Characterization of High Temperature Deformation Behavior of BFe10-1-2 Cupronickel Alloy Using Orthogonal Analysis

Jun Cai; Kuaishe Wang; Xiaolu Zhang; Wen Wang

doi:10.1515/htmp-2016-0018

Article Open Access

Characterization of High Temperature Deformation Behavior of BFe10-1-2 Cupronickel Alloy Using Orthogonal Analysis

Jun Cai , Kuaishe Wang , Xiaolu Zhang and Wen Wang

Published/Copyright: September 10, 2016

Published by

Become an author with De Gruyter Brill

Submit Manuscript Author Information Explore this Subject

From the journal High Temperature Materials and Processes Volume 36 Issue 7

Abstract

High temperature deformation behavior of BFe10-1-2 cupronickel alloy was investigated by means of isothermal compression tests in the temperature range of 1,023~1,273 K and strain rate range of 0.001~10 s^–1. Based on orthogonal experiment and variance analysis, the significance of the effects of strain, strain rate and deformation temperature on the flow stress was evaluated. Thereafter, a constitutive equation was developed on the basis of the orthogonal analysis conclusions. Subsequently, standard statistical parameters were introduced to verify the validity of developed constitutive equation. The results indicated that the predicted flow stress values from the constitutive equation could track the experimental data of BFe10-1-2 cupronickel alloy under most deformation conditions.

Keywords: BFe10-1-2 cupronickel alloy; high temperature deformation behavior; orthogonal analysis; constitutive equation

Introduction

With the rapid development of the shipping, nuclear and seawater desalted industry in recent years, the increasing requirement for cupronickels has been proposed [1]. Cupronickel alloys are commonly used as heat exchanger tube materials in the auxiliary coolant system/moderator system owing to their high strength, good thermal conductivity and excellent corrosion resistance [2, 3, 4, 5]. BFe10-1-2 cupronickel alloy is a typical Cu-Ni alloy employed as pipelines, structural materials and ship hulls in marine environments. At present, the main processing methods of BFe10-1-2 cupronickel alloy pipes are semi-solid casting ingots and subsequent hot extrusion, which lead to considerable problems, such as long process time, high energy consumption, low product yield and high cost. Therefore, hot deformation is an important processing step during the manufacture of BFe10-1-2 cupronickel alloy products, affecting the microstructure and consequently the mechanical properties of the deformed material. However, the hot deformation of metallic materials is a complex process [6]. Various physical mechanisms, such as work-hardening, dynamic recovery and dynamic recrystallization, are affected by various influential factors such as the chemical composition of metals and alloys, deformation temperature, strain and strain rate [7]. Understanding the flow behaviors of metals and alloys at hot deformation conditions has a great importance for designers of metal forming processes owing to its effective role on metal flow pattern and the kinetics of metallurgical transformation [8]. Meanwhile, various defects such as fracture, overload and die failure can be often found during high temperature extrusion process for cupronickel alloy pipes. Therefore, a thorough study on high temperature deformation behavior of BFe10-1-2 cupronickel alloy is essential to properly design the thermo-mechanical process parameters. However, few efforts have been done to understand, evaluate and predict the high temperature deformation behavior of this alloy.

The aim of present paper is to investigate the high temperature deformation behavior BFe10-1-2 cupronickel alloy. To achieve this aim, isothermal hot compression tests were conducted at the temperatures of 1,023, 1,073, 1,123, 1,173, 1,223 and 1,273 K, and strain rates of 0.001, 0.01, 0.1, 1, and 10 s^–1. On the basis of orthogonal experiment and variance analysis, the effect of deformation parameters on the flow behavior of BFe10-1-2 cupronickel alloy was analyzed. And a constitutive model amongst strain, strain rate and deformation temperature was developed to predict high temperature flow behavior. Finally, the validity of developed constitutive equation was examined in terms of standard statistical parameters.

