Interior Fracture Mechanism Analysis and Fatigue Life Prediction of Surface-Hardened Gear Steel under Axial Loading

Abstract

The interior defect-induced fracture of surface-hardened metallic materials in the long life region has become a key issue on engineering design. In the present study, the axial loading test with fully reversed condition was performed to examine the fatigue property of a surface-carburized low alloy gear steel in the long life region. Results show that this steel represents the duplex S-N (stress-number of cycles) characteristics without conventional fatigue limit related to 10⁷ cycles. Fatigue cracks are all originated from the interior inclusions in the matrix region due to the inhabitation effect of carburized layer. The inclusion induced fracture with fisheye occurs in the short life region below 5 × 10⁵ cycles, whereas the inclusion induced fracture with fine granular area (FGA) and fisheye occurs in the long life region beyond 10⁶ cycles. The stress intensity factor range at the front of FGA can be regarded as the threshold value controlling stable growth of interior long crack. The evaluated maximum inclusion size in the effective damage volume of specimen is about 27.29 μm. Considering the size relationships between fisheye and FGA, and inclusion, the developed life prediction method involving crack growth can be acceptable on the basis of the good agreement between the predicted and experimental results.

1. Introduction

Because of the protective effect against surface fatigue fracture, the surface-hardening technology has been extensively employed to enhance the fatigue strength or life of structural materials such as low carbon alloy steels [1]. However, recent studies have shown that the surface-hardening sometimes cannot enhance fatigue performance of structural materials with respect to long life [2,3]. The reason is that there is a change of the fracture mode from the surface fatigue fracture at high stress level to the interior fatigue fracture at low stress level [3,4]. It is because of the transition of fatigue fracture mode or crack nucleation site that some surface-hardened or high-strength structural materials can present peculiar S-N characteristics [5,6] and complicated fracture mechanisms [7,8,9,10].

Surface fatigue fracture of structural materials is very common, which is often induced from irreversible cyclic slip or machining flaws. Moreover, the service environment can degrade the fatigue performance of structural materials and promote the occurrence of surface fatigue fracture. By contrast, interior fatigue fracture is mainly associated with some metallurgical defects of materials such as non-metallic inclusions or pores. For alloy steels, interior inclusion-induced crack nucleation and growth is the most common mode of interior fatigue fracture. Generally, a propagating crack shaped like a fisheye can occur on the fracture surface, and the inclusion is almost located at the center of the fisheye. Furthermore, it should be noted that a characteristic rough area with granular morphology sometimes can occur at the vicinity of the inclusion. This area is named as “fine granular area (FGA)” [5]. Some theories or ideas such as “depressive decohesion of spherical carbide” [6], “hydrogen embrittlement-assisted cracking” [7], “cyclic compression between crack faces” [8], “grain refinement and local stress decreasing” [9], and “numerous cyclic pressing and nanograin formation” [10] have been proposed to explain the formation mechanism of the FGA. Unfortunately, the uniform conclusion about the formation mechanism of the FGA has not yet been drawn. However, researchers all believe that the crack nucleation and growth behaviors within the FGA govern the fatigue properties of alloy steels with respect to long life.

Based on the idea that the crack nucleation is predominant in the long life fatigue process, several models related to dislocation theory [11] were developed to evaluate the crack nucleation life within the FGA, but it is still a difficult task since the crack nucleation mechanism within the FGA is not yet well understood. Conversely, studies [12,13] have shown that fatigue crack still can grow even though the stress intensity factor at the crack tip is below the traditional threshold value controlling long crack growth, and in vacuum the effective crack growth rate of some alloy steels can be reduced to 5 × 10⁻¹³ m/cycle [13]. Moreover, the crack morphology similar to the FGA is observed on the fracture surface of specimens during the crack growth rate testing in vacuum [9]. In view of the fact that the interior crack-induced fatigue fracture takes place in vacuum and the propagating crack can be formed in very few cycles [14], some researchers proposed [15,16] that fatigue life consumed in the FGA formation process could be evaluated from the viewpoint of crack growth.

