. In FIG. 21, the horizontal axis represents the nitrogen concentration (mass%), and the vertical axis represents the residual indentation depth (μm). As is clear from FIG. 21, the residual indentation depth was greatly reduced when the tempering temperatures were 240 ° C. and 260 ° C., compared to when the tempering temperatures were 180 ° C. and 210 ° C. Further, when the tempering temperature is 180 ° C. and 210 ° C., the residual indentation depth increases as the nitrogen concentration increases, whereas when the tempering temperature is 240 ° C. and 260 ° C. As the nitrogen concentration increased, the residual indentation depth became smaller (harder to plastic deformation). From this result, in the range of the above experiment (tempering temperature is 180 ° C. or higher and 260 ° C. or lower), the yield strength increases as the tempering temperature increases in the steel material containing nitrogen, and a high static load capacity is obtained. I found out that

(2) Relationship between the nitrogen concentration in the surface layer portion and the indentation origin type peeling life Next, the relationship between the nitrogen concentration in the surface layer portion and the indentation origin type peeling life when subjected to high temperature tempering (240 ° C, 260 ° C) investigated. First, a test piece processed into an inner ring shape of a ball bearing (bearing model number: 6206) was produced. And the artificial indentation of 6 degrees equidistant was formed in the rolling-surface groove bottom part of the said test piece, and the rolling fatigue test was implemented. The artificial indentation was formed by loading a Rockwell indenter with a load of 196N. In the rolling fatigue test, the maximum contact surface pressure was 3.2 GPa, the inner ring rotational speed was 3000 rpm, and the lubricating oil was circulating oil supply of turbine oil VG56.

  In FIG. 22, the result of having investigated about the relationship between the nitrogen concentration in a surface layer part and an indentation origin type | mold peeling life is shown. FIG. 22 is a Weibull plot of an indentation origin type peeling life, where the horizontal axis indicates the life (h) and the vertical axis indicates the cumulative failure probability (%). Further, in FIG. 22, the nitrogen concentration and the tempering temperature are indicated by the display of “nitrogen concentration−tempering temperature”. For example, “0.4 mass% −240 ° C.” indicates that the nitrogen concentration is 0.4 mass% and the tempering temperature is 240 ° C. For reference, the results are also shown when the nitrogen concentration is 0.4 mass% and the tempering temperature is 180 ° C. As is apparent from FIG. 22, when the nitrogen concentration is 0.4 mass% and the tempering temperature is 240 ° C., the results are almost the same as when the nitrogen concentration is 0 mass% and the tempering temperature is 180 ° C. Obtained. However, as the nitrogen concentration decreased, the indentation origin peel life decreased. Therefore, in order to achieve both improvement in yield strength and improvement in life, the tempering temperature is set to a high temperature (240 ° C. and 260 ° C.) as described above, and the nitrogen concentration in the surface layer portion is set to 0.4% by mass or more. It was found that it was necessary to make it higher.

(3) Relationship between the nitrogen concentration and tempering temperature in the surface layer portion and the hydrogen embrittlement peeling life Next, the influence of the nitrogen concentration and tempering temperature in the surface layer portion on the hydrogen resistance in rolling fatigue was investigated. Here, the hydrogen source in rolling fatigue is the lubricant itself or water mixed in the lubricant, which decomposes due to slippage between the contact elements and generates hydrogen, and a part of this hydrogen is in the steel. It is thought to invade.

A rolling fatigue test was performed using a bearing ring of a thrust bearing (bearing model number: 51106) as a test piece. As the operation pattern, the rapid acceleration / deceleration pattern shown in FIG. 23 was used. In FIG. 23, the horizontal axis represents time (sec), and the vertical axis represents the rotation speed (min ⁻¹ ). Further, as shown in FIG. 23, and accelerated to the rotational speed of 2500min ^-1 during 0～0.1Sec, then maintaining the rotational speed between 0.3 sec, 0min ^-1 during the 0.1sec Slow down to The test was conducted by repeating this cycle. A ball made of SUS440C was used, and the number was reduced from 17 (standard number) to 12. As the cage, a resin-made one for 12 equal distribution was prepared, and the maximum contact surface pressure was set to 2.3 GPa. A water-soluble polyglycol oil was used as the lubricating oil, and pure water as a hydrogen source was mixed therein (pure water concentration: 40% by mass). The tester automatically stopped when the raceway ring was separated and the vibration increased.