Experimental procedure

The chemical composition (wt. %) of BFe10-1-2 cupronickel alloy used in the present investigation is as follows: Ni, 10.80; Mn, 2; Fe, 1.38; and Cu, bal. Furthermore, the original microstructure of as received BFe10-1-2 cupronickel alloy is given in Figure 1 with a typical cast microstructure.

Figure 1:

Original microstructure of as received BFe10-1-2 cupronickel alloy.

Isothermal compression experiments were carried out by a Gleeble-3800 thermal simulator. The cylindrical specimens with 10 mm in diameter and 15 mm in height were machined from a bar. Thereafter, the specimens were heated to the test temperatures at a heating rate of 10℃/s, and then held for 5 min at the compression temperature to secure heat balance prior to deformation. The samples were compressed at temperatures of 1,023, 1,073, 1,123, 1,173, 1,223 and 1,273 K, with strain rates of 0.001, 0.01, 0.1, 1, and 10 s^–1 to the true strain of 0.8. After deformation, the specimens were cooled to room temperature in air, and the strain–stress curves were recorded automatically in isothermal compression. The typical macropicture of the isothermal compression samples before and after tests is shown in Figure 2 .

Figure 2:

Typical appearance on the specimens before isothermal compression tests.

Results and discussion

Flow stress

The flow stress curves at the deformation temperature of 1,073 K and strain rate of 10 s^–1 are given in Figure 3. It can be seen from figure that the flow stress is sensitively dependent on the deformation temperature and strain rate. The flow stress increases with the increase of the strain rate at a curtain temperature, and decreases with the increase of the temperature at a curtain strain rate. At the beginning of deformation stage, the flow stress increases rapidly with the increase of strain, leading to the evident work hardening process. Then, owing to the occurrence of dynamic softening, the rate of work hardening decreases with the increase of strain till a peak stress is reached. Subsequently, the flow stress keeps at a steady level, exhibiting the typical characteristics of dynamic recovery (DRV).

Figure 3:

Flow curves of BFe10-1-2 cupronickel alloy obtained at various deformation conditions (a) 1,073 K, (b) 10 s^–1.

Furthermore, strongly single peak can be observed in flow stress at the strain of 0.05 for low strain rates (0.01 and 0.001 s^–1), as shown in Figure 3(a). The reason for this phenomenon is not very clear. Similar flow stress was reported by Lin [9, 10] in BFe10-1-1 cupronickel alloy at the strain rates of 10 and 20 s^–1, and BFe30-1-1 cupronickel alloy at the strain rate of 20 s^–1. Lin argued that dynamic recrystallization (DRX) lead to the drop of flow stress for BFe10-1-1 cupronickel alloy. As is well known, DRX results in an equiaxed structure [11]. Figure 4 illustrates the microstructures of BFe10-1-2 alloy under the deformation conditions of 1,123 K, 0.01 s^–1. It can be seen from Figure 4 that only deformed flat grains can be observed, but no equiaxed DRX grains can be detected. Meanwhile, similar drops can also be found in 42CrMo steel [12] at the strain rates of 10 s^–1 and 50 s^–1. Further research needs to be done to draw a firm conclusion. Furthermore, the phenomenon of periodic fluctuation can be observed at high strain rate, as can be seen in Figure 3(b). Similar fluctuation was found in Ti-6Al-4V alloy at the strain rate of 10 s^–1 [13], 42CrMo steel in 50 s^–1 [14], and Ti600 titanium alloy in 10 s^–1 [15]. This may attribute to the noise during the compression process.

Figure 4:

Microstructure of BFe10-1-2 cupronickel alloy under the deformation condition of (a) 1,123 K, 10 s^–1.