In this study, the axial loading test was performed to experimentally examine the fatigue property of a surface-hardened gear steel in the long life region. Based on the analysis of S-N characteristics, fracture mechanisms, characteristic crack sizes, and severity of stress distribution around crack tip, a theoretical method of predicting the fatigue strength and life for the surface-hardened steel in its longevity was proposed.

2. Experimental Procedure

2.1. Material and Specimen

The material investigated in this study is a low alloy Cr-Ni steel for drive gear, its main chemical composition (mass percentage) is 0.16 C, 0.37 Si, 0.60 Mn, 0.035 S, 0.035 P, 1.65 Cr, and 3.65 Ni. From the annealed steel bar with a diameter of 16 mm, first specimens were machined into the hourglass-shape with a certain amount of finishing margin, and then grinded in a direction of parallel to the axis of specimen by the grade 600–2000 abrasive paper to the final shape, as shown in Figure 1. The minimum diameter and the round-notched radius of the specimen are 4.5 mm and 60 mm, respectively. The corresponding elastic stress concentration factor, K_t, is about 1.02 based on the book on “stress concentration factors” [17].

2.2. Carburizing and Microstructure

Specimens were placed into a container filled up with carburization powder that is composed of charcoal, calcium carbonate, and barium carbonate with 12:1:5. The container was sealed by fire clay and heated by a vacuum furnace. The furnace temperature first rises up to 800–850 °C, and then is held for 2 h or 4 h soaking time, finally reaching the carburizing temperature of about 930 °C. According to the speed of pack carburizing—about 0.1–0.15 mm/h—the carburizing time is about 8 h and the expected depth of carburized layer is about 0.8–1.2 mm. Upon completion of the process, the furnace temperature is stepped down to 850 °C for 30 min prior to quenching in oil, followed by tempering at 170 °C for 3 h.

After grinding and polishing, then etching with 4% alcohol nitric acid solution, the cross-sectional microstructure of specimen was observed by using the scanning electron microscopy (SEM). The microstructure in carburized layer differs from that in the core region, and the relevant morphologies are shown in Figure 2a,b, respectively. Combined with the analysis of energy dispersive X-ray spectrometer (EDS), the acicular martensites with high carbon and partial residual austenites can be observed in the carburized layer, whereas the lath martensites with low carbon can be observed in the core region. Moreover, some non-metallic inclusions of Al₂O₃ can be found in the microstructure, as shown in Figure 2c.

2.3. Experimental Method

An electromagnetic resonant testing machine (CCQB Testing Co. Ltd., Changchun, China) at frequency of 100 Hz was used to perform the fatigue test of carburized Cr-Ni gear steel under axial loading. Fatigue testing at the constant stress ratio of −1 was performed at room temperature in an open environment. After the experiment, all the fracture surfaces of fractured specimens were carefully observed by the SEM.

3. Results and Discussion

3.1. Micro-Hardness and Residual Stress

By using an instrumented nano-indenter G200 with the measuring function of continuous stiffness, the micro-hardness on cross-sections of specimens was measured. Its distribution is characterized as a function of the depth from surface, ζ, as shown in Figure 3. At the near surface, the value of micro-hardness is the largest, and then tends to decrease. At the ζ-value of no less than about 1200 μm, it reaches a constant value of 613 kgf/mm² that is the micro-hardness of untreated material. Thus, it can be concluded that the depth of the carburized layer is about 1.2 mm.

Based on the sin²ψ method with Cr-Kα radiation, the value of residual stress on the round-notch surface of specimen was measured along the axis of specimen by the TEC 4000 X-ray diffraction system. During testing, the tube voltage is 30 kV and the tube current is 6.7 mA. The maximum compressive residual stress occurs on the surface and is about 268 MPa by averaging the values of four measurement points on the surface.

3.2. S-N Characteristics

The S-N diagram of carburized Cr-Ni gear steel under axial loading is shown in Figure 4. Based on the preliminary SEM observation of fracture surface, especially crack nucleation site, the interior fatigue fracture becomes the predominant fracture mode in the life region of 10⁴–10⁸ cycles. Overall, this carburized steel presents the continuously descending S-N characteristics. The conventional fatigue limit corresponding to 10⁷ cycles cannot be found.

