Microstructure and Tribological Properties of Spark-Plasma-Sintered Ti3SiC2-Pb-Ag Composites at Elevated Temperatures

Ti3SiC2-PbO-Ag composites (TSC-PA) were successfully prepared using the spark plasma sintering (SPS) technique. The ingredient and morphology of the as-synthesized composites were elaborately investigated. The tribological properties of the TSC-PA pin sliding against Inconel 718 alloys disk at room temperature (RT) to 800 °C were examined in air. The wear mechanisms were argued elaborately. The results showed that the TSC-PA was mainly composed of Ti3SiC2, Pb, and Ag. The average friction coefficient of TSC-PA gradually decreased from 0.72 (RT) to 0.3 (800 °C), with the temperature increasing from RT to 800 °C. The wear rate of TSC-PA showed a decreasing trend, with the temperature rising from RT to 800 °C. The wear rate of Inconel 718 exhibited positive wear at RT and negative wear at elevated temperatures. The tribological property of TSC-PA was related to the tribo-chemistry, and the abrasive and adhesive wear.


Introduction
Ti 3 SiC 2 belongs to one of the MAX phases (polycrystalline nanolaminates of ternary carbides and nitrides, over 60 + phases) [1]. It possesses the combined characteristics of metal and ceramics, such as being easily machinable, being electrically and thermally conductive, being oxidation resistant, and having a high melting point. Ti 3 SiC 2 can be a potential candidate for structural functional components. Similar to graphite and MoS 2 , it has a hexagonal structure, endowing it with an exceptional lubricating property. Research on the tribological properties of Ti 3 SiC 2 demonstrated that it is not a special solid lubricant. Contrarily, Ti 3 SiC 2 generally has a high friction coefficient (µ > 0.6) and a high wear rate (WR: in the order of 10 −2 -10 −3 mm 3 /N m), especially at medium and low temperatures (RT) [2][3][4][5][6][7][8]. It has been reported that, in some circumstances (such as with temperature > 600 • C, at a speed of >5 m/s, or sliding against some particular tribopair material), polycrystalline Ti 3 SiC 2 displays the relatively low µ and wear rate, which mainly results from the tribo-oxidation transfer films generated on the contact surface [2,6,[8][9][10]. In other situations, the fracture and pulling-out of Ti 3 SiC 2 grains causes three-body abrasive wear, which is the main wear mechanisms for Ti 3 SiC 2 .
Subsequently, most of scientific enthusiasts concentrate on the intensifying research of polycrystalline Ti 3 SiC 2 by uniting metal and/or ceramic to enhance its friction and wear behaviors. Ren et al. [11] prepared Ti 3 SiC 2 /Cu/Al/SiC composites, and they found that the tribological behaviors of the composite were better than those of polycrystalline Ti 3 SiC 2 at RT and 200 • C, while the wear properties of the composite were worse than

Mechanical Properties
The densities of the composites were determined using Archimedes's principle. Microhardness was measured on a Micro-hardness Tester (MH-5-VM, Shanghai Hengyi Technology Co., Ltd., Shanghai, China). with a load of 500 g and a dwell time of 10 s. Flexural strength and compression strength were measured using a universal material tester (SANS-CMT5205, Shenzhen New Sansi Material Testing Co., Ltd., Shenzhen, China). The three-point bending test was conducted to obtain the flexural strength, and the samples were cut to 3 mm high × 4 mm wide × 20 mm long. The cross-head speed and span were 0.05 mm/min and 16 mm, respectively. The sizes of the samples for the compression strength test were Φ 5 mm × 12.5 mm, and the cross-head speed was 0.2 mm/min.