Orthogonal analysis

In order to analyze the significance of the effect of deformation parameters, i. e. strain, deformation temperature and strain rate, some stress values corresponding to the deformation parameters for BFe10-1-2 cupronickel alloy are introduced to support the orthogonal experiment. The impact factors of test alloy are given in Table 1, and a L₂₅(5⁶) orthogonal table is introduced for experiment arrangement, as shown in Table 2. The values of flow stress corresponding to the relevant deformation conditions are used as objective functions to evaluate the significance of the impact of those factors.

Table 1:

Factors of BFe10-1-2 cupronickel alloy.

Level	Factor
	A	B	C
	Strain	Temperature /K	Strain rate /s^–1
1	0.1	1,023	0.001
2	0.3	1,123	0.01
3	0.5	1,173	0.1
4	0.7	1,223	1
5	0.8	1,273	10

Table 2:

Experimental program of orthogonal analysis.

Test number	Column			Stress(MPa)
	A	B	C
1	1	1	1	49.33
2	1	2	2	47.57
3	1	3	3	42.35
4	1	4	4	55.01
5	1	5	5	57.48
6	2	1	2	85.46
7	2	2	3	63.83
8	2	3	4	77.83
9	2	4	5	81.70
10	2	5	1	21.12
11	3	1	3	110.00
12	3	2	4	75.83
13	3	3	5	105.87
14	3	4	1	27.46
15	3	5	2	32.74
16	4	1	4	143.06
17	4	2	5	113.71
18	4	3	1	34.91
19	4	4	2	40.47
20	4	5	3	44.62
21	5	1	5	173.02
22	5	2	1	54.79
23	5	3	2	48.05
24	5	4	3	50.98
25	5	5	4	50.01
K₁	251.74	560.87	187.61
K₂	329.94	355.73	254.29
K₃	351.9	309.01	311.78
K₄	376.77	255.62	401.74
K₅	376.85	205.97	531.78
k₁	50.348	112.174	37.522
k₂	65.988	71.146	50.858
k₃	70.38	61.802	62.356
k₄	75.354	51.124	80.348
k₅	75.37	41.194	106.356

The range K_i of each factor in Table 2 is employed for variance analysis. The sum of squares of deviations for total experiment SS_T can be expressed as:

(1)SST=∑i=1nσi2−1n∑i=1nσi2

where n is the number of experiment, σ is the flow stress (MPa). And the sum of squares of deviations for each factor SS_j is:

(2)SSj=1r∑i=1rKi2−1n∑i=1nσi2

where r is the repetition of each level, and sum of squares of deviations for error is:

(3)SSerro=SST−SSA−SSB−SSC

The degree of freedom df=r−1, mean value of squares of deviations MS=SSj/dfj, and f-distribution in Mathematic Statistic F=MSj/MSerro. The calculation results of BFe10-1-2 cupronickel alloy via employing variance analysis are depicted in Table 3. From Table 3, it is noted that the values of F for deformation temperature and strain rate are both much higher than F_0.01(4,12), which indicate that the flow stress of BFe10-1-2 cupronickel alloy is extremely sensitive to deformation temperature and strain rate. However, the value of F for strain is a little higher than F_0.05(4,12) but lower than F_0.01(4,12), which indicates that strain has a relatively small effect on the flow stress.

Table 3:

Analysis of variance for BFe10-1-2 cupronickel alloy.

Source	SS	Df	MS	F	Significance
Strain	2,141.97	4	535.491	4.432	low
Temperature	15,008.53	4	3752.131	31.055	high
Strain rate	14,384.78	4	3596.196	29.764	high
Error	1,449.86	12	120.822
Total	32,985.14	24

F_0.01(4, 12)=5.412, F_0.05(4, 12)=3.26.

