Experimental and Numerical Investigations in Mechanical Machining of FibreReinforced Composite Materials
View this Special IssueResearch Article  Open Access
ShaoHsien Chen, ChungAn Yu, "Prediction of Tool Lifetime and Surface Roughness for NickelBased Waspaloy", Advances in Materials Science and Engineering, vol. 2020, Article ID 2013487, 12 pages, 2020. https://doi.org/10.1155/2020/2013487
Prediction of Tool Lifetime and Surface Roughness for NickelBased Waspaloy
Abstract
In recent years, most of nickelbased materials have been used in aircraft engines. Nickelbased materials applied in the aerospace industry are used in a wide range of applications because of their strength and rigidity at high temperature. However, the high temperatures and high strength caused by the nickelbased materials during cutting also reduce the tool lifetime. This research aims to investigate the tool wear and the surface roughness of Waspaloy during cutting with various cutting speeds, feed per tooth, cutting depth, and other cutting parameters. Then, it derives the formula for the tool lifetime based on the experimental results and explores the impacts of these cutting parameters on the cutting of Waspaloy. Since the impacts of cutting speed on the cutting of Waspaloy are most significant in accordance with the experimental results, the highspeed cutting is not recommended. In addition, the actual surface roughness of Waspaloy is worse than the theoretical surface roughness in case of more tool wear. Finally, a set of mathematical models can be established based on these results, in order to predict the surface roughness of Waspaloy cut with a worn tool. The errors between the predictive values and the actual values are 5.122%∼8.646%. If the surface roughness is within the tolerance, the model can be used to predict the residual tool lifetime before the tool is damaged completely. The errors between the predictive values and the actual values are 8.014%∼20.479%.
1. Introduction
In recent years, the development of engine design aims at the applications under high pressure and high temperature, in order to improve the fuel efficiency and to save the related costs. Some parts which adopt stainless steel, aluminum alloys, magnesium alloys, and titanium alloys in the past, such as compressor housings, combustor combustion chambers, and turbine blades, have adopted nickelbased alloys gradually as shown in Figure 1, to meet the requirements of the applications in the special corrosionresistant environments, hightemperature corrosion environments, or the equipment with hightemperature mechanical strength.
Nickelbased alloys are the alloys containing more than 30°wt% nickel, and the nickelbased parts available on the market often contain more than 50°wt% nickel. Nickelbased alloys were researched and developed in the late 1930s and were first produced by the British in 1941. They support high hardness, hightemperature strength, good thermal stability, and corrosion resistance. They support, especially, better hightemperature resistance than lowalloy steel and stainless steel in case the temperature is higher than 650°C. In recent years, they have been widely used in aerospace industry, petrochemical industry and other fields. Among these applications, the aerospace industry supports the highest output value accounting for 33% of the total output value [2, 3].
Hanasaki et al. [4] discovered that the coated tool supports better resistance on the groove wear and the tool wear when cutting a nickelbased alloy with a tungsten carbide tool with a specific coating. They also pointed out that the tool lifetime depends on the tool chipping and the adhesion wear during the lowspeed cutting and depends on the wear caused by the tool temperature increases during the highspeed cutting.
In the research on the cutting Inconel718 alloy with ceramic tools and ceramic tools, Nalbant [5] figured out that carbide tools are more suitable then ceramic tools for cutting Inconel718 alloy. According to the comparison of different cutting speeds, they discovered that ceramic tools are suitable for highspeed cuttings, and carbide tools are suitable for lowspeed cuttings. Moreover, the cutting force is inversely proportional to the cutting speed.
Jawaid et al. [6] explored the cutting performance and the wear resistance of tungsten carbide tools with and without TiN coating on the face milling of Inconel718 alloy.
Zetek et al. [7] cooled down and changed the tool angle with the cutting fluids to cut Inconel718 alloys. The tool lifetime was improved by 35% by improving the tool geometrical shape.
