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Research on the influence of cemented carbide micro-textured structure on tribological properties

  • Zhixiong Tang , Zhenghao Ge EMAIL logo and Jie Li
Published/Copyright: October 22, 2024
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High Temperature Materials and Processes
From the journal High Temperature Materials and Processes Volume 43 Issue 1

Abstract

To examine how micro-textures with distinct structures affect the tribological properties of cemented carbide tool-cutting processes, various micro-textures were meticulously fabricated on YG8 cemented carbide blocks. Subsequently, friction and wear experiments were systematically conducted to examine the microstructure nuances resulting from the diverse structures. The influence of these micro-textures on the friction coefficient of cemented carbide and its underlying factors was comprehensively analyzed. To further investigate the impact of these micro-textures on the cutting force in cemented carbide tools, finite element analysis was conducted. Identical micro-textures used in the tribological experiment were applied to the tool, followed by milling simulations aimed at elucidating the impact of these varied micro-textures on the three-dimensional cutting force exerted by the tool. Empirical investigations and finite element analyses revealed that micro-textures characterized as parallel (parallel to the main cutting edge), perpendicular (perpendicular to the main cutting edge), and a combination of “parallel + perpendicular” significantly enhance the tribological properties of cemented carbide tools. This enhancement is evident in the reduction of both the friction coefficient and cutting force of the tool. Particularly noteworthy is the substantial efficacy of vertical micro-textures in minimizing both the frictional force and cutting force, resulting in a noteworthy reduction of the primary cutting force by more than 60% and a concomitant alleviation of tool feeding force by approximately 25%.

Keywords: micro-textures; tribology; cutting force; friction coefficient

1 Introduction

Cemented carbide stands out as a widely used powder metallurgy material known for its elevated levels of hardness, strength, and wear resistance [1,2]. Due to its exceptional overall performance, it is widely used in various applications such as cutting tools, molds, and bearings [3]. The robust WC phase provides it with remarkable hardness and wear resistance, while the binder phase significantly enhances fracture toughness, albeit with a marginal sacrifice in hardness. However, as increasingly challenging-to-process materials continue to emerge, the incidence of carbide tool failures attributed to friction and wear has become more common [4,5]. Consequently, there is an increased emphasis on advancing friction reduction technologies specific to cemented carbide. Notably, surface modification has emerged as a recent and promising approach to tailor properties better suited for tribological applications [6]. Various surface modification methods have been developed, including ion implantation, electrical discharge machining (EDM) [7], and surface texturing. Among these methods, surface texturing offers a solution for enhancing tribological properties and has attracted widespread attention [8].

The use of surface micro-texturing technology is becoming increasingly prevalent in the field of tribology. Both theoretical simulations and empirical studies support the idea that surface micro-texturing significantly enhances the tribological performance of friction pair surfaces compared to their smooth counterparts [9,10]. This methodology has found extensive applications across various industrial sectors, including mechanical face seals [11], magnetic storage disk surfaces [12], and engine cylinder liners [13,14]. Various surface texturing techniques have been developed, including EDM [15], reactive ion etching (RIE) [16], and laser surface texturing (LST) [17].

In comparison to other micro-texture processing technologies, laser micro-texture processing offers distinct advantages, including high material removal rate, processing flexibility, a limited heat-affected zone, precise controllability, environmental friendliness, and the ability to fabricate surface micro-textures with intricate complexity and precision. These attributes have attracted significant attention [18,19,20]. The functions of surface micro-textures include the collection of wear debris [21], serving as micro-reservoirs for lubricants [22], and augmenting load-carrying capacity under hydrodynamic conditions [23,24].