Influence of deformation parameters on the flow stress

On the basis of orthogonal analysis mentioned above, the influence of strain, strain rate and temperature on the flow stress can be analyzed quantitatively by the mean values of flow stress k_i in Table 2:

(4)ki=Kir

Figure 5 demonstrates the relationship between flow stress and strain. It can be seen the flow stress increases monotonically with the increase of strain, and the rate of flow stress rising decreases with the increase of strain. In theory, the deformation at high temperature is presented as the competing process of work hardening and dynamic softening. At the initial stage, the dislocation density generation is significant with the increase of deformation, resulting in the evident work hardening. Then, the energy of deformation accumulating with the increase of strain is able to stimulate the occurrence of dynamic softening, which can diminish the dislocation density and offset the influence of work hardening [16]. When the work hardening and dynamic softening reach a balance, the dislocation density remains relatively constant, and a saturation flow stress appears.

Figure 5:

Relationship between lnk and lnε.

According to the DRX mechanism during high temperature deformation, the flow stress will show a peak stress due to the occurrence of recrystallization, and then the flow stress will decrease until it reaches a steady stress [17]. However, it is clear that there is no peak stress in Figure 5, indicating only the occurrence of DRV during deformation. Microstructures of BFe10-1-2 alloy under the deformation conditions of 1,123 K, 10 s^–1 and 1,223 K, 0.1 s^–1 are given in Figure 6. As can be seen from the figure, the grains after deformation tend to be elongated perpendicular to the compression direction, but no DRX grains can be observed. Therefore, the main flow softening mechanism for BFe10-1-2 cupronickel alloy is DRV not DRX.

Figure 6:

Microstructure of BFe10-1-2 cupronickel alloy under the deformation condition of (a) 1,123 K, 10 s^–1; (b) 1,223 K, 0.1 s^–1.

The evolution of dislocation density can be regarded as a result of the multiplication and annihilation of dislocations due to work-hardening and DRV respectively, and can be expressed as follows [18]:

(5)dρdε=U−Ωρ

where dρ/dε is the increasing rate of dislocation density ρ with strain ε; U represents the dislocation storage during the deformation; Ωρ represents DRV due to dislocation annihilation and rearrangement, and Ω is the coefficient of DRV. When plastic strain ε=0, dislocation density ρ=ρ0, where ρ0 is the initial dislocation density, and the corresponding flow stress is the initial yield stress σ0. Then the variations in the dislocation density during the hot deformation can be obtained by integrating eq. (5) as [19]:

(6)ρ=UΩ−UΩ−ρ0e−Ωε

Then taking the natural logarithms of both sides of eq. (6), the following expression can be derived:

(7)lnUΩ−ρ=lnUΩ−ρ0−Ωε

Therefore, dislocation density increases with the increase of strain. Meanwhile, the flow stress σ can be introduced in a relationship with dislocation density by Taylor equation [20]:

(8)σ=αGMbρ

where α is the Taylor constant, G is the shear modulus of material, M denotes Taylor factor, and b is the Burgers vector. Therefore, flow stress will increase with the increase of strain. Subsequently, a quadratic equation is use to represent the influence of strain on the mean flow stress (as shown in Figure 5):

(9)lnk=4.34629+0.08235lnε−0.04466(lnε)2

where k is the mean flow stress corresponding to the impact factor strain (Column A in Table 2).

The relationship between deformation temperature, strain rate and dislocation density is expressed as [21]:

(10)ε˙=ρmAexp−ΔG∗cT

where ρm=fρ is the mobile dislocation density, f is about 0.1 representing the proportion of the mobile dislocation density in the total dislocation density ρ. A is a materials constant, and c is the Boltzmann constant. Taking the natural logarithms of both sides of eq. (10), eq. (11) can be derived:

(11)lnρ=lnε˙+ΔG∗/kT+lnAf

It can be found from eq. (11) that the dislocation density increases with the increase of strain rate, and decreases with the increase of deformation temperature. Therefore, from eq. (8), the flow stress increases with the increase of strain rate, and decreases with the increase of deformation temperature, as shown in Figure 7. A linear and a quadratic equation are employed to represent the influence of strain rate and deformation temperature on the mean flow stress respectively (as shown in Figure 7):

(12)lnk=4.4021+0.11036lnε˙

(13)k=1258.342−1.79965T+0.000663353T2

$Figure 7: Relationship between: (a) lnk-lnε˙$\ln \dot \varepsilon $; (b) k-T.$

Figure 7:

Relationship between: (a) lnk-lnε˙; (b) k-T.