After applying the Tibased and Crbased metal tool coated with diamondlike films to mill aluminum alloys, XH, Wang and Su [8] figured out that the surface roughness is worse than those milled with tools without coating. However, the tool wear is better, and this of Crbased metal tools is better than this of Tibased metal tools.
The thesis on machining mostly issue on tool wear and optimization parameter, this study mainly objects at the simultaneous prediction of tool wear and surface roughness to specifically for the nickelbased alloy Waspaloy.
2. Cutting Principle and Material Property
2.1. Cutting Property of NickelBased Materials
Waspaloy is one of the nickelbased alloys and contains about fifteen alloy elements. Among these elements, the additional aluminum (Al) and chromium (Cr) can improve the hightemperature oxidation resistance, the additional chromium (Cr) and titanium (Ti) can prevent hot corrosion caused by sulfides, and other elements also can provide corresponding features. After the aging treatment, nickelbased alloys will coherently precipitate the fine spherical phase on the base (phase) of the facecentered cubic (FCC) and then generate the coherency strain. The generation of phase affects the hightemperature properties of nickelbased alloys, and more generations cause better hightemperature properties. Moreover, the solidified aluminum (Al) and titanium (Ti) contribute to the generation of the phase, and cobalt (Co) can increase the phase melting temperature and raise the hightemperature strength and stability. Because Waspaloy contains more aluminum (Al) and titanium (Ti), it has more phase, and better hightemperature strength, creep, oxidation, and corrosion resistance. However, it also causes more processing difficulties [9, 10].
The increase of the phase precipitations enhances both the tensile strength and the falling strength of the alloy but reduces the toughness. In addition, the carbon elements contained in the alloy also cause the absolute influences on the properties of the nickelbased alloy. Carbon does not combine with nickel to form carbides, but it can combine with other alloy elements to form intermetallic compounds. The carbides that precipitated from nickelbased alloys are MC, M_{6}C, M_{7}C_{3}, and M_{23}C_{6} as shown in Figure 2. Material scientists discovered that MC (hightemperature tungsten carbide phase) would be precipitated in the form of a mass, which is not beneficial for alloy materials and M_{6}C is often precipitated at the grain boundary in the form of a mass to control the grain size. Moreover, M_{7}C_{3} will be generated in the intervals between crystal grains. If it is discontinuously distributed, it will strengthen the alloy material. On the contrary, if it is precipitated at the grain boundaries, it may cause the embrittlement of the alloy.
The toughness of Waspaloy is relative to the precipitated carbides at the forging deformation grain boundary, the largeangle recrystallization grain boundary, and the deformation twin rather than the size and distribution of phase. At above the phase dissolution temperature (above 1080°C), MC will be autolysis. During the subsequent solid solution process, the MC precipitations result in a twin structure and may generate a carbide film at the grain boundary. The content of major elements in the hightemperature superalloys leads to a great influence on microstructure, structural stability, and final properties. In the production process, the content of major elements in the phase and the carbide may be not the same, and their precipitation quantities, precipitations, and solid solution temperature may also be different. [12, 13].
2.2. Strengthening Mechanism of Waspaloy Superalloy
Nickelbased alloys have good strength and ductility at medium and low temperatures. The strengthening factors come from a combination of various mechanisms, including the solid solution strengthening, the precipitation strengthening, and the grain boundary strengthening as the following summarization [14–16].
2.2.1. AusteniticBase Solid Solution Strengthening
Since the alloy contains about Cr and Mo and the atomic volumes of Cr and Mo are both larger than this of Ni, the substitutional solid solution will be generated when the alloy is solid solubilized in the base. Then, the grain lattice of base will be distorted to generate the strain and the strengthening effect.
2.2.2. Phase Precipitation Strengthening
The precipitation strengthening is relative to the interaction between the precipitation phase and the dislocation. Since the phase is regular and coherent precipitates, the strengthening effect on the precipitates is generally caused by the inversed phase boundary and defect hardening when the dislocation generates precipitates, the proportion of size and the volume of precipitates affects the important factors of the coherency strain.