Xiang et al. [25] investigated the impact of various micro-texture processing technologies on the adhesion and friction properties of diamond BD films. They utilized laser technology to modify the surface micro-textures of carbides, creating different types and depth–diameter ratios, and deposited BD thin films using the HFCVD (hot filament chemical vapor deposition) method. The film’s microstructure was characterized, and both the adhesion strength and friction performance were analyzed. Lian et al. [26,27] employed femtosecond laser processing with five different carbides to explore the impact of carbide variations on micro-texture preparation. They created periodic and uniform nanogratings by scanning carbides with a femtosecond laser. Three experiments were designed to examine the effects of single-pulse energy, scanning speed, and scanning spacing on the periodicity and uniformity of the formed nanogratings. Meng et al. [28] introduced a plasma-assisted laser processing method for creating micro-textures, uncovering the impact of plasma/laser micro-textures on the interface performance of physical vapor deposition (PVD) tool coatings. Yin et al. [29] utilized picosecond ultraviolet laser technology to create three different shapes of micro-textures on the surface of TC4 titanium alloy, aiming to enhance its tribological properties. Through experiments, they confirmed that micro-textures can effectively improve the surface hardness of the titanium alloy. Liu et al. [30] demonstrated, through experiments, that micro-textures can increase the interface contact area, achieve surface modification, promote chemical bonding between CFRP and TC4 at high temperatures, and further improve joint strength. Liu et al. [31] investigated the impact of laser surface micro-textures on the dry friction characteristics of 40Cr at different grinding angles and concluded that micro-textures with a motion angle of 60° had the most significant wear reduction effect. Ye and Hu [32] employed femtosecond laser technology to create three types of micro-textures on the front face of the cutting tool and conducted tests on friction, wear, and cutting performance under lubrication conditions. The results indicated that cemented carbide with narrow grid micro-textures exhibited the highest wear resistance under lubrication conditions. Liu et al. [33] explored the impact of laser composite micro-textures on the tribological properties of GCr15/Si3N4 friction pairs and concluded that laser composite micro-textures can effectively enhance the friction and wear performance of friction pairs under dry friction conditions.

This study focuses on YG8 cemented carbide and creates groove micro-textures with single-group (parallel to each other) and double-group (perpendicular to each other) structures. Friction and wear tests were performed on the prepared micro-textured cemented carbide using a friction and wear testing machine. Specifically, when conducting friction and wear experiments on cemented carbide with a single set of micro-textures, the friction direction includes two forms: parallel to the micro-textures and perpendicular to the micro-textures. Through a series of experimental studies, the anti-friction effects of different forms of micro-textures on the friction and wear behavior of cemented carbide were summarized. Finite element analysis was performed and a micro-textured tool model identical to that used in friction and wear experiments was established. The micro-texture forms include those perpendicular to the main cutting edge, parallel to the main cutting edge, and a combination of being perpendicular and parallel to the main cutting edge, abbreviated as vertical micro-textures, parallel micro-textures, and bidirectional micro-textures. Milling and cutting simulations were performed on the established tool model and how different forms of micro-textures influence cutting forces was analyzed.

2 Experimental procedures

2.1 Materials

The substrate material used in this research was WC + 8 wt% Co cemented carbide with dimensions φ = 20 × 2.5 mm. The composition, physical, and mechanical properties of this cemented carbide are documented in Table 1. The friction counterparts used were GCr15-bearing steel balls with a diameter of 6 mm. The chemical composition and mechanical properties of these GCr15-bearing steel balls are detailed in Tables 2 and 3, respectively [34]. The substrate surfaces were finished by grinding and polishing to a roughness Ra less than 0.05 μm, while the balls had a Ra of about 0.1 μm. All the cemented carbides and balls were washed twice in an ultrasonic washer with alcohol, each time for 15 min. Subsequently, they were dried in a vacuum dryer for about 10 min.

Table 1

Properties of cemented carbide materials

Composition (wt%) Density (g·cm−3) Hardness (GPa) Flexural strength (MPa) Fracture toughness (MPa·m1/2) Impact toughness (J·cm−2)
WC + 8%Co 14.6 16.0 2,320 14.8 2.5
Table 2

Chemical composition of GCr15-bearing steel balls

Chemical composition C Mn Cr Si P S
Content (wt%) 0.95–1.05 0.25–0.45 1.40–1.65 0.15–0.35 ≤0.025 ≤0.025
Table 3

Mechanical properties of GCr15-bearing steel balls

Hardness (HRC) Tensile strength (MPa) Yield strength (MPa) Elongation after fracture (%) Flexural strength (MPa)
25.8 861.3 518.42 27.95 1821.61

The material chosen for the cutting simulation of the workpiece is 6061 aluminum alloy. Table 4 outlines the chemical composition of the 6061 aluminum alloy, and Table 5 presents specific simulation parameters of this alloy [35].