Furthermore, these test data can be divided into two parts based on their distribution characteristics. One part corresponds to the short life region below 5 × 10⁵ cycles, while the other part corresponds to the long life region beyond 10⁶ cycles. Basically, the separation of these two parts of test data is distinct. Therefore, the duplex S-N curves are used to represent the fatigue S-N characteristics of carburized Cr-Ni gear steel under axial loading. In view of the nonlinear distribution feature of each part of test data on semilog coordinates, a Basquin model is used to establish these two S-N curves corresponding to the test data with short life and long life, respectively, plotted by a dashed line and a solid line in Figure 4.

3.3. Fatigue Fracture Mechanism

Based on the SEM observation and the EDS analysis, the interior fracture of specimens is all induced from nonmetallic inclusions in both the short and long timeframes. The fisheye can be observed on the fracture surface, as shown in Figure 5a,c. The inclusion is nearly located at the center of the fisheye. It should be noted that these inclusions are basically confined to the interior matrix region. In other words, the inclusions existing in the carburized layer hardly become crack nuclei due to the effect of the carburized layer. This means that the effective damage zone of a specimen under axial loading is just the interior matrix region.

In the short life region below 5 × 10⁵ cycles, the FGA cannot be observed at the vicinity of the inclusion, as shown in Figure 5b. Conversely, in the long life region beyond 10⁶ cycles, the FGA is observable at the vicinity of the inclusion, as shown in Figure 5c. This is consistent with the other experimental results of alloy steels with interior inclusion-induced fracture in the long life region [5,10,11]. Therefore, it can be confirmed that the formation of FGA is greatly related to the definite fatigue life. Approximately, the number of loading cycles with about 10⁶ is the lowest critical fatigue life for the FGA formation.

In addition, the multiple fisheyes—i.e., multiple interior crack nucleation sites—can be observed on a fracture surface under high stress levels. Figure 5e shows the fracture surface morphology with two fisheyes. For these two fisheyes, fatigue cracks are all originated from the inclusions. With the increasing of loading cycles, two propagating cracks derived from two inclusions can interfere with each other. The interfered cracks can grow along the tangential direction of two fisheyes. In this case, it is concluded that the combined effects of two fisheyes should be responsible for the interior fatigue fracture of this specimen. Therefore, it is summarized that with the decrease of applied stress, the fatigue fracture of carburized Cr-Ni gear steel under axial loading successively represents the multiple inclusion-fisheye induced fracture, the single inclusion-fisheye induced fracture, and the single inclusion-FGA-fisheye induced fracture.

3.4. Crack Size Characteristics

Based on the fractography, several crack size parameters were defined to discuss the interior fracture mechanism. First, the parameter d_inc denotes the depth of inclusion from its center to the nearest edge of fracture surface. By using Imagej software, the measured values of d_inc are in the range of 1216.11–2220.66 μm, as shown in Figure 6. They are almost all larger than the thickness of carburized layer. This further verifies the result of fracture surface observation. That is, the carburized layer can effectively inhibit the crack nucleation from the inclusions contained in itself. Furthermore, it can be seen that the values of d_inc are almost regardless of fatigue life. It is known that, under the axial loading, the stress distribution on the cross-section of specimen is uniform. Thus, combining the results of d_inc, it is concluded that fatigue strength or life should be mainly associated with the sizes of inclusions in the matrix region, instead of the location of inclusions.