2.2.3. Grain Boundary Strengthening
It is the strengthening effect caused by the precipitating carbides generated at the grain boundary to block the grain boundary sliding. A small amount of boron (B) segregates the precipitated carbides at the grain boundary and reduces the grain boundary diffusion. Also, the grain size and direction can be controlled to generate the strengthening effect. In case of the higher creep resistance of fine grain at the medium temperature and high stress, the control factor of creep is the dislocation sliding. In case of the higher creep resistance of coarse grain at the high temperature and low stress, the control factor of creep is the dislocation climbing. The main precipitation strengthening mechanism in the nickelbased alloy is . This mechanism and the coherency strain generated in the base support higher strength for the nickelbased alloy at the medium or low temperature environment.
2.3. Cutting Principle
2.3.1. Tool Life and Wear
The experiment method used in this research is face milling. For the tool lifetime predictions and cutting research, the feed per tooth, cutting speed, and depth are the essential cutting parameters. Since a disposable insert of circular is adopted in the cutting process, the feed per tooth and the cutting depth are relative, as shown in Figure 3. Thus, the feed per tooth is calculated as follows [17, 18]:
Generally, the cutting tool lifetime research is divided into qualitative method and quantitative method. The research adopts the quantitative method for the investigations and analysis mainly. In each set of the cutting parameters, the total travel length is 1410 mm. For each 282 mm, the tool wear and the surface roughness are measured for each 282 mm. Therefore, there are 5 values of the tool wear and the surface roughness for each set of the cutting parameters. Based on these measurement results, the tool lifetime for each set of the cutting parameters can be derived at the tool wear VB = 0.3 mm, and then it can be substituted into the formula as follows [19, 20]:
Substitute the known values of the cutting speed, , , and ; the feed per tooth, , , and ; cutting depth, , , and ; and tool lifetime, , , and into the above formula:
Since the previous formula with each set of the cutting parameters can derive a constant value C, it can be derived as follows:
After the further derivations, the cutting parameters, feed per tooth, cutting speed, and depth are proportional and can be presented as follows:
Rewrite the above formula in a matrix as follows:
Based on the previous formula, the variables, n, a, and b and each set of the cutting parameters can be derived and substituted into formula (3) for the constant value C, and then the formula of tool lifttime on the cutting of superalloy, Waspaloy, can be derived finally. Also, the impacts of cutting parameters on the cutting of superalloy, Waspaloy, can be derived based on the formula of tool lifttime.
The machining time required for the tool to reach flank wear, mainly for continuous cutting test of single blade and then the tool wear process, is (1) initial wear rate, (2) uniform wear rate, and (3) accelerating wear rate, for uniform wear is 0.3 mm and nonuniform wear is 0.6 mm (tool life criterion); this study is based on the ISO86881/1994 standard for testing and analysis.
2.3.2. Tool Wear and Surface Roughness
For most of the sets of cutting parameters, the actual surface roughness is less than the theoretical one. The theoretical surface roughness can be defined as the surface roughness under conditions of a complete tool. However, the cutting of a worn tool is a straightline as shown in Figure 4(b) rather than a circular arc as shown in Figure 4(a). Moreover, the surface roughness generated by a worn tool is less than the theoretical one based on Figure 4. Thus, the straightline generated by the tool shape will be impacted by the tool wear as shown in Figure 5. The surface roughness is relative to the feed per tooth in accordance with the surface roughness theory, the feed per tooth in the first set of cutting parameters is 0.3 mm/tooth, and the straightline (C2) caused by the tool wear is much more than the feed per tooth. Therefore, the tool wear and the shape of worn tool may impact the surface roughness in addition to the feed per tooth in this experiment.