Friction and Wear Test
The friction and wear experiments were carried out in air on a high-temperature tribometer with a pin-on-disk setup (THT01-04015, CSM Instruments SA, Peseux, Switzerland). The TSC-PA was used as a pin, the size of which was Φ 6 mm × 12 mm. The Inconel 718 was used as a disk, and its size was Φ 32 mm × 8 mm. The surfaces of the disk and pin were ground and polished into a surface roughness (Ra) of 0.06 µm. The tribopairs slid against each other for 200 m at a sliding speed of 0.1 m/s under a normal load of 5 N. The friction coefficient was automatically documented by computer during the experiment. The wear volume was obtained by quantifying the volume loss of TSC-PA pin by optical microscopy and by examining the cross-sectional area of the worn area of Inconel 718 disk by 3D surface profilometry (NanoMap-D, Columbus, OH, USA). The wear rates were acquired by Equation (1)

Analysis
The morphology of TSC-PA was investigated by scanning electron microscopy (SEM, JSM-5600LV, JEOL, Tokyo, Japan) equipped with energy dispersive X-ray spectroscopy. The EDS (IE250, Oxford Instrument, Abingdon, Oxfordshire, UK) was equipped with X-Max Silicon Drift Detector (SDD; the spectral resolution of 124 eV at Mn Kα) and an ultra-thin window; the active area of the SDD was 50 mm 2 . The phase composition of TSC-PA was analyzed by X-ray diffraction (XRD, Philips X'Pert Pro, PANalytical Netherlands, Almelo, Netherland) using Cu Kα radiation (λ = 0.15418 nm) within the 2θ-angle range from 5 • to 90 • . X-ray photoelectron spectroscope (XPS, PHI-5702, Physical Electronics Corporation, Chanhassen, MN, USA) was used to analyze the elemental chemical states of TSC-PA on the worn surfaces, and the binding energy of adventitious carbon (C1s: 284.8 eV) was used as the reference.

Phase Composition and Microstructure of TSC-PA
The XRD pattern of TSC-PA is displayed in Figure 1. As noticed in Figure 1, the main phases of TSC-PA were Ti 3 SiC 2 , Pb, and Ag. The Ti 3 SiC 2 was temporarily stable and did not break down during the sintering process of TSC-PA. To the best of the authors' knowledge, the Ti 3 SiC 2 revealed high reaction activity when in contact with the metal phases, such as Cu [23][24][25], Al [26,27], and Fe [28]. In this study, the Ti 3 SiC 2 did not decompose with the co-addition of Ag and PbO at the sintering temperature of 1130 • C. In a previous paper [21], we reported that PbO in the Ti 3 SiC 2 -PbO system was deoxidized to Pb by C or Si during the preparation process and Ti 3 SiC 2 did not decompose at 1200 • C. The relevant chemical reactions were described in Reference [21]. In comparison, the addition of Ag did not change the composition of the Ti 3 SiC 2 -PbO system.

Phase Composition and Microstructure of TSC-PA
The XRD pattern of TSC-PA is displayed in Figure 1. As noticed in Figure 1, the main phases of TSC-PA were Ti3SiC2, Pb, and Ag. The Ti3SiC2 was temporarily stable and did not break down during the sintering process of TSC-PA. To the best of the authors' knowledge, the Ti3SiC2 revealed high reaction activity when in contact with the metal phases, such as Cu [23][24][25], Al [26,27], and Fe [28]. In this study, the Ti3SiC2 did not decompose with the co-addition of Ag and PbO at the sintering temperature of 1130 °C . In a previous paper [21], we reported that PbO in the Ti3SiC2-PbO system was deoxidized to Pb by C or Si during the preparation process and Ti3SiC2 did not decompose at 1200 °C . The relevant chemical reactions were described in Reference [21]. In comparison, the addition of Ag did not change the composition of the Ti3SiC2-PbO system. As observed in Figure 2, the morphology and the distributions of elements of the cross section of the TSC-PA was analyzed using SEM. It can be observed that the Pb particles were homogeneously scattered in the Ti3SiC2 matrix, while the Ag particles were agglomerated to a certain extent. As the melting point of silver was merely 961 °C , some amount of molten silver nearby flowed together during sintering. Therefore, the agglomeration of Ag occurred in the TSC-PA.  As observed in Figure 2, the morphology and the distributions of elements of the cross section of the TSC-PA was analyzed using SEM. It can be observed that the Pb particles were homogeneously scattered in the Ti 3 SiC 2 matrix, while the Ag particles were agglomerated to a certain extent. As the melting point of silver was merely 961 • C, some amount of molten silver nearby flowed together during sintering. Therefore, the agglomeration of Ag occurred in the TSC-PA.