Table 4

Chemical composition of 6061 aluminum alloy

Chemical composition Al Mg Si Cu Cr Fe Ti Zn Mn
Content (wt%) 98 1 0.6 0.28 0.2 0.7 0.15 0.25 0.15
Table 5

Simulation parameters of 6061 aluminum alloy

Density (kg·m−3) Young’s modulus (MPa) Poisson’s ratio Linear expansion coefficient (10−5 °C−1) Specific heat capacity (kg·°C) Thermal conductivity (m·°C)
2,700 70,000 0.22 4.5 220 75.4

2.2 Fabrication of microscale textures

The experiment employed a nanosecond fiber laser marking machine (HGTECH-LG20, Wuhan Huagong Fiber Laser Marking Machine) with an emission wavelength of 1,064 nm, a maximum average power of 20 W, a pulse duration of 200 ns, and a repetition rate that can be continuously adjusted in the range of 30–60 kHz. Figure 1 depicts the schematic diagram of the working optical path of a nanosecond laser and the Gaussian heat source model.

Figure 1 Schematic diagram of the working optical path of a nanosecond laser Gaussian heat source model.
Figure 1

Schematic diagram of the working optical path of a nanosecond laser Gaussian heat source model.

The nanosecond laser parameters for creating micro-textures are as follows: the laser power is 20 W, the laser scanning speed is 100 mm·s−1, and the laser repetition frequency is 30 kHz. Figure 2 depicts the surface morphology of two types of micro-structured cemented carbides captured under a confocal microscope, where panel (a) shows the unidirectional micro-structured cemented carbide three-dimensional shape, panel (b) shows the bidirectional micro-structured cemented carbide three-dimensional shape, panel (c) shows the unidirectional micro-structured cemented carbide two-dimensional shape, and panel (d) shows the bidirectional micro-structured cemented carbide two-dimensional shape.

Figure 2 Surface morphology of two types of micro-structured cemented carbides.
Figure 2

Surface morphology of two types of micro-structured cemented carbides.

As shown in Figure 2, the depth of the grooves on the surface of cemented carbide with dual-group micro-textures is significantly greater than that of cemented carbide with single-group micro-textures. The main reason for this result is that the laser repeatedly scans the same position.

2.3 Friction and wear experiment

The friction experimental equipment used is an MSR-2T electrochemical reciprocating friction and wear testing machine produced by Lanzhou Zhongke Kaihua Technology Development Co., Ltd. The test load range of this device is 10–50 N, the frequency of reciprocating sliding can be adjusted within the range of 0.1–45 Hz, and the length of reciprocating sliding can be adjusted within the range of 0.5–25 mm. The measurement accuracy of its friction coefficient can reach 0.2% F.S. The specific parameters of the friction experiment are as follows: the load is 5 N, the test time is 60 min, the running speed is 120 mm·s−1, the reciprocating running length is 5 mm, the scanning length is 2 mm, and the sampling frequency is 2 Hz. Figure 3 illustrates the friction experimental setup.

Figure 3 Friction experimental setup.
Figure 3

Friction experimental setup.

To specifically characterize the impact of LST on friction and wear, the wear volume loss of the surface balls was used to evaluate the wear resistance of different textures under varying lubrication conditions. The volume loss of the wear ball was calculated by measuring the diameter of the worn surface. Figure 4 illustrates the shape and parameters of the worn steel ball. The amount of ball loss can be expressed as [36]:

(1) v = π 3 ( R − R 2 − r 2 ) 2 ( R 2 − r 2 + 2 R ) .

Figure 4 Shape and parameters of the worn steel ball.
Figure 4

Shape and parameters of the worn steel ball.

2.4 Cutting simulation

This article utilizes AdvantEdge finite element analysis software to simulate the milling process of aluminum alloy and analyze the influence of micro-texture types on cutting force. The simulation specifically employs the Johnson–Cook constitutive model [37].

(2) σ = ( A ̇ + B ε p n ) 1 + C ln ε ̇ ε ̇ 0 1 − T ̇ − T 0 T melt − T 0 m .

In the equation, A ̇ is the initial yield stress of the material, in MPa; B is the strain hardening index of the material, in MPa; n is the cutting hardening index of the material; ε is the equivalent elastic strain; C is the characteristic coefficient of the material; m is the thermal softening coefficient of the material; ε ̇ is the equivalent elastic strain rate, in s−1; ε ̇ 0 is the reference equivalent elastic strain rate, in s−1; T ̇ is the deformation temperature of the workpiece, in °C; T 0 is the room temperature, in °C; and T melt is the melting temperature of the workpiece, in °C.