(a)
(b)
The tool wear and the surface roughness are relative. Thus, the tool wear straightline is calculated as follows:where VB is the tool wear (mm) and R is the radius of tool (fixed value: 6 mm).
3. Experimental Procedure and Equipment
3.1. Experimental Plan
The research contains the variable factors, resolution, cutting depth, and feed rate and adopts the disposable insert tool coated TiAlN to perform the experiment. Through the generalized formula of tool lifetime and the substitution of a set of cutting parameter into the formula to derive the constant value C, the formula of tool lifttime on the cutting of superalloy, Waspaloy, can be derived finally. Moreover, the relations between surface roughness and the tool wear can be established through the formula of surface roughness, and the impacts of cutting parameters on the cutting of superalloy, Waspaloy, can be derived based on the formula of tool lifttime. This experiment adopts the cutting speed, the feed per tooth, and the cutting depth as the variables in accordance with the recommendations of the tool catalog on the cutting of nickelbased alloy, such that the cutting speed (Vc) is 40∼36.5 (m/min) and the feed per tooth (fz) is 0.28∼0.42 (mm/tooth). The experimental procedure is described in Figure 6 and Table 1.

4. Result and Discussion
4.1. The Relationship between Tool Wear and Time
The cutting experimental results show the tool wear is more with the longer cutting travel length or the cutting time. The tool lifetime aims to explore the relations between the cutting time and tool wear, and this experiment observes the impacts of cutting travel length on the tool wear. Therefore, the travel length can be converted into the cutting time in the following tables and figures. In addition, the feed rate (F) can be derived based on the cutting conditions mentioned. The cutting travel length is directly proportional to the cutting time and inversely proportional to the feed rate.
The cutting parameters adopted in the first experiment for tool wear are the cutting speed (V) = 40 m/min, the feed per tooth (fz) = 0.3 mm/tooth, the cutting depth (ap) = 0.3 mm, and the travel length (L) = 282 mm, 564 mm, 846 mm, 1128 mm, and 1410 mm. As shown in Figure 7, the longer travel length will increase the tool wear. It is caused by the effects of tool usage mainly.
Based on the experimental results, the relations between time and tool wear can be drawn as shown in Figure 7. With the method of least squares, a curve approaching the experimental point can be derived, and the formula of fitting curve can be described as follows:
Through the above formula, at the 0.3 mm of tool wear (i.e., VB = 0.3), the time is 8.108 min. It is the tool lifetime (T) under conditions of the first cutting parameters, where VB is tool wear (mm) and t is the cutting time (min).The cutting parameters adopted in the second experiment for tool wear are the cutting speed (V) = 37.5 m/min, the feed per tooth (fz) = 0.35 mm/tooth, the cutting depth (ap) = 0.25 mm, and the travel length (L) = 282 mm, 564 mm, 846 mm, 1128 mm, and 1410 mm as shown in Figure 8.
Based on the experimental results, the relations between time and tool wear can be drawn as Figure 8. With the method of least squares, a curve approaching the experimental point can be derived, and the formula of fitting curve can be described as follows:
Through the above formula, at the 0.3 mm of tool wear (i.e., VB = 0.3), the time is 8.544 min. It is the tool lifetime (T) under conditions of the second cutting parameters. The cutting parameters adopted in the third experiment for tool wear are the cutting speed (V) = 35 m/min, the feed per tooth (fz) = 0.4 mm/tooth, the cutting depth (ap) = 0.2 mm, and the travel length (L) = 282 mm, 564 mm, 846 mm, 1128 mm, and 1410 mm as shown in Figure 9.
Based on the experimental results, the relations between time and tool wear can be drawn as in Figure 9. With the method of least squares, a curve approaching the experimental point can be derived, and the formula of fitting curve can be described as follows:
Through the above formula, at the 0.3 mm of tool wear (i.e., VB = 0.3), the time is 11.003 min. It is the tool lifetime (T) under conditions of the third cutting parameters. Summarily, the above experimental results can be listed in Table 2.