On the other hand, in view of the approximately circular shape of the inclusion, FGA, and fisheye, the parameters R_inc, R_FGA, and R_fisheye are used to indicate the radiuses of the inclusion, FGA and fisheye, respectively. The measured values of R_inc, R_FGA and R_fisheye are shown in Figure 7. It can be seen that the values of R_inc are independent on fatigue life. The average value of R_inc is evaluated as 13.49 μm. However, for the values of R_FGA and R_fisheye, they all tend to increase with the increasing of fatigue life. The parameters ρ_fisheye and ρ_FGA were defined to indicate the ratios of R_fisheye to R_inc and R_FGA to R_inc, respectively. Figure 8 shows the relationships between ρ_fisheye and ρ_FGA, and N_f. It can be found that the values of ρ_fisheye and ρ_FGA all tend to increase with the increasing fatigue life, respectively indicated by a dashed curve and a solid curve in Figure 8. The corresponding curve equations are given by:

• For fisheye:

  $$\mathrm{Log}\left({\rho }_{\mathrm{fisheye}}\right)=\mathrm{Log}\left(\frac{R_{\mathrm{fisheye}}}{R_{\mathrm{inc}}}\right)=0.42+0.19\mathrm{Log}\left(N_{\mathrm{f}}\right)$$

  (1)
• For FGA:

  $$\mathrm{Log}\left({\rho }_{\mathrm{FGA}}\right)=\mathrm{Log}\left(\frac{R_{\mathrm{FGA}}}{R_{\mathrm{inc}}}\right)=-0.97+0.19\mathrm{Log}\left(N_{\mathrm{f}}\right)$$

  (2)

3.5. Evaluation of Interior Crack Growth

Studies [18,19,20] have shown that smaller inclusions or defects can be viewed as small cracks, and the propagating crack within the fisheye can be considered to have a circular shape. Therefore, under the stress ratio of −1, the stress intensity factor (SIF) range for an interior circular crack having a radius a, ΔK, can be determined by [20]:

$$\Delta K=\frac{2}{\pi }{\sigma }_a\sqrt{\pi a}$$

(3)

In view of the fact that the tension has a predominant effect on the crack growth behavior but the compression has no significant effect, the value of ΔK in Equation (3) is evaluated by using the stress amplitude instead of the stress range. Moreover, Equation (3) is used with high accuracy even for a circular crack that is not concentric with the axis of the cylindrical specimen and has a radius up to one-half of the radius of the specimen [20]. Thus, the corresponding SIF values for the inclusion, FGA, and fisheye—ΔK_inc, ΔK_FGA, and ΔK_fisheye—can be expressed as:

$$\Delta K_{\mathrm{inc},\mathrm{or}\mathrm{FGA}\mathrm{and}\mathrm{or}\mathrm{fisheye}}=\frac{2}{\pi }{\sigma }_a\sqrt{\pi R_{\mathrm{inc},\mathrm{or}\mathrm{FGA}\mathrm{and}\mathrm{or}\mathrm{fisheye}}}$$

(4)

Based on Equation (4), the evaluated values of ∆K_inc are in the range of 1.99–4.62 MPam^1/2 and tend to increase with the increasing of N_f, as indicated by a solid line in Figure 9. Like S-N data, the values of ∆K_inc also can be divided into two parts based on the difference of fracture mode. One part corresponds to the inclusion-fisheye induced fracture in the short life region below 5 × 10⁵ cycles, and the relevant values of ∆K_inc are in the range of 3.41–4.62 MPam^1/2. Another part corresponds to the inclusion-FGA-fisheye induced fracture in the long life region beyond 10⁶ cycles, and the relevant values of ∆K_inc are smaller and only in the range of 1.99–3.14 MPam^1/2. Moreover, Figure 9 shows the relationship between ∆K_FGA and N_f. The values of ΔK_FGA are scattered in a limited range of 3.52–4.01 MPam^1/2 with an average value of 3.7 MPam^1/2, regardless of fatigue life. It is noted that the values of ΔK_FGA are similar to the partial values of ∆K_inc for the inclusion-fisheye induced fracture, and also similar to the threshold stress intensity factor governing long crack growth for some alloy steels, about 4 MPam^1/2 [5,10,21].