  Here, it has been confirmed in advance that the effect of pure water, which is a hydrogen source, on the life (hydrogen resistant life) does not change when the pure water concentration is 20% by mass or more. After the test, the proportion of pure water in the lubricating oil is slightly reduced. Therefore, the adequacy of the experiment for evaluating the hydrogen resistance is ensured by measuring the mixing ratio of pure water after the test and confirming that it is 20% by mass or more. In addition, after the said experiment, about 35 mass% pure water remained.

FIG. 24 and Table 2 show the results of investigating the relationship between the surface nitrogen concentration and tempering temperature and the hydrogen embrittlement peeling life. FIG. 24 is a Weibull plot of the hydrogen resistance lifetime, where the horizontal axis indicates the lifetime (h) and the vertical axis indicates the cumulative failure probability (%). Further, in FIG. 24, the nitrogen concentration and the tempering temperature are indicated by the display of “nitrogen concentration−tempering temperature” as in the case of FIG. Table 2 shows the L ₁₀ life (h), L ₅₀ life (h), and Weibull slope values for each heat treatment condition (nitrogen concentration-tempering temperature).

Figure 24 and Table 2, 0 wt% in the case of -180 ° C. while _{L 10} life was 44h is in the case of 0.4 wt% -180 ° C. 138h (3.1 In the case of 0.4 mass% -240 ° C., it is 173 h (3.9 times), and in the case of 0.4 mass% -260 ° C., it is 185 h (4.2 times). The lifespan became longer with the increase of. As explained with reference to the results shown in FIG. 21, this is considered to be due to the fact that plastic deformation becomes difficult as the tempering temperature increases. It is known that hydrogen acts on plastic deformation by facilitating the movement of dislocations, stabilizing atomic vacancies generated by the interaction between dislocations, and causing proliferation. Therefore, it is considered that the life is extended so that plastic deformation is difficult.

  The longest life is 212 h in the case of 0% by mass-180 ° C, 242 h in the case of 0.4% by mass-180 ° C, and 251 h in the case of 0.4% by mass-240 ° C. In the case of 0.4 mass% -260 ° C., it was 266 h, so there was no significant difference in the longest life. On the other hand, in the case of 0% by mass-180 ° C., the life variation is large, and as a result, the L10 life is shortened, whereas 0.4% by mass-180 ° C., 0.4% by mass-240 ° C. and 0% by mass. In the case of .4 mass% -260 ° C., it is considered that all have a stable and long life.

(4) Relationship between tempering temperature and retained austenite (γ) amount Next, the relationship between the tempering temperature and the retained austenite amount was investigated. As described above, the static load capacity and life of the bearing vary depending on the tempering temperature, but it is difficult to obtain the tempering temperature condition directly from the bearing in the product state. However, when the tempering temperature is constant, there is a correlation between the amount of retained austenite at the position where the nitrogen concentration is 0.4% by mass and the tempering temperature. It is possible to clarify.

  FIG. 25 shows the relationship between the tempering temperature and the amount of retained austenite. In FIG. 25, the horizontal axis indicates the tempering temperature (° C.), and the vertical axis indicates the amount of retained austenite (volume%) at the position where the nitrogen concentration is 0.4 mass%. Further, the holding time of the tempering process is constant at 2 h. As shown in FIG. 25, when the tempering temperature is 240 ° C., the amount of retained austenite becomes 8% by volume or less, and when the tempering temperature is 260 ° C., it decreases to 5% by volume or less. It was.

(5) Relationship between area ratio of internal precipitates and tempering temperature Next, the relationship between the area ratio of internal precipitates and the tempering temperature was investigated. As a method of indirectly clarifying the tempering temperature from the product state, there is a method of measuring the area ratio of precipitates in addition to the amount of retained austenite. This is because when the heating temperature during quenching (here, 850 ° C., the prior austenite grains are No. 9 to 11 according to JIS standard) and the holding time during tempering are constant. This is because, as the return temperature increases, carbon dissolved in the matrix precipitates and large cementite (Fe ₃ C) is formed.