Substituting all known values into formula (3) and calculating the matrix can derive the results: n = 0.036, a = 0.302, and b = –0.088. Substituting these values into formula (5) can derive the formula as follows:
Substituting the first set of cutting parameters, including the cutting speed (V), feed per tooth (fz), cutting depth (ap), and tool lifetime (T), into the above formula can derive the constant value C = 33.334. Finally, the formula for tool lifetime can be derived as follows:
4.2. Experimental Parameters and Significant Factor Analysis
Based on the formula of tool lifetime, the relations between the cutting speed (V) and the tool lifetime (T) can be derived when the feed per tooth (fz) and the cutting depth (ap) are set to 1. Similarly, the relations between the feed per tooth and the tool lifetime and between the cutting depth and the tool lifetime can also be derived. These procedures can be described as follows [20]:
They are substituted into formula (16):
According to formula (20), will be reduced 27.778 when increases 1. That is, T will be multiplied by when increases 1. Second, will be reduced 8.389 when increases 1. That is, T will be multiplied by when increases 1. Third, will be reduced 2.444 when increases 1. That is, T will be multiplied by when increases 1. Based on these results, the larger slope of the formula leads to more impacts on the tool lifetime. Therefore, the impacts of the cutting speed on the cutting of Waspaloy are larger, and the impacts of the cutting depth are smaller as shown in Figure 10.
4.3. Relations between Tool Wear and Surface Roughness
As the experimental procedure, not only the tool wear but also the surface roughness of Waspaloy is measured when the travel length is 282 mm, 564 mm, 846 mm, 1128 mm, and 1410 mm for each set of the cutting parameters. In addition to the tool wear and surface roughness at each travel length, Table 3 also lists the theoretical surface roughness for further discussion. The derivation of theoretical surface roughness is mentioned in surface roughness theory in (31). However, this theoretical surface roughness is described by the maximum surface roughness (Rmax), and the experiment applies the average surface roughness at the central line (Ra). Thus, the theoretical surface roughness shall be converted through the formula as follows [20]:where Ra is the average surface roughness at the central line and Rmax is the maximum surface roughness.

As shown in Table 3, for most of the sets of cutting parameters, the actual surface roughness is less than the theoretical one. The theoretical surface roughness can be defined as the surface roughness under conditions of a complete tool. For example, the first set of cutting parameters shall present the 0.469 μm of the theoretical surface roughness at the 282 mm of the travel length, and the actual surface roughness is 0.297 μm only. It shall be caused by the tool shape as shown in Figures 4 and 5. Take 0.157 mm of tool wear at 282 mm of travel length for the first set of cutting parameter as an example; that is, VB is 0.157 mm of tool wear in Figure 11. Therefore, a is 0.019 mm and C2 is 0.954 mm.
For the impacts of tool wear on the surface roughness, the relation between the tool wear and the surface roughness can be established based on the data in Table 4. For each set of the cutting parameters, the more tool wear will cause more surface roughness. However, the data at several experimental points is not in compliance with the trend. In addition to the tool wear, these symptoms may be caused by the tool adhesion, the cuttings which are not cleared and adhered on the workpiece surface, or other phenomena influencing the surface roughness of tool during the cutting.

If these experimental points are treated as noise and removed, the relation between tool wear and the surface roughness becomes linear as shown clearly in Figure 11, and the impacts of feed per tooth on the tool wear and surface roughness can be discovered. For each set of the cutting parameters, both of the impacts of cutting speed (V) and the cutting depth (ap) are decreasing, and the impacts of the feed per blade are increasing. Moreover, under conditions of the same tool wear, the increased feed per tooth causes more surface roughness. Therefore, the three fitting curves approaching the experimental curves can be derived through the method of least squares and are shown in Table 4.