Phase Composition and Microstructure of TSC-PA
The XRD pattern of TSC-PA is displayed in Figure 1. As noticed in Figure 1, the m phases of TSC-PA were Ti3SiC2, Pb, and Ag. The Ti3SiC2 was temporarily stable and not break down during the sintering process of TSC-PA. To the best of the auth knowledge, the Ti3SiC2 revealed high reaction activity when in contact with the m phases, such as Cu [23][24][25], Al [26,27], and Fe [28]. In this study, the Ti3SiC2 did not compose with the co-addition of Ag and PbO at the sintering temperature of 1130 °C . previous paper [21], we reported that PbO in the Ti3SiC2-PbO system was deoxidize Pb by C or Si during the preparation process and Ti3SiC2 did not decompose at 1200 The relevant chemical reactions were described in Reference [21]. In comparison, the dition of Ag did not change the composition of the Ti3SiC2-PbO system. As observed in Figure 2, the morphology and the distributions of elements of cross section of the TSC-PA was analyzed using SEM. It can be observed that the Pb ticles were homogeneously scattered in the Ti3SiC2 matrix, while the Ag particles w agglomerated to a certain extent. As the melting point of silver was merely 961 °C , s amount of molten silver nearby flowed together during sintering. Therefore, the aggl eration of Ag occurred in the TSC-PA.

Mechanical Performance of TSC-PA
The relative density, microhardness, flexural strength, and compressive strength of TSC-PA and TSC are listed in Table 1. It can be seen that the relative densities of TSC-PA and TSC were 95.35% and 98.24%, respectively. The microhardness of TSC-PA was less than half that of TSC, and their microhardness values were 2.24 and 5.5 GPa, respectively. Pb and Ag in the TSC-PA belong to soft metals and caused the low hardness of TSC-PA. The flexural strength of TSC-PA was less than that of TSC, and their values were 311 and  Note: The data in the first line were from Reference [21].
As shown in Figure 3a, the TSC-PA only suffered from elastic deformation before fracture, which was a typical brittle fracture. The fracture surface of TSC-PA (see Figure 3b) indicated that the fracture surface of TSC-PA was featured by intergranular and transgranular fracture. This fracture mode of TSC-PA was similar to TSC. As well known, the diverse energy-absorbing strategies including the diffuse of the microcracks, lamination, crack deflection, and grain pull-out were discovered to be in charge of the high flexural strength of TSC [29,30]. In addition to intergranular and transgranular fracture, some pores and cracks resulting from the unsatisfactory compatibility (e.g., wettability) of the TSC matrix and Pb and Ag were observed (see Figure 3b). The thermal expansion coefficients (for instance: TSC: 9.1 × 10 −6 , Pb: 29.3 × 10 −6 , and Ag: 19.5 × 10 −6 • C −1 ) of different phases were not matched with each other, leading to the weak bonding between granules and the formation of some defects (such as micro-pores and micro-cracks) during the preparation procedure. The as-formed defects were detrimental to the flexural strength. An additional major justification for the poor fracture strength of the TSC-PA was that the distribution of Pb and Ag around the TSC grains to a certain extent hindered the diverse energy-assimilating strategies, which let fracture take place between the grains. and TSC were 95.35% and 98.24%, respectively. The microhardness of TSC-PA was less than half that of TSC, and their microhardness values were 2.24 and 5.5 GPa, respectively. Pb and Ag in the TSC-PA belong to soft metals and caused the low hardness of TSC-PA. The flexural strength of TSC-PA was less than that of TSC, and their values were 311 and 428 MPa, respectively. The compressive strength of TSC-PA was only half that of TSC, and their values were 654 MPa and 1230 MPa, respectively. Note a: The data in the first line were from Reference [21].