The Johnson–Cook constitutive model for 6061 aluminum alloy is crucial for achieving accurate cutting simulation, and Table 6 presents some of the Johnson–Cook constitutive parameters [38].

Table 6

Johnson–Cook constitutive parameters of 6061 aluminum alloy

A B C n m T melt (°C) T 0 (°C)
272 572 0.83 0.2 1 660 20

In the cutting simulation process, it is essential to establish cutting separation criteria based on attributes for material removal. For metal materials, the Johnson–Cook shear failure criterion and its corresponding parameters are employed. The definition of ω is as follows:

(3) ω = ∑ Δ ε ¯ P 1 ε ¯ P 1 ,

(4) ε ¯ P 1 = d 1 + d 2 exp d 3 p q ⋅ 1 + d 4 ln ε ¯ ̇ P 1 ε ̇ 0 [ 1 + d 5 θ ˆ ] .

In the equation, Δ ε ̅ P 1 is the equivalent plastic strain increment; ε ̅ P 1 is the failure strain; ε ̅ ̇ P 1 is the plastic strain rate; d 1–d 5 are shear failure parameters. The shear failure parameters corresponding to 6061 aluminum alloy are shown in Table 7 [38].

Table 7

6061 Shear failure parameters of aluminum alloy

d 1 d 2 d 3 d 4 d 5
0.071 1.248 −1.142 0.147 0

The tool model is a face milling cutter with four teeth, featuring a cutting edge length of 3 mm, a rake angle of 5°, a main deviation angle of 80°, a tool rotation diameter of 12.5 mm, a feed rate of 0.15 mm·r−1, a milling speed of 20,000 rpm, and a back feed of 1 mm. The size of the workpiece is 20 mm × 5 mm × 2 mm. As shown in Figure 5, the stress cloud map (a) and temperature cloud map (b) of the simulation results are presented. To correlate finite element analysis with tribological experiments, three types of micro-textures, namely, perpendicular to the main cutting edge, parallel to the main cutting edge, and “perpendicular to the main ‘cutting + parallel’ to the main cutting edge,” were applied on the rake face of the cutting tooth.

Figure 5 Stress and temperature clouds of simulation results.
Figure 5

Stress and temperature clouds of simulation results.

3 Results and discussion

3.1 Dry friction test results

By comparing the data from ball disc friction and wear testing machines, it is evident that under dry friction conditions, the texture parameters will affect the friction coefficient. Figure 6 illustrates the results of the dry friction experiment. Among them, Figure 6(a) displays the variation curve of the friction coefficient, and Figure 6(b) presents the histogram of the average friction coefficient. Terms a, b, c, and d represent the average friction coefficient when there is no micro-texture, when the direction of motion is perpendicular to the unidirectional micro-textures, when the direction of motion is parallel to the unidirectional micro-textures, and when the micro-texture is bidirectional, respectively.

Figure 6 Results of the dry friction experiment.
Figure 6

Results of the dry friction experiment.

The results of friction experiments indicate that hard alloys with micro-textures oriented in three ways – perpendicular to, parallel to, and bidirectional to the friction direction – exhibit lower friction coefficients than hard alloys without prepared micro-textures. This finding suggests that these micro-textures can effectively reduce the friction coefficients of hard alloys to some extent.

The presence of micro-textures primarily reduces the friction coefficient of cemented carbide for several reasons: (1) Micro-textures on the surface of these carbides provide a lubricating effect, diminishing direct contact between surfaces. These structures can adsorb lubricants and form a lubricating film, reducing dry friction, similar to the effect of lubricants without external additions. (2) Micro-structures in micro-textured cemented carbide disperse local stress, preventing stress concentration. This minimizes local wear and, consequently, reduces friction. Small structure design controls local stress distribution. (3) Micro-structures on the micro-textured hard alloy increase the effective surface area, diminishing actual contact points between surfaces and thus reducing dry friction. Geometric shape and size of micro-textures can be adjusted for this purpose. (4) The surface structure of micro-textured cemented carbide can exhibit a self-cleaning effect, removing impurities or wear particles, maintaining a clean surface, and reducing friction. (5) Micro-structures in micro-textured cemented carbide can induce local oscillations and gas film effects, further reducing dry friction by generating small oscillations and isolation layers on the friction surface, minimizing direct contact.