4.4. Tool Wear and Surface Roughness to Prediction
The research aims to predict that the surface roughness of workpiece after cutting meets the requirements or not in case of worn tool and how long such tool can be used subsequently. Based on the relations between the tool wear and surface roughness, the tool wear and the feed per tooth cause a certain influence on the surface roughness. Therefore, here assume a formula about the tool wear, the feed per tooth, and the surface roughness as follows [20]:
The unknown values, a, b, and c, in formula (21) can be derived by substituting the results of the tool wear, the feed per tooth, and the surface roughness into formula (22) as follows:
Formula (23) can be described as the following matrix, where the experimental results of tool wear, feed per tooth, and surface roughness are
Solving the above matrix can derive a = 0.248, b = 0.633, and c = 0.067; then substitute these values into formula (22) as follows:
By substituting the experimental results of the feed per tooth and the tool wear into formula (25) and drawing it as shown in Figure 12, it presents a corresponding trend line for each feed per tooth. Therefore, the predictive value of surface roughness after cutting can be derived after measuring the tool wear and substituting the value and the given feed per tooth into formula (25). Also, the predictive value of surface roughness can be used to determine the tool can be used subsequently or not. Table 5 shows the comparison for the experimental predictive surface roughness for each set of the cutting parameters.

4.5. Tool Wear and Cutting Time to Prediction
If the tool can be used in the cutting process subsequently, the next issue is how long the tool can be used subsequently. The cutting time, including the tool lifetime, is relative to the tool wear, and the relation can be presented with a curve. Therefore, a formula of curve can be assumed to describe the relation between the cutting time and the tool wear as follows [20]:
A and B in formula (27) are the factors influencing the formula of curve, and the values of A and B may be not the same under different cutting conditions as the fitting curve formula for each set of the cutting parameters. These results are listed in Table 6.

Since the A and B may be different with the set of cutting parameters, assume the A and B are relative to the cutting speed, the feed per tooth and the cutting depth as follows:
Formula (28) shows the relation of A to the cutting parameters, where a1, b1, and c1 are unknown values and impact on A. A can be derived by the following procedure:
Practicing the logarithm in the above formula can derive the following one:
Substitute the corresponding values of A for each set of the cutting parameters into the above formula (e.g., , , and ):
Then, solving the matrix of the above formula can derive a1 = –5.666, b1 = –10.095, and c1 = –5.207. Then, solving the matrix of the above formula can derive a2 = 5.191, b2 = 10.804, and c2 = 6.639. Finally, substitute the values, a1, a2, b1, b2, c1, and c2, into formulas (28) and (29) to derive the prediction formula as follows:
Summarily, there are two sets of derived formulas. The first set, formula (25), can predict the feasibility of a won tool in the cutting process. The second set, formulas (32)–(34), can predict the residual cutting time of such worn tool. Tables 5 and 6 show the comparison for the experimental predictive cutting time for each set of the cutting parameters. For example, practicing a cutting process with the first set of cutting parameter, the cutting speed (V) = 40 m/min, the feed per tooth (fz) = 0.3 mm/tooth, the cutting depth (ap) = 0.3 mm, and the given tool wear (VB) = 0.157 mm; then the surface roughness and the residual cutting time can be derived as follows.
Substitute the tool wear (VB) and the feed per tooth (fz) into formula (24):
Solving the above formulas can derive the surface roughness (SR) = 0.296 μm at the tool wear (VB) = 0.157 mm. The result can be used to determine the surface roughness processed by the tool meets the requirement or not. If the tool is available, substitute the cutting speed (V) = 40 m/min, the feed per tooth (fz) = 0.3 mm/tooth, and the cutting depth (ap) = 0.3 mm into formulas (33) and (34) and derive the influence factors of the predictive formula of cutting time, A and B:
Substitute the derived A and B into formula (33) to derive the predictive formula of cutting time as follows:
Substitute the tool wear (VB) = 0.157 mm into the above formula to derive the time of the tool used under the given cutting parameters. Assume the tool is unavailable at the tool wear (VB) = 0.3 mm or more. Then, the cutting time at the tool wear (VB) = 0.3 mm can be derived. By subtracting the cutting time at the tool wear (VB) = 0.157 mm from the cutting time at tool wear (VB) = 0.3 mm, the residual time of the tool can be derived as 4.124 (min), as shown in Table 7.