Furthermore, the relationships between ΔK_inc and ΔK_FGA, and inclusion/FGA sizes are established in Figure 10. It is clear that most of the values of ΔK_inc for the inclusion-fisheye induced fracture and most of the values of ΔK_FGA are all regardless of respective inclusion or FGA sizes. However, the values of ΔK_inc for the inclusion-FGA-fisheye induced fracture, shown in the shadow region of Figure 10, obviously tend to increase with the increasing of inclusion sizes. Therefore, ΔK_FGA can approximately be viewed as the threshold value controlling stable growth of interior long crack. This means that even if the inclusion belongs to the category of small crack in size, once its size exceeds the critical size corresponding to ΔK_FGA under a given stress level, the crack induced from this inclusion can directly enter the stable long crack growth stage. Conversely, if the inclusion size is less than the critical size corresponding to ΔK_FGA under a given stress level, the small crack growth can play a key role in the process of interior fracture. The threshold value controlling small crack growth from the inclusion is not a constant, but greatly proportional to inclusion size.

In addition, Figure 9 also shows the relationship between ∆K_fisheye and N_f. The values of ∆K_fisheye are also scattered in a limited range of 17.52–19.92 MPam^1/2 with an average value of 18.5 MPam^1/2, regardless of fatigue life. They are similar to the fatigue fracture roughness of steel. Therefore, ∆K_fisheye can be regarded as the threshold value for controlling unstable long crack growth.

Therefore, from the viewpoint of crack growth, the interior fatigue fracture progress of carburized Cr-Ni gear steel in the long life region beyond 10⁶ cycles can be divided into three stages: (A) the small crack growth from the small inclusion to the FGA, controlled by ∆K_inc; (B) the stable long crack growth from the FGA to the fisheye, controlled by ΔK_FGA, or the stable long crack growth from the large inclusion to the fisheye, controlled by ∆K_inc; (C) the unstable crack growth from the fisheye to the final fracture, controlled by ∆K_fisheye. Among them, stage (C) is extremely short and can be negligible in the total life, whereas stage (A) determines the fatigue property in the long life region beyond 10⁶ cycles.

Firstly, studies [15,16] have shown that for the small crack growth in stage (A), the corresponding crack growth rate, da/dN, can be described by Paris equation, and given by:

$$da/dN=C_{\mathrm{A}}{\left(\Delta K\right)}^{m_{\mathrm{A}}}$$

(5)

where C_A and m_A are the material-independent constants in this stage. Integrating of Equation (5) from the inclusion size, R_inc, to the FGA size, R_FGA, and combining with Equation (4), gives:

$${\left(\frac{2}{\pi }{\sigma }_a\sqrt{\pi R_{\mathrm{inc}}}\right)}^{m_{\mathrm{A}}}\left(\frac{N_{\mathrm{A}}}{R_{\mathrm{inc}}}\right)=\frac{2}{C_{\mathrm{A}}\left(m_{\mathrm{A}}-2\right)}\left[1-{\left(\frac{R_{\mathrm{inc}}}{R_{\mathrm{FGA}}}\right)}^{\frac{m_{\mathrm{A}}}{2}-1}\right]$$

(6)

Since more than 90% of total fatigue life is consumed in stage (A) [5,6], so fatigue life N_A can be approximatly equivalent to the total fatigue life N_f. Combined with the measured sizes of inclusion and FGA, as well as the S-N data in the long life region beyond 10⁶ cycles, the values of C_A and m_A can be evaluated as 1.54 × 10⁻¹⁵ and 6.42, respectivley. Therefore, the interior crack growth rate in stage (A) is obtained as:

$$da/dN=1.54\times {10}^{-15}{ \left(\Delta K\right)}^{6.42}$$

(7)