Among these, cemented carbide blocks with micro-textures parallel to the reciprocating friction direction have the smallest friction coefficient, followed by those with micro-textures perpendicular to the reciprocating friction direction. Cemented carbide blocks with two sets of micro-textures exhibit the highest friction coefficient. The smaller friction coefficient in the parallel direction is attributed to the following: (1) micro-structures facilitating lubricant flow and forming a gas film on the friction surface, reducing material contact and friction coefficient along micro-textured grooves. The gas film effect is more pronounced in this direction. (2) Micro-structures disperse local stress on the friction surface, preventing stress concentration and reducing friction along micro-textured grooves. (3) Friction experiments perpendicular to the micro-texture direction result in a severe furrow effect, causing additional friction due to overcoming adhesion and cohesion between materials. Two sets of perpendicular micro-textures not only exhibit furrowing effects but also may lead to increased wear due to susceptibility to cutting or scraping during frictional motion. This increases material contact and friction coefficient. Additionally, the uneven local stress distribution from vertical micro-textures may generate higher stresses, increasing friction. Hence, two sets of micro-textures perpendicular to each other have the highest friction coefficient.

3.2 Ball wear results

Figure 7 illustrates the wear surface morphology of balls after wear under identical friction conditions. In the figure, panel (a) shows the ball used in the friction experiment with cemented carbide featuring micro-textures aligned perpendicular to the friction direction, panel (b) displays the ball used in the friction experiment with cemented carbide featuring micro-textures aligned parallel to the friction direction, panel (c) presents the ball used in friction experiments with bidirectional micro-textures on cemented carbide, while panel (d) demonstrates the ball used in friction experiments with cemented carbide without micro-textures.

Figure 7 Surface wear morphology of the balls.
Figure 7

Surface wear morphology of the balls.

Figure 7(b) depicts distinctive surface scratches on the ball subjected to reciprocating friction parallel to the micro-texture direction. This phenomenon is attributed to the sharp edges of the micro-texture grooves. As the friction ball traverses these sharp edges, it undergoes scraping and scratching, resulting in visible surface marks. Figure 8 visually represents the ball’s wear, featuring a bar chart illustrating the wear volume. In this chart, A, B, C, and D denote the wear volumes of the friction balls used in experiments with the hard alloy friction perpendicular to the micro-texture direction, parallel to the micro-texture direction, along bidirectional micro-textures, and without micro-textures, respectively.

Figure 8 Wear volume of the balls.
Figure 8

Wear volume of the balls.

The wear volume observed in the three cemented carbide friction and wear experiments featuring micro-textures exceeds that of the hard alloy friction and wear experiment conducted without micro-textures. Notably, the ball wear in the test involving cemented carbide with double-sided micro-textures is particularly severe, exhibiting a wear volume approximately nine times greater than that of the ball employed in the friction and wear experiment with no micro-textures in the cemented carbide. The wear volume of the ball oriented perpendicular to the micro-texture direction is slightly lower, with a wear volume approximately eight times that of the ball used in the friction and wear experiment involving no micro-textures in the cemented carbide. Conversely, the ball oriented parallel to the micro-texture direction demonstrates the lowest wear volume, approximately five times less than that of the ball used in the friction and wear experiment with no micro-textures in the cemented carbide. The observed phenomenon can be attributed to the following main factors: First, the edges of the texture are notably sharp. As the friction ball moves across these sharp edges, it induces scraping on the surface of the friction ball. Consequently, the hard alloy with micro-textures is more prone to causing wear on the ball. Second, for balls oriented in the same direction as the micro-textures, there is scraping or localized shearing, contributing to increased wear. Thus, the wear on balls oriented perpendicular to the micro-texture direction is more pronounced than that on balls oriented parallel to the micro-texture direction. Finally, bidirectional texturing results in the cumulative effect of wear in both parallel and perpendicular directions, leading to maximum wear on the balls in contact with bidirectional micro-textures.