5. Conclusion
(1)Tool wear curve: based on the experiments of the first and the second sets of cutting parameters, the tool wear is significant after the cutting time is more than 9 minutes. Since the tool wear can be divided into three stages, namely, the burst stage, the stable stage, and the damage stage, the significant tool wear is caused that the tool wear has exceeded the stable stage and reached the damage stage.(2)Factors impacting tool lifetime: according to the experimental results, the impacts of the cutting speed on the tool lifetime are the most significant, and the impacts of the cutting depth on the tool lifetime are the least. The experimental results are similar to most of research results. In addition, the impacts of the feed per tooth on the surface roughness are more, followed by the impacts of the tool wear.(3)Comparison of experimental and predicted surface roughness: in the prediction of surface roughness, the maximum error between the actual value and the predicted value for the first set of cutting parameters is 5.799%, this for the second set of cutting parameters is 5.122%, and this of the third set of cutting parameters is 8.375%.(4)Comparison of experimental and predicted cutting time: in the prediction of cutting time, the average magnitude of error between the actual value and the predicted value for the first set of cutting parameters is 12.19%, this for the second set of cutting parameters is 10.4458%, and this of the third set of cutting parameters is 8.014%.
Nomenclature
V:  Cutting speed (m/min) 
VB:  Tool wear (mm) 
Ap:  Cutting depth (mm) 
H:  Cutting thickness (fixed value: 0.1 mm) 
Ci:  Diameter of throwaway tool (fixed value: 12 mm) 
T:  Cutting time (min) 
Fz:  Feed per tooth (mm/tooth) 
SR:  Surface roughness (Ra, μm) 
a1, a2, b1, b2, c1, and c2:  Constant values 
A, B:  Influence factors 
fz_1, fz_2,…,fz_n:  Experimental results of feed per tooth (mm/tooth) 
SR_1, SR_2,…,SR_n:  Experimental results of surface roughness (Ra, μm). 
Data Availability
The raw/processed data required to reproduce these findings cannot be shared at this time as the data also form part of an ongoing study.
Conflicts of Interest
The authors declare that they have no conflicts of interest.
References
 F. Campbell, “Chapter 6superalloys,” in Manufacturing Technology for Aerospace Structural Materials, F. Campbell, Ed., pp. 211–272, Elsevier Science, Oxford, MI, USA, 2006. View at: Google Scholar
 E. O. Ezugwu, Z. M. Wanga, and R. Machado, “The machinability of nickelbased alloys: a review,” Journal of Materials Processing Technology, vol. 86, no. 1–3, pp. 1–16, 1999. View at: Publisher Site  Google Scholar
 R. Polvorosa, A. Suárez, L. N. L. de Lacalle, I. Cerrillo, A. Wretland, and F. Veiga, “Tool wear on nickel alloys with different coolant pressures: comparison of Alloy 718 and Waspaloy,” Journal of Manufacturing Processes, vol. 26, pp. 44–56, 2017. View at: Publisher Site  Google Scholar
 S. Hanasaki, J. Fujiwara, M. Touge, Y. Hasegawa, and K. Uehara, “Tool wear of coated tools when machining a high nickel alloy,” CIRP Annals, vol. 39, no. 1, pp. 77–80, 1990. View at: Publisher Site  Google Scholar
 M. Nalbant, A. Altın, and H. Gökkaya, “The effect of cutting speed and cutting tool geometry on machinability properties of nickelbase Inconel 718 super alloys,” Materials & Design, vol. 28, no. 4, pp. 1334–1338, 2007. View at: Publisher Site  Google Scholar
 A. Jawaid, S. Koksal, and S. Sharif, “Cutting performance and wear characteristics of PVD coated and uncoated carbide tools in face milling Inconel 718 aerospace alloy,” Journal of Materials Processing Technology, vol. 116, no. 1, pp. 2–9, 2001. View at: Publisher Site  Google Scholar
 M. Zetek, I. Česáková, and V. Švarc, “Increasing cutting tool life when machining Inconel 718,” Procedia Engineering, vol. 69, pp. 1115–1124, 2014. View at: Publisher Site  Google Scholar
 S. H. Wang and Y. L. Su, Tribology Potential of DLC Coated Milling Inserts, National Cheng Kung University the Degree of Master, Tainan, Taiwan, 1998.