As shown in Figure 3a, the TSC-PA only suffered from elastic deformation before fracture, which was a typical brittle fracture. The fracture surface of TSC-PA (see Figure  3b) indicated that the fracture surface of TSC-PA was featured by intergranular and transgranular fracture. This fracture mode of TSC-PA was similar to TSC. As well known, the diverse energy-absorbing strategies including the diffuse of the microcracks, lamination, crack deflection, and grain pull-out were discovered to be in charge of the high flexural strength of TSC [29,30]. In addition to intergranular and transgranular fracture, some pores and cracks resulting from the unsatisfactory compatibility (e.g., wettability) of the TSC matrix and Pb and Ag were observed (see Figure 3b). The thermal expansion coefficients (for instance: TSC: 9.1 × 10 −6 , Pb: 29.3 × 10 −6 , and Ag: 19.5 × 10 −6 °C −1 ) of different phases were not matched with each other, leading to the weak bonding between granules and the formation of some defects (such as micro-pores and micro-cracks) during the preparation procedure. The as-formed defects were detrimental to the flexural strength. An additional major justification for the poor fracture strength of the TSC-PA was that the distribution of Pb and Ag around the TSC grains to a certain extent hindered the diverse energy-assimilating strategies, which let fracture take place between the grains.   Figure 4a showed the plot of µ versus distance curve of the TSC-PA/Inconel 718 tribopair at elevated temperatures. It can be easily construed that the temperature had a direct effect on the µ of the tribopair. At RT and 200 • C, the µ had a big fluctuation. At 400, 600, and 800 • C, the incipient µ had a big fluctuation and, then, it soon achieved a steady state with low µ values. Specifically, at RT, the µ showed a larger fluctuation than that at other temperatures. Particularly, at 600 • C, the µ exhibited a turbulent behavior in contrasted with that at other temperatures, which indicated an incipient short breakin period with relatively low µ values; then, it reached high µ values and fluctuated largely. Later, it approached a stable state with relatively low µ values. In comparison, the fluctuation of the µ decreased with the temperature increasing from RT to 800 • C. Figure 4b compared the µ mean of TSC-PA/Inconel 718 tribopair at elevated temperatures. It can be seen that the µ mean decreased with the temperature increasing from RT to 800 • C. steady state with low μ values. Specifically, at RT, the μ showed a larger fluctuation than that at other temperatures. Particularly, at 600 °C, the μ exhibited a turbulent behavior in contrasted with that at other temperatures, which indicated an incipient short break-in period with relatively low μ values; then, it reached high μ values and fluctuated largely. Later, it approached a stable state with relatively low μ values. In comparison, the fluctuation of the μ decreased with the temperature increasing from RT to 800 °C. Figure 4b compared the μmean of TSC-PA/Inconel 718 tribopair at elevated temperatures. It can be seen that the μmean decreased with the temperature increasing from RT to 800 °C. Figure 5a plotted the wear rates of the TSC-PA pin at elevated temperatures. The wear rates of the pin decreased with the temperature increasing from RT to 400 °C. Moreover, the wear rates of the pin were the same when the temperature was at 400, 600, and 800 °C. No other results were found in the literature for a comparison with the results in this work because Ti3SiC2 composites with the co-addition of PbO and Ag have not been reported before. Moreover, it was not easy to make a comparison between tribology results as they were carried out under distinct conditions on the basis of the detailed demands of an application. For interpretative aspirations, Table 