3.3 Cutting simulation results

Figure 9 presents the output result of the three-way cutting force after solving. Figure 9(a) displays the original output result curve of the cutting force, and Figure 9(b) shows the smoothed curve after the filter is activated. From top to bottom, the main cutting force, feed force, and cutting resistance are shown sequentially. Panels a, b, c, and d represent the simulation result curves of non-textured tools, parallel micro-textured tools, vertical micro-textured tools, and bidirectional micro-textured tools.

Figure 9 Cutting simulation cutting force output result curve. (a) Before filtering operation. (b) After filtering operation.
Figure 9

Cutting simulation cutting force output result curve. (a) Before filtering operation. (b) After filtering operation.

As depicted in the figure, the three different forms of micro-textures exhibit a consistent impact on the three-dimensional cutting force of the tool. They significantly reduce the main cutting force and cutting resistance, with no apparent influence on the feed force, and a slight increase in the feed force may occur. Moreover, these micro-textures notably reduce the main cutting force by over 60% and cut the resistance by about 25%. When comparing the three forms of micro-textures, vertical and bidirectional micro-textures demonstrate nearly equal effectiveness in reducing the main cutting force, surpassing the impact of parallel micro-textures. Vertical micro-textures are most effective in reducing tool cutting resistance, while bidirectional micro-textures show the least effect. Consequently, vertical micro-textures have the most pronounced impact on reducing tool friction, while bidirectional micro-textures have the least effect. The cutting simulation results align with the friction experimental outcomes.

3.4 Analysis of micro texture friction reduction mechanism

Based on the above experimental research, it can be concluded that introducing micro-textured grooves in cemented carbide achieves friction reduction effects. The friction reduction mechanism primarily includes the following aspects.

First, micro-textured grooves can reduce the actual contact surface area between objects, decreasing the contact area by increasing the “virtual position” of the surface. This reduction minimizes contact resistance and wear during dry friction, significantly mitigating the adhesion and wear typical of traditional planar friction.

Second, micro-textured grooves create a gas cushion effect during dry friction. As air compresses in the grooves during the friction process, a layer of gas cushion forms, diminishing direct contact between the friction surfaces and reducing friction and wear.

Concurrently, these grooves establish a soft deformation layer, lowering the surface contact pressure. This deformation layer acts as a buffer zone, decreasing the contact force between objects and, consequently, reducing friction and wear.

Finally, micro-textures can inhibit the formation of abrasive particles. Illustrated in Figure 10 is a schematic of the friction and wear mechanism. During the friction process, small abrasive particles may enter the grooves, avoiding rolling and scraping on the friction surface. This mechanism lessens damage and wear caused by abrasive particles, extending the lifespan of friction components.

Figure 10 Schematic diagram of the friction and wear mechanism.
Figure 10

Schematic diagram of the friction and wear mechanism.

4 Conclusions

Through the integration of experimental research and finite element simulation, this study investigated the impact of various micro-texture configurations on the tribological and cutting characteristics of cemented carbide. The following key findings were derived:

  1. Micro-textures aligned parallel to the reciprocating friction direction, those oriented perpendicular to this direction, and bidirectional micro-textures contribute to enhancing the tribological performance of hard alloy tools, thereby reducing the three-dimensional cutting force during the cutting process.

  2. Among the three micro-texture configurations scrutinized in this study, those perpendicular to the reciprocating friction direction exert the most substantial impact on diminishing tool friction and cutting force, whereas bidirectional micro-textures exhibit the least influence.

  3. The three types of micro-textures primarily affect the reduction of the tool’s main cutting force, followed by a decrease in feed force, with minimal impact on tool engagement resistance.

  4. Micro-textures aligned parallel to the friction direction can effectively decrease the main cutting force of the tool by more than 60% and cutting resistance by approximately 25%.

Acknowledgements

The authors greatly acknowledge National Key Research and Development Program under (Grant 2022YFB3205801), The Major Science and Technology Project of Anhui Province (Grant 2022e03020002), Natural Science Basic Research Program of Shaanxi (Grant 2024JC-YBQN-0455), Open Research Fund of State Key Laboratory of Mechanical Manufacturing Systems Engineering (Grant sklms 2022016) for the financial and technical support of the present study.

  1. Funding information: Authors state no funding involved.

  2. Author contributions: All authors contributed to the conception and design of the review. All authors approved the final version to be submitted.

  3. Conflict of interest: The authors state no conflict of interest.

  4. Data availability statement: The data that support the findings of this study are available in the Additional files of this article.