 C. T. Sims and W. Hagel, The Superalloys, WileyInterscience, New York, NY, USA, 1972.
 H. Bhadeshia, Nickel Based Superalloys, University Of Cambridge, Cambridge, England, 2002.
 H.Y. Bor, A Study on the Elevated Temperature Brittleness and Fracture Mechanism of MarM247 Superalloy, National Chiao Tung University the Degree of Master, Hsinchu, Taiwan, 1998.
 B. H. Kear, J. M. O’blak, and A. F. Giami, “Stacking faults in gamma prime precipitation hardened nickelbase alloys,” Metallurgical Transacions, vol. 1, pp. 2477–2486, 1970. View at: Google Scholar
 C. M. Hong, Z. H. Yao, M. C. Zhang, J. X. Dong, and Y. F. Zhang, “The thermodynamic calculation of Waspaloy alloy carbide and phase precipitation law,” Journal of University of Science and Technology Beijing, vol. 30, no. 9, pp. 1018–1023, 2008. View at: Google Scholar
 A. S. Abdulhakim and A. C. Okafor, “Effects of geometric parameters of wavyedge bullnose helical endmill on cutting force prediction in endmilling of Inconel 718 under MQL cooling strategy,” Journal of Manufacturing Processes, vol. 23, pp. 102–114, 2016. View at: Publisher Site  Google Scholar
 S. H. Chen, “Study on application of grey prediction model in superalloy MAR247 machining,” Advances in Materials Science and Engineering, vol. 2015, Article ID 704143, 10 pages, 2015. View at: Publisher Site  Google Scholar
 S. H. Chen and YuL. Ho, “Lifespan of superalloy Waspaloy cutting tools,” Heliyon, vol. 5, no. 4, Article ID e01388, 2018. View at: Publisher Site  Google Scholar
 P. Nieslony, G. M. Krolczyk, S. Wojciechowski, R. Chudy, K. Zak, and R. W. Maruda, “Surface quality and topographic inspection of variable compliance part after precise turning,” Applied Surface Science, vol. 434, pp. 91–101, 2018. View at: Publisher Site  Google Scholar
 R. W. Maruda, G. M. Krolczyk, S. Wojciechowski, K. Zak, W. Habrat, and P. Nieslony, “Effects of extreme pressure and antiwear additives on surface topography and tool wear during MQCL turning of AISI 1045 steel,” Journal of Mechanical Science and Technology, vol. 32, no. 4, pp. 1585–1591, 2018. View at: Publisher Site  Google Scholar
 S. E. Oraby and D. R. Hayhurst, “Tool life determination based on the measurement of wear and tool force ratio variation,” International Journal of Machine Tools and Manufacture, vol. 44, no. 1213, pp. 1261–1269, 2004. View at: Publisher Site  Google Scholar
 C. A. Yu and S. H. Chen, The Prediction of Tool Life in Milling Waspaloy, NCUT the Degree of Master, Taichung, Taiwan, 2016.
Copyright
Copyright © 2020 ShaoHsien Chen and ChungAn Yu. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.