Next, for the stable long crack growth in stage (B), the corresponding crack growth rate also can be given by:

$$da/dN=C_{\mathrm{B}}{\left(\Delta K\right)}^{m_{\mathrm{B}}}$$

(8)

where C_B and m_B are the material-independent constants in this stage. Because the fatigue life consumed in the process from the FGA to the fisheye cannot be determined, so the crack growth rate in this stage can be approximately evaluated by using the crack growth behavior from the large inclusion to the fisheye in the short life region. Integrating of Equation (8) from the inclusion size, R_inc, to the fisheye size, R_fisheye, and combining with Equation (4), Equation (8) can be rewritten as:

$${\left(\frac{2}{\pi }{\sigma }_a\sqrt{\pi R_{\mathrm{inc}}}\right)}^{m_{\mathrm{B}}}\left(\frac{N_{\mathrm{B}}}{R_{\mathrm{inc}}}\right)=\frac{2}{C_{\mathrm{B}}\left(m_{\mathrm{B}}-2\right)}\left[1-{\left(\frac{R_{\mathrm{inc}}}{R_{\mathrm{fisheye}}}\right)}^{\frac{m_{\mathrm{B}}}{2}-1}\right]$$

(9)

Based on the mearsued sizes of inclusion and fisheye, as well as the S-N data in the short life region below 5 × 10⁵ cycles, the values of C_B and m_B can be evaluatd as 1.21 × 10⁻¹⁵ and 7.72, respectively. Therefore, the interior crack growth rate in stage (B) is obtained as:

$$da/dN=1.21\times {10}^{-15}{ \left(\Delta K\right)}^{7.72}$$

(10)

3.6. Evaluation of Maximum Inclusion and FGA Sizes

The maximum sizes of inclusion and FGA in a given volume of steel, V, were evaluated by using the statistics of extreme values (SEV) method [18]. Taking the inclusion as an example, firstly the inclusions observed from fracture surfaces are viewed as the maximum inclusions in a given set of inspection planes, S₀. Herein, S₀ is defined as the effective damage zone of minimum cross-section of specimen under axial loading—i.e., the interior matrix region, about 3.46 mm².

Then, let X be the dimension of extreme inclusions, and the inclusion sizes are assumed to be well characterized by the Gumbel distribution function, F(x), given by:

$$F\left(x\right)=\exp \{-\exp \{-\left[\right(x-\lambda )/\alpha \left]\right\}\}$$

(11)

where λ and α are location parameter and scale parameter, respectively. The size of ith inclusion, x_i, are classified, starting from the smallest and indexed with i = 1, 2, ···, n, where n denotes the number of inclusion. For the small sample, the cumulative probability corresponding to x_i is given by:

$$P(x_i)=(i-0.3)/(n+0.4)$$

(12)

According to Equations (11) and (12), the following equations are obtained as:

$$x_i=\alpha y_i+\lambda$$

(13)

$$y_i=-\ln \{-\ln [(i-3)/(n+0.4)]\}$$

(14)

The relationship between x_i and y_i is shown in Figure 11, which is described by a solid line with slope α and intercept λ. Based on the least square method, the values of λ and α are evaluated as 12.51 and 2.01, respectively.

Next, the maximum inclusion is expected to be exceeded once in this volume. Let X_V denote the characteristic value of maximum inclusion size, so the return period, T, and the cumulative probability of X_V, P(X_V), are given by:

$$T=V/V_0$$

(15)

$$P(X_V)=1-1/T$$

(16)

where V₀ is the volume of inspection plane with a certain thickness. The thickness is defined as the mean inclusion size, about 13.49 μm, so the value of V₀ is evaluated as about 0.047 mm³. Therefore, the value of X_V for the inclusion can be expressed as:

$$X_V=12.51-2.01\ln [-\ln (1-0.047/V)]$$

(17)

Similarly, for the FGA, the relationship between x_i and y_i is indicated by a dashed line in Figure 11, and the values of λ and α are evaluated as 25.01 and 4.83, respectively. The mean size of FGAs is about 27.45 μm, so the value of V₀ for the FGA is evaluated as about 0.095 mm³. Thus, the value of X_V for the FGA is given by:

$$X_V=25.01-4.83\ln [-\ln (1-0.095/V)]$$

(18)

Figure 12 shows the evaluated maximum sizes of inclusion and FGA as a function of V for carburized Cr-Ni gear steel. Apparently, they all tend to increase with the increasing of V. For the specimen under axial loading, the tested volume V can be expressed as [22]:

$$V=0.25\pi l{q}^2$$

(19)

where q is the diameter of matrix region of minimum cross-section, l is defined as the length at which the stress value on the cross-section is 0.9 times that on minimum cross-section at l/2. For the tested specimen in this study, the values of q and l are 2.1 mm and 21.3 mm, respectively. Based on Equation (19), the value of V is evaluated as about 73.89 mm³. Then, based on Equations (17) and (18), the maximum inclusion and FGA sizes for the specimen in this study are evaluated as about 27.29 μm and 57.15 μm, respectively.