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Received: 2024-02-27
Revised: 2024-06-10
Accepted: 2024-08-15
Published Online: 2024-10-22

© 2024 the author(s), published by De Gruyter

This work is licensed under the Creative Commons Attribution 4.0 International License.

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https://doi.org/10.1515/htmp-2024-0048
Keywords for this article
micro-textures; tribology; cutting force; friction coefficient
Creative Commons
BY 4.0

Articles in the same Issue

  1. Research Articles
  2. De-chlorination of poly(vinyl) chloride using Fe2O3 and the improvement of chlorine fixing ratio in FeCl2 by SiO2 addition
  3. Reductive behavior of nickel and iron metallization in magnesian siliceous nickel laterite ores under the action of sulfur-bearing natural gas
  4. Study on properties of CaF2–CaO–Al2O3–MgO–B2O3 electroslag remelting slag for rack plate steel
  5. The origin of {113}<361> grains and their impact on secondary recrystallization in producing ultra-thin grain-oriented electrical steel
  6. Channel parameter optimization of one-strand slab induction heating tundish with double channels
  7. Effect of rare-earth Ce on the texture of non-oriented silicon steels
  8. Performance optimization of PERC solar cells based on laser ablation forming local contact on the rear
  9. Effect of ladle-lining materials on inclusion evolution in Al-killed steel during LF refining
  10. Analysis of metallurgical defects in enamel steel castings
  11. Effect of cooling rate and Nb synergistic strengthening on microstructure and mechanical properties of high-strength rebar
  12. Effect of grain size on fatigue strength of 304 stainless steel
  13. Analysis and control of surface cracks in a B-bearing continuous casting blooms
  14. Application of laser surface detection technology in blast furnace gas flow control and optimization
  15. Preparation of MoO3 powder by hydrothermal method
  16. The comparative study of Ti-bearing oxides introduced by different methods
  17. Application of MgO/ZrO2 coating on 309 stainless steel to increase resistance to corrosion at high temperatures and oxidation by an electrochemical method
  18. Effect of applying a full oxygen blast furnace on carbon emissions based on a carbon metabolism calculation model
  19. Characterization of low-damage cutting of alfalfa stalks by self-sharpening cutters made of gradient materials
  20. Thermo-mechanical effects and microstructural evolution-coupled numerical simulation on the hot forming processes of superalloy turbine disk
  21. Endpoint prediction of BOF steelmaking based on state-of-the-art machine learning and deep learning algorithms
  22. Effect of calcium treatment on inclusions in 38CrMoAl high aluminum steel
  23. Effect of isothermal transformation temperature on the microstructure, precipitation behavior, and mechanical properties of anti-seismic rebar
  24. Evolution of residual stress and microstructure of 2205 duplex stainless steel welded joints during different post-weld heat treatment
  25. Effect of heating process on the corrosion resistance of zinc iron alloy coatings
  26. BOF steelmaking endpoint carbon content and temperature soft sensor model based on supervised weighted local structure preserving projection
  27. Innovative approaches to enhancing crack repair: Performance optimization of biopolymer-infused CXT
  28. Structural and electrochromic property control of WO3 films through fine-tuning of film-forming parameters
  29. Influence of non-linear thermal radiation on the dynamics of homogeneous and heterogeneous chemical reactions between the cone and the disk
  30. Thermodynamic modeling of stacking fault energy in Fe–Mn–C austenitic steels
  31. Research on the influence of cemented carbide micro-textured structure on tribological properties
  32. Performance evaluation of fly ash-lime-gypsum-quarry dust (FALGQ) bricks for sustainable construction
  33. First-principles study on the interfacial interactions between h-BN and Si3N4
  34. Analysis of carbon emission reduction capacity of hydrogen-rich oxygen blast furnace based on renewable energy hydrogen production
  35. Just-in-time updated DBN BOF steel-making soft sensor model based on dense connectivity of key features
  36. Effect of tempering temperature on the microstructure and mechanical properties of Q125 shale gas casing steel
  37. Review Articles
  38. A review of emerging trends in Laves phase research: Bibliometric analysis and visualization
  39. Effect of bottom stirring on bath mixing and transfer behavior during scrap melting in BOF steelmaking: A review
  40. High-temperature antioxidant silicate coating of low-density Nb–Ti–Al alloy: A review
  41. Communications