2 compared tribological behavior of Ti3SiC2 composites with the addition of the different amount of Ag or the addition of the different amount of PbO. Comparatively, the incorporation of relative low content (5-20 vol%) of Ti3SiC2 can diminish the wear rate of the Ag-based composite during sliding against Al2O3 at 5N and 0.5 m/s [19]. In this work, the situation was different because the sample was Ti3SiC2 based-composite with 70 vol% of Ti3SiC2. At RT, comparatively, Ti3SiC2 and composites of Ti3SiC2 with 15vol% Ag, with 15vol% PbO, and with 15vol% PbO-15vol% Ag showed wear rates of 2 × 10 −3 mm 3 /(N·m), 3 × 10 −5 mm 3 /(N·m), 2 × 10 −4 mm 3 /(N·m), and 2 × 10 −4 mm 3 /(N·m), respectively, during sliding against Inconel 718 at 5N and 0.1 m/s [20,22]. These results showed that the incorporation of 15vol% Ag or 15vol% PbO or 15vol% PbO-15vol% Ag can decrease the wear rate of Ti3SiC2 by at least an order of magnitude at RT. At elevated temperatures (>200 °C), the composite of Ti3SiC2 with 15vol% PbO showed better wear resistance than both Ti3SiC2 and the composite of Ti3SiC2 with 15vol% PbO-15vol% Ag (TSC-PA). The tribological behavior of the composite of Ti3SiC2 with 15vol% Ag at elevated temperature was unavailable and incomparable. It can be seen from Table 2 that TSC-PA showed a lower friction than TSC at > 200 °C and a lower friction than Ti3SiC2-15vol% PbO at <600 °C. It was concluded that the addition of  Figure 5a plotted the wear rates of the TSC-PA pin at elevated temperatures. The wear rates of the pin decreased with the temperature increasing from RT to 400 • C. Moreover, the wear rates of the pin were the same when the temperature was at 400, 600, and 800 • C. No other results were found in the literature for a comparison with the results in this work because Ti 3 SiC 2 composites with the co-addition of PbO and Ag have not been reported before. Moreover, it was not easy to make a comparison between tribology results as they were carried out under distinct conditions on the basis of the detailed demands of an application. For interpretative aspirations, Table 2 compared tribological behavior of Ti 3 SiC 2 composites with the addition of the different amount of Ag or the addition of the different amount of PbO. Comparatively, the incorporation of relative low content (5-20 vol%) of Ti 3 SiC 2 can diminish the wear rate of the Ag-based composite during sliding against Al 2 O 3 at 5N and 0.5 m/s [19]. In this work, the situation was different because the sample was Ti 3 SiC 2 based-composite with 70 vol% of Ti 3 SiC 2 . At RT, comparatively, Ti 3 SiC 2 and composites of Ti 3 SiC 2 with 15 vol% Ag, with 15 vol% PbO, and with 15 vol% PbO-15 vol% Ag showed wear rates of 2 × 10 −3 mm 3 /(N·m), 3 × 10 −5 mm 3 /(N·m), 2 × 10 −4 mm 3 /(N·m), and 2 × 10 −4 mm 3 /(N·m), respectively, during sliding against Inconel 718 at 5N and 0.1 m/s [20,22]. These results showed that the incorporation of 15 vol% Ag or 15 vol% PbO or 15 vol% PbO-15 vol% Ag can decrease the wear rate of Ti 3 SiC 2 by at least an order of magnitude at RT. At elevated temperatures (>200 • C), the composite of Ti 3 SiC 2 with 15 vol% PbO showed better wear resistance than both Ti 3 SiC 2 and the composite of Ti 3 SiC 2 with 15 vol% PbO-15 vol% Ag (TSC-PA). The tribological behavior of the composite of Ti 3 SiC 2 with 15 vol% Ag at elevated temperature was unavailable and incomparable. It can be seen from Table 2 that TSC-PA showed a lower friction than TSC at > 200 • C and a lower friction than Ti 3 SiC 2 -15 vol% PbO at <600 • C. It was concluded that the addition of PbO and Ag apparently improved the tribological behavior of TSC-PA, in comparison with TSC and Ti 3 SiC 2 -15 vol% PbO.  