  FIG. 26 shows the results of investigating the relationship between the area ratio of precipitates in the internal non-nitrided region and the tempering temperature. In FIG. 26, the horizontal axis indicates the tempering temperature (° C.), and the vertical axis indicates the area ratio (%) of the precipitate. Further, the holding time in the tempering process was fixed at 2 hours. 27 to 30 are photographs of a cross section of the steel material when the tempering temperatures are 180 ° C., 210 ° C., 240 ° C., and 260 ° C., and precipitates in the steel material appear black. FIG. 26 shows the area ratio of precipitates that appear black from the photographs of FIGS. 27 to 30 and shows the relationship with the tempering temperature. FIG. 31 is a photograph of the prior austenite crystal grains (JIS standard 9 to 11) in the internal non-nitrided region when the heating temperature during the quenching process is 850 ° C.

  From FIG. 26, it was found that when the tempering temperature is 240 ° C., the area ratio becomes 11% or more, and when it is 260 ° C., it increases to 12% or more. The reason why the area ratio of the precipitate is determined in the internal non-nitrided region is that the area ratio of the precipitate greatly fluctuates because the carbon solid solubility limit is changed in the nitrided surface layer portion. is there. Moreover, although the said area ratio fluctuates also by carbonitriding temperature and quenching heating temperature, these can be estimated from the average grain size of prior austenite crystal grains. As shown in FIG. 31, the grain size number of the prior austenite crystal grains in the non-nitrided region when the heating temperature was 850 ° C. was 9.5. From the examination of (1) to (5) above, the steel material within the above component range is subjected to carbonitriding treatment and quenching treatment so that the nitrogen concentration on the surface (rolling surface or rolling surface) is 0.4 mass% or more. Further, it has been found that by performing the tempering treatment at a temperature of 240 ° C. or higher, a bearing component that is inexpensive and has improved yield strength and life can be obtained.

  The embodiments and examples disclosed herein are illustrative in all respects and should not be construed as being restrictive. The scope of the present invention is defined by the terms of the claims, rather than the description above, and is intended to include any modifications within the scope and meaning equivalent to the terms of the claims.

  The bearing component and rolling bearing of the present invention can be applied particularly advantageously in bearing components and rolling bearings that are inexpensive and require improved yield strength and life.

DESCRIPTION OF SYMBOLS 1 Deep groove ball bearing, 2 Conical roller bearing, 11, 21 Outer ring, 11A, 21A Outer ring rolling surface, 11B, 12B, 22B Unground surface, 12, 22 Inner ring, 12A, 22A Inner ring rolling surface, 13 balls, 13A, 23A Rolling surface, 14, 24 Cage, 23 rollers, 30 Atmosphere control process, 31 Undecomposed NH ₃ partial pressure control process, 32 H ₂ partial pressure control process, 33 CO / CO ₂ partial pressure control process, 40 Heating pattern Control process.

Claims (6)

0.95 to 1.1 mass% carbon, less than 0.3 mass% silicon, less than 0.5 mass% manganese, less than 0.008 mass% sulfur, and 1.4 mass% A bearing component that is made of steel consisting of the balance iron and impurities, and containing a carbonitriding layer on the surface layer including the contact surface that is in contact with other components. There,
The average nitrogen concentration in the surface layer part is 0.3% by mass or more and 0.6% by mass or less, and the variation in nitrogen concentration in the surface layer part is 0.1% by mass or less,
The amount of retained austenite in the surface layer is 8% by volume or less,
The grain size number of prior austenite grains in the interior of carbonitriding layer is not formed Ri der JIS standard No. 9 or No. 11 or less,
In the approximate curve of the nitrogen concentration distribution in the depth direction of the bearing component, the slope of the nitrogen concentration calculated between two points with a nitrogen concentration of 0.3 mass% and a depth of 0.1 mass% is −15 (1 / M) or more bearing parts.   The bearing component according to claim 1, wherein the amount of retained austenite is 5% by volume or less. Wherein the surface layer portion, a diameter of the carbonitride is 0.3μm or more 0.5μm or less exists five or more per 100 [mu] m ^2, the bearing component according to claim 1 or 2. The bearing component according to any one of claims 1 to 3 , wherein a nitrogen concentration in an unground portion including an unground surface that is a surface other than the contact surface is less than 0.7 mass%. After performing a heat treatment with a heating temperature of 500 ° C. and a holding time of 1 hour, the carbonitriding in the thickness direction of the bearing component is Vickers hardness at a depth of 0.4 (mm) from the contact surface. 80HV or more than the Vickers hardness in the area where the layer is not formed high, bearing component according to any one of claims 1-4. Comprising a bearing component according to any one of claims 1 to 5 the rolling bearing.