3.7. Prediction of Fatigue Life

Combined with Equations (2) and (6), fatigue strength for the inclusion-FGA-fisheye induced fracture in the long timeframe can be given by:

$${\sigma }_a={\left(\frac{2}{C_{\mathrm{A}}\left(m_{\mathrm{A}}-2\right)}\left[1-{\left({10}^{-0.97+0.19\mathrm{Log}\left(N_{\mathrm{f}}\right)}\right)}^{\frac{m_{\mathrm{A}}}{2}-1}\right]\right)}^{1/m_{\mathrm{A}}}\frac{\sqrt{\pi }}{2}{R}_{\mathrm{inc}}^{\left(2-m_{\mathrm{A}}\right)/2m_{\mathrm{A}}}{N}_{\mathrm{f}}^{-1/m_{\mathrm{A}}}$$

(20)

Combined with Equations (1) and (9), fatigue strength for the inclusion-fisheye induced fracture in a short timeframe can be given by:

$${\sigma }_a={\left(\frac{2}{C_{\mathrm{B}}\left(m_{\mathrm{B}}-2\right)}\left[1-{\left({10}^{0.42+0.19\mathrm{Log}\left(N_{\mathrm{f}}\right)}\right)}^{\frac{m_{\mathrm{B}}}{2}-1}\right]\right)}^{1/m_{\mathrm{B}}}\frac{\sqrt{\pi }}{2}{R}_{\mathrm{inc}}^{\left(2-m_{\mathrm{B}}\right)/2m_{\mathrm{B}}}{N}_{\mathrm{f}}^{-1/m_{\mathrm{B}}}$$

(21)

Therefore, only the values of C_A and m_A or the values of C_B and m_B, as well as the inclusion size, are known, the interior S-N curve corresponding to different fracture mechanisms can be established by using Equations (20) and (21). Based on the mean and maximum inclusion sizes, the predicted interior S-N curves of carburized Cr-Ni gear steel are plotted in Figure 13. The predicted results using the mean inclusion size are in good agreement with experimental data while, by using the maximum inclusion size, effectively indicate the lower boundary of experimental data. In general, the life prediction method involving crack growth for the inclusion-FGA-fisheye induced fracture and the inclusion-fisheye induced fracture can be acceptable. It is noted that the method proposed in this study is mainly based on fatigue fracture mechanisms consisting of inclusion-fisheye induced fracture and inclusion-FGA-fisheye induced fracture. Only if the materials exhibit these fatigue fracture mechanisms, this method can be used to evaluate the relevant fatigue life or strength. Certainly, the applicability of this method still needs to be verified by the experimental results of other materials.

4. Conclusions

Main conclusions obtained in this study are summarized as follows:

(1)

The carburized Cr-Ni gear steel exhibits the constantly decreasing duplex S-N property without the traditional fatigue limit related to 10⁷ cycles.

(2)

Fatigue cracks are all originated from the inclusions limited in the matrix region due to the inhabitation effect of the carburized layer.

(3)

The inclusion-fisheye induced fracture is the main fracture mechanism in the short timeframe, whereas the inclusion-FGA-fisheye induced fracture is the main fracture mechanism in the long timeframe.

(4)

ΔK_FGA can be viewed as the threshold value controlling stable long crack growth, and ∆K_fisheye can be regarded as the threshold value for controlling unstable long crack growth.

(5)

The evaluated maximum sizes of inclusion and FGA in the effective damage volume of specimen are 27.29 μm and 57.15 μm, respectively.

(6)

The proposed life prediction method involving crack growth can be acceptable based on the good agreement between predicted and experimental results.