Figure 5b compared the wear rates of the Inconel 718 disk sliding against TSC-PA at elevated temperatures. As the temperature raised from RT to 800 °C, the wear rates of the disk decreased. At RT, a positive wear rate was found for the disk. Interestingly, negative wear rates were detected for the disk and increased with the temperature rising from 200 to 800 °C. Moreover, the wear rate of the disk at 600 °C was identical to that at 800 °C. The    Figure 5b compared the wear rates of the Inconel 718 disk sliding against TSC-PA at elevated temperatures. As the temperature raised from RT to 800 • C, the wear rates of the disk decreased. At RT, a positive wear rate was found for the disk. Interestingly, negative wear rates were detected for the disk and increased with the temperature rising from 200 to 800 • C. Moreover, the wear rate of the disk at 600 • C was identical to that at 800 • C. The detection of Ti, Si, Pb, and Ag on the worn surface of Inconel 718 was in line with the negative wear of the disk (see Table 3). Figure 6 showed the SEM assessment of tribosurfaces of TSC-PA/Inconel 718 tribocouple after tribological testing at elevated temperature. TSC-PA was full of scars resulting from the abrasive wear, while the Inconel 718 surface was covered with an even tribolayer delivered from the TSC-PA surface. The surface was surrounded by the tribolayer made up of incompletely oxidized TSC-PA (Table 3 and Figure 6). With the rise in temperature, the tribofilm formed on the surface of TSC-PA was smoother and denser. This film was formed undoubtably by a coalescence of diverse mechanical blending, fracturing, resintering, and mechanically vitalized oxidation and other chemical processes, perhaps, continuously refined during the heat cycle. The EDS data showed that the elements of Ni, Cr, and Fe from Inconel 718 alloy appeared on the surface of TSC-PA (Figure 6a,c,e,g,i in Table 3) and the elements of Ti, Si, Pb, and Ag from TSC-PA appeared on the surface of Inconel718 alloy (Figure 6b,d,f,h,j in Table 3). Moreover, tribo-oxidation was a predominant factor that influenced, and even controlled, the wear mechanism and finally brought about the change of friction and wear features [31]. The chemical states of Ti, Si, Pb, and Ag elements on the worn surface of TSC-PA at RT-800 • C were investigated in detail by XPS (see Figure 7). Table 3. The chemical components of samples corresponding to Figure 6 as determined by EDS. At RT, some wear debris dispersed on the worn surface of the TSC-PA with several dark continent regions (see Figure 6a). It was worth mentioning that some loose cracks and pores scattered on the worn surface, which was due to the peeling-off and decentralization of the granules. Such an episode was in accordance with Ti 3 SiC 2 [6]. Therefore, it can be deduced that the addition of Pb and Ag did not affect the wear behavior of Ti 3 SiC 2 at RT. Though the weak bonding between Ti 3 SiC 2 grains in the TSC-PA led to the fracture and pulling out of Ti 3 SiC 2 granules, soft metals (including Pb and Ag) distributed around the Ti 3 SiC 2 grains, inhibiting the peeling-off and decentralization of Ti 3 SiC 2 matrix; therefore, the wear rate of TSC-PA was only one tenth of Ti 3 SiC 2 (see Table 2). A third body was formed and entrapped between the pin and disk, leading to the severe wear of TSC-PA and Inconel 718 at RT. The obvious evidence was that wear grooves were found on the worn surface of Inconel 718 after tribology testing at RT (see Figure 6b) and mutual material transfer between the pin and disk was detected by EDS analysis (see Table 3). The abrasive wear was the primary wear mechanism for TSC-PA. A small amount of SiO 2 and PbO was detected on the worn surface of TSC-PA (see Figure 7). However, the temperature was too low to form an enough thick tribo-oxidation film between the contact surface of TSC-PA and Inconel 718, so high friction coefficients and high wear rates were present at RT (see Figures 4 and 5a).