Constitutive equation

During hot deformation, constitutive equation of metals can be expressed as:

σ=f(ε,ε˙,T)

The effect of strain, strain rate and temperature on the flow stress can be expressed in another form as [22]:

(14)σ=σ0fεfε˙fT

where σ0 is the initial stress of BFe10-1-2 cupronickel alloy under current experimental conditions; fε, fε˙ and fT are the influence coefficient of the strain, strain rate and temperature, respectively. And eq. (14) is rewritten as:

(15)fεfε˙fT=σσ0

Equations (9), (12) and (13) are used to regress the equations of fε, fε˙ and fT. Table 4 shows the regression of values of fε. The values of k at different strains are calculated from eq. (9). Based on eq. (15), the values of fε at various strain can be obtained from k/k₀, and k₀ is the value of k at the minimum level of each factor (i. e. stain 0.1, strain rate 0.001 s^–1, and temperature 1,023 K in this study), as shown in Table 4.

Table 4:

Regression of fε.

ε	k /MPa	fε=k/k0
0.1	50.446	1
0.2	60.285	1.195028
0.3	65.590	1.300189
0.4	69.017	1.36811
0.5	71.433	1.41602
0.6	73.228	1.451591
0.7	74.607	1.478946
0.8	75.694	1.500472

The relationship between ln(fε) and lnε is shown in Figure 8(a), and a quadratic equation is used to characterize the influence coefficient of the strain fε:

(16)ln(fε)=0.42638+0.08234lnε−0.04466(lnε)2

$Figure 8: Relationship between: (a) ln(fε)$\ln ({f_\varepsilon})$-lnε$\ln \varepsilon $; (b) ln(fε˙)$\ln ({f_{\dot \varepsilon}})$-lnε˙$\ln \dot \varepsilon $; (b) fT${f_T}$-T.$

Figure 8:

Relationship between: (a) ln(fε)-lnε; (b) ln(fε˙)-lnε˙; (b) fT-T.

Then:

(17)fε=exp(0.42638+0.08234lnε−0.04466(lnε)2)

Similarly, the values of fε˙ and fT can be obtained from Tables 5 and 6 respectively.

Table 5:

Regression of fε˙.

⋅ε	k /MPa	fε˙=k/k0
0.001	38.083	1
0.01	49.101	1.289318
0.1	63.306	1.662341
1	81.622	2.143286
10	105.237	2.763376

Table 6:

Regression of fT.

T	k /MPa	fT=k/k0
1,023	111.518	1
1,073	91.055	0.8165
1,123	73.909	0.66275
1,173	60.079	0.53874
1,223	49.566	0.44447
1,273	42.370	0.37994

Figure 8(b) and (c) illustrate the relationship between ln(fε˙)-lnε˙ and fT-T respectively, and equations of fε˙ and fT can be obtained as:

(18)fε˙=2.1433ε˙0.11036

(19)fT=11.28374−0.01614⋅T+5.94838×10−6⋅T2

Flow stress corresponding to the minimum level of all factors in Table 2 should be chosen as the initial stress σ0 (49.33 MPa). Therefore, the developed constitutive model of BFe10-1-2 cupronickel alloy during hot working can be summarized as:

(20){σ=σ0fε˙fTfεσ0=49.33fε=exp(0.42638+0.08234lnε−0.04466(lnε)2)fε˙=2.1433ε˙0.11036fT=11.28374−0.01614⋅T+5.94838×10−6⋅T2

Verification of constitutive equation

The validity of the developed constitutive equation of BFe10-1-2 cupronickel alloy is estimated by comparing the experimental and predicted data, as demonstrated in Figure 9. It can be seen that the predicted flow stress data from the constitutive equation can track the experimental data of BFe10-1-2 cupronickel alloy throughout the entire temperature and strain rate range. Only under some processing conditions (i. e. at 1,023 K, 1,073 K, 1,173 K in 10 s^–1 and 1,123 K, in 1 s^–1), an obvious variation between experimental and computed flow stress data can be observed.