  42. Experimental investigation on the deterioration of the physical and mechanical properties of autoclaved aerated concrete at elevated temperatures
  43. Damage evaluation of the austenitic heat-resistance steel subjected to creep by using Kikuchi pattern parameters
  44. Topical Issue on Focus of Hot Deformation of Metaland High Entropy Alloys - Part II
  45. Synthesis of aluminium (Al) and alumina (Al2O3)-based graded material by gravity casting
  46. Experimental investigation into machining performance of magnesium alloy AZ91D under dry, minimum quantity lubrication, and nano minimum quantity lubrication environments
  47. Numerical simulation of temperature distribution and residual stress in TIG welding of stainless-steel single-pass flange butt joint using finite element analysis
  48. Special Issue on A Deep Dive into Machining and Welding Advancements - Part I
  49. Electro-thermal performance evaluation of a prismatic battery pack for an electric vehicle
  50. Experimental analysis and optimization of machining parameters for Nitinol alloy: A Taguchi and multi-attribute decision-making approach
  51. Experimental and numerical analysis of temperature distributions in SA 387 pressure vessel steel during submerged arc welding
  52. Optimization of process parameters in plasma arc cutting of commercial-grade aluminium plate
  53. Multi-response optimization of friction stir welding using fuzzy-grey system
  54. Mechanical and micro-structural studies of pulsed and constant current TIG weldments of super duplex stainless steels and Austenitic stainless steels
  55. Stretch-forming characteristics of austenitic material stainless steel 304 at hot working temperatures
  56. Work hardening and X-ray diffraction studies on ASS 304 at high temperatures
  57. Study of phase equilibrium of refractory high-entropy alloys using the atomic size difference concept for turbine blade applications
  58. A novel intelligent tool wear monitoring system in ball end milling of Ti6Al4V alloy using artificial neural network
  59. A hybrid approach for the machinability analysis of Incoloy 825 using the entropy-MOORA method
  60. Special Issue on Recent Developments in 3D Printed Carbon Materials - Part II
  61. Innovations for sustainable chemical manufacturing and waste minimization through green production practices
  62. Topical Issue on Conference on Materials, Manufacturing Processes and Devices - Part I
  63. Characterization of Co–Ni–TiO2 coatings prepared by combined sol-enhanced and pulse current electrodeposition methods
  64. Hot deformation behaviors and microstructure characteristics of Cr–Mo–Ni–V steel with a banded structure
  65. Effects of normalizing and tempering temperature on the bainite microstructure and properties of low alloy fire-resistant steel bars
  66. Dynamic evolution of residual stress upon manufacturing Al-based diesel engine diaphragm
  67. Study on impact resistance of steel fiber reinforced concrete after exposure to fire
  68. Bonding behaviour between steel fibre and concrete matrix after experiencing elevated temperature at various loading rates
  69. Diffusion law of sulfate ions in coral aggregate seawater concrete in the marine environment
  70. Microstructure evolution and grain refinement mechanism of 316LN steel
  71. Investigation of the interface and physical properties of a Kovar alloy/Cu composite wire processed by multi-pass drawing
  72. The investigation of peritectic solidification of high nitrogen stainless steels by in-situ observation
  73. Microstructure and mechanical properties of submerged arc welded medium-thickness Q690qE high-strength steel plate joints
  74. Experimental study on the effect of the riveting process on the bending resistance of beams composed of galvanized Q235 steel
  75. Density functional theory study of Mg–Ho intermetallic phases
  76. Investigation of electrical properties and PTCR effect in double-donor doping BaTiO3 lead-free ceramics
  77. Special Issue on Thermal Management and Heat Transfer
  78. On the thermal performance of a three-dimensional cross-ternary hybrid nanofluid over a wedge using a Bayesian regularization neural network approach
  79. Time dependent model to analyze the magnetic refrigeration performance of gadolinium near the room temperature
  80. Heat transfer characteristics in a non-Newtonian (Williamson) hybrid nanofluid with Hall and convective boundary effects
  81. Computational role of homogeneous–heterogeneous chemical reactions and a mixed convective ternary hybrid nanofluid in a vertical porous microchannel
  82. Thermal conductivity evaluation of magnetized non-Newtonian nanofluid and dusty particles with thermal radiation
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