Figure 9:

Comparison between the experimental and predicted flow stress at the temperature of: (a) 1,023 K, (b) 1,073 K, (c) 1,123 K, (d) 1,173 K, (e) 1,223 K, (f) 1,273 K.

The main reason of this variation may be due to the fact that the response of flow behavior of metal materials during high temperature deformation is a highly nonlinear process. Many influencing factors for the flow stress are nonlinear, which reduce the accuracy of the developed constitutive equation [23]. Moreover, temperature rise due to deformation heating at high strain rates may lead to flow softening because the deformation time is too short to allow for heat transfer [24]. The influence of the temperature rise on the flow stress is more significant at lower temperatures, while the influence is relatively weaker at higher temperatures. It should be noted that the flow stress data obtained from hot compression test above 10 s^–1 are not suitable for constitutive analysis unless adiabatic temperature changes are accounted [25]. Mandal [26] reported that a hyperbolic sine constitutive equation could predict the flow stress of Ti-modified austenitic stainless steel throughout the entire temperatures and strain rates range except at low temperature (1,123 K) and high strain rates (10 and 100 s^–1). Yuan [27] et al. proposed a double multiple nonlinear regression constitutive equation for Ti-6Al-4V alloy, significant deviation in prediction were observed at and higher strain rate. Sun et al. [28] established Arrhenius-type and modified Johnson-Cook constitutive equation of Al-0.62Mg-0.73Si Aluminum Alloy, and both of the developed models provide unreliable prediction of flow stress at low temperature and high strain rate. Meanwhile, similar results were also found in modified 9Cr-1Mo steel [29], 7050 aluminum alloy [30], and Fe-23Mn-2Al-0.2C twinning induced plasticity steel [31].

Standard statistical parameters such as correlation coefficient R and average absolute relative error AARE are introduced to quantify the predictability of the developed constitutive equation. These are expressed as [32]:

(21)R=∑i=1N(Ei−Eˉ)(Pi−Pˉ)∑i=1N(Ei−Eˉ)2∑i=1N(Pi−Pˉ)2

(22)AARE(%)=1N∑i=1NEi−PiEi×100

where E is the experimental flow stress and P is the predicted flow stress calculated from the developed constitutive equation considering strain compensation. Eˉ and Pˉ are the mean values of E and P respectively. N is the total number of data used in this study. R is a commonly employed statistical parameter and provides information on the strength of the linear relationship between the experimental and predicted data. AARE is calculated through a term by term comparison of the relative error and therefore is an unbiased statistical parameter for determining the predictability of the equation [32]. As can be seen from Figure 10, the values of R and AARE are found to be 0.9831 and 8.441 % respectively, which indicate that the developed constitutive model can predict the high temperature flow behavior of BFe10-1-2 cupronickel alloy accurately.

Figure 10:

Correlation between the experimental and predicted flow stress data from the developed constitutive equation.

Conclusions

The high temperature deformation behavior of BFe10-1-2 cupronickel alloy have been investigated in terms of compressed tests in a wide range of temperatures (1,023~1,273 K) and strain rates (0.001~10 s^–1). Based on this study, the following conclusions are obtained:

On the basis of the results of orthogonal analysis, it can be found that deformation temperature and strain rate have significant influence on the flow stress of BFe10-1-2 cupronickel alloy, while strain has a relatively small effect on the flow stress.
A constitutive equation based on orthogonal analysis is proposed. The proposed constitutive equation can predict the flow stress accurately under most deformation conditions. The validity of presented constitutive equation is quantified in terms of correlation coefficient (R) and average absolute relative error (AARE). The results of R and AARE are calculated to be 0.983 and 8.441 % respectively, which reflect the good prediction capabilities of the developed constitutive equation.

Funding statement: The authors gratefully acknowledge the financial support received from Planned Scientific Research Project of Education Department of Shaanxi Provincial Government (15JS056); Pre-research Foundation of Jinchuan Company-Xi’an University of Architecture and Technology (YY1501).

References

[1] C.L. Gan, X.F. Liu, H.Y. Huang and J.X. Xie, Mater. Sci. Eng. A, 579 (2013) 202–208.10.1016/j.msea.2013.05.029Search in Google Scholar

[2] Z.M. Yan, X.T. Li, K. Qi, Z.Q. Cao, X.L. Zhang and T.J. Li, Mater. Des., 30 (2011) 2072–2076.10.1016/j.matdes.2008.08.047Search in Google Scholar

[3] J. Mei, X.H. Liu and J.X. Xie, Int. J. Miner. Metall. Mater., 19 (2012) 339–347.10.1007/s12613-012-0561-ySearch in Google Scholar

[4] G.Y. Lin, W. Yang, Y.C. Wan, P.J. Tang, B. Wei, S.H. Zhang. J. Rare Earth., 27 (2009) 259–263.10.1016/S1002-0721(08)60231-8Search in Google Scholar

[5] S. Cincera, S. Barella, M. Bellogini and E. Bresciani, J. Fail. Anal. Prev., 12 (2012) 300–304.10.1007/s11668-012-9565-1Search in Google Scholar

[6] H.Y. Li, Y.H. Li, X.F. Wang, J.J. Liu and Y. Wu, Mater. Des., 49 (2013) 493–501.10.1016/j.matdes.2012.12.083Search in Google Scholar

[7] G.L. Ji, Q. Li and L. Li, Mater. Sci. Eng. A, 615 (2014) 247–254.10.1016/j.msea.2014.07.082Search in Google Scholar

[8] Y.C. Lin and X.M. Chen, Mater. Des., 32 (2011) 1733–1759.10.1016/j.matdes.2010.11.048Search in Google Scholar

[9] G.Y. Lin, J. Zhou, L.P. Sun, Z.F. Zhang and S.H. Zhang, Cailiao Kexue yu Gongyi., 17 (2009) 441–444 (in Chinese).Search in Google Scholar

[10] G.Y. Lin, J. Zhou, Z.F. Zhang, X.Y. Zheng, H. Cai and S.H. Zhang, Hot Working Technol., 36 (2007) 9–12 (in Chinese).Search in Google Scholar

[11] W.X. Yu, M.Q. Li and J. Luo, Rare Metals., 31 (2012) 7–11.10.1007/s12598-012-0452-4Search in Google Scholar

[12] Y.C. Lin, M.S. Chen and J. Zhong, J. Mater. Process. Technol., 205 (2008) 308–315.10.1016/j.jmatprotec.2007.11.113Search in Google Scholar

[13] J. Luo, M.Q. Li, W.X. Yu and H. Li, Mater. Des., 31 (2011) 741–748.10.1016/j.matdes.2009.09.055Search in Google Scholar

[14] Y.C. Lin, M.S. Chen and J. Zhong, Comp. Mater. Sci., 42 (2008) 470–477.10.1016/j.commatsci.2007.08.011Search in Google Scholar

[15] Y. Niu, H.L. Hou, M.Q. Li and Z.Q. Li, Mater. Sci. Eng. A, 492 (2008) 24–28.10.1016/j.msea.2008.02.036Search in Google Scholar

[16] Y. Sun, Z.P. Wan, L.X. Hu and J.S. Ren, Mater. Des., 86 (2015) 922–932.10.1016/j.matdes.2015.07.140Search in Google Scholar

[17] Y.Q. Ning, X. Luo, H.Q. Liang, H.Z.Guo, J.L. Zhang and K. Tan, Mater. Sci. Eng. A, 635 (2015) 77–85.10.1016/j.msea.2015.03.071Search in Google Scholar

[18] Y. Bergstrom, Mater. Sci. Eng. A, 5 (1970) 193–200.10.1016/0025-5416(70)90081-9Search in Google Scholar

[19] G.L. Ji, Q Li, K.Y. Ding, L. Yang and L. Li, J. Alloys Compd., 648 (2015) 397–407.10.1016/j.jallcom.2015.06.264Search in Google Scholar

[20] A. Momeni, G.R. Ebrahimi, M. Jahazi and P. Bocher J. Alloys Compd., 587 (2014) 199–210.10.1016/j.jallcom.2013.10.180Search in Google Scholar

[21] D.K. Shi and W.D. Zhu. Materials Physics, China Machine Press., Beijing (2006).Search in Google Scholar

[22] M.L. Xiao, F.G. Li, W. Zhao and G.L. Yang, Mater. Des., 35 (2012) 184–193.10.1016/j.matdes.2011.09.044Search in Google Scholar

[23] R. Liang and A.S. Khan, Int. J. Plast., 15 (1999) 963–980.10.1016/S0749-6419(99)00021-2Search in Google Scholar

[24] Y.C. Lin. M.S. Chen, and J. Zhong, Mech. Res. Commun., 35 (2008) 142–150.10.1016/j.mechrescom.2007.10.002Search in Google Scholar

[25] F.A. Slooff, J. Zhou, J. Duszczyk and L. Katgerman, Scripta Mater., 57 (2007) 759–762.10.1016/j.scriptamat.2007.06.023Search in Google Scholar

[26] S. Mandal, V. Rakesh, P.V. Sivaprasad, S. Venugopal and K.V. Kasiviswanathan, Mater. Sci. Eng. A, 500 (2009) 114–121.10.1016/j.msea.2008.09.019Search in Google Scholar

[27] Z.W. Yuan, F.G. Li, H.J. Qiao, M.L. Xiao, J. Cai and J. Li, Mater. Sci. Eng. A, 578 (2013) 260–270.10.1016/j.msea.2013.04.091Search in Google Scholar

[28] Y. Sun, W.H. Ye and L.X. Hu, J. Mater. Eng. Perform., 25 (2016) 1621–1630.10.1007/s11665-016-1988-5Search in Google Scholar

[29] D. Samantaray, S. Mandal and A.K. Bhaduri, Comp. Mater. Sci., 47 (2009) 568–576.10.1016/j.commatsci.2009.09.025Search in Google Scholar

[30] B. Wu, M.Q. Li and D.W. Ma, Mater. Sci. Eng. A, 542 (2012) 79–87.10.1016/j.msea.2012.02.035Search in Google Scholar

[31] J.Q. Zhang, H.S. Di, X.Y. Wang, Y. Cao, J.C. Zhang and T.J. Ma, Mater. Des., 44 (2013) 354–364.10.1016/j.matdes.2012.08.004Search in Google Scholar

[32] D. Samantaray, S. Mandal and A.K. Bhaduri, Mater. Des., 31 (2010) 981–998.10.1016/j.matdes.2009.08.012Search in Google Scholar

Received: 2016-1-25

Accepted: 2016-4-25

Published Online: 2016-9-10

Published in Print: 2017-7-26

This article is distributed under the terms of the Creative Commons Attribution Non-Commercial License, which permits unrestricted non-commercial use, distribution, and reproduction in any medium, provided the original work is properly cited.

Articles in the same Issue

https://doi.org/10.1515/htmp-2016-0018

Keywords for this article

BFe10-1-2 cupronickel alloy; high temperature deformation behavior; orthogonal analysis; constitutive equation

Creative Commons

BY-NC-ND 3.0