Positions
At 200 • C, some compacted wear debris was found on the worn surface of TSC-PA (see Figure 6c). Compared with RT, besides SiO 2 and PbO, other oxides, TiO 2 and Ag 2 O, were formed on the surface of TSC-PA (evidently owing to the XPS at 200 • C in Figure 7), generating a thicker tribo-oxidation film. The formation of the tribo-oxidation film did not inhibit the fracture and pulling-out of Ti 3 SiC 2 grains. The formation and entrapment of the third body (the formed wear debris) between the pin and disk contributed to the wear of TSC-PA and Inconel 718. The mutual material transfer between the pin and disk at 200 • C was detected by EDS analysis (see Table 3). A tribo-oxidation film with some wear grooves was transferred to the Inconel 718, so the counterpart showed relatively flat region and slight negative wear (see Figures 5b and 6d). At 200 • C, the abrasive wear mechanism was the main wear mechanism with very slight adhesive wear. TSC-PA; therefore, the wear rate of TSC-PA at 400 °C exhibited a distinct decline in contrast to those at RT and 200 °C. Moreover, the addition of Ag and Pb could strengthen the ductility of TSC-PA. On other hand, when the asperities of the tribo-pair were in contact with each other, the instant flash temperature may reach 3000 °C [32]. Therefore, a high temperature was beneficial for the formation of oxides, such as TiO2, SiO2, PbO, and Ag2O. Therefore, the adhesive wear and plastic flow was the main wear mechanism with slight abrasive wear (as distinct on account of the slight wear trenches on the Inconel 718 disk).  which was smoothest and densest among all temperatures (see Figure 6). With the thickness of the tribofilm increasing, the covering of the Inconel 718 surface increased. Matter accumulation on the Inconel 718 led to seizure of the contact. The tribofilm reached a critical thickness so that it was easily peeled off from TSC-PA (see Figure 6i). The Inconel 718 showed a smooth tribofilm with large negative wear (see Figures 5b and 6j). Of course, mutual transfer of matter between the pin and the disk was also confirmed by the EDS data in Table 3. The wear mechanism was adhesive wear and tribochemistry of elements of Pb, Ag, Ti, and Si to form TiO2, SiO2, PbO, and AgO (see Figure 7). Conclusively at RT and 200 °C, the abrasive wear ascribed to the peeling-off and pulled-out of Ti3SiC2 grains dominated the wear mechanism of TSC-PA, leading to the indispensable friction and wear. As the temperature increased, the formation of tribo- At 400 • C, obviously, the TSC-PA was covered with some large wear debris after tribology testing (see Figure 6e). It was expected that, initially, a tribo-oxidation film containing TiO 2 , SiO 2 , PbO and Ag 2 O was formed on its surface (as evident owing to the XPS at 400 • C in Figure 7), which was similar to the oxidation composition at 200 • C. Then, the peel-off and removal of the tribo-oxidation film occurred for TSC-PA. As the sliding finished, the mutual material transfer between the pin and disk was detected by EDS analysis (see Table 3). It was seen from Figure 6f that a relatively smooth film was built up on the surface of the Inconel 718. The plastic flow, in some way, retarded the abrasive wear of TSC-PA; therefore, the wear rate of TSC-PA at 400 • C exhibited a distinct decline in contrast to those at RT and 200 • C. Moreover, the addition of Ag and Pb could strengthen the ductility of TSC-PA. On other hand, when the asperities of the tribo-pair were in contact with each other, the instant flash temperature may reach 3000 • C [32]. Therefore, a high temperature was beneficial for the formation of oxides, such as TiO 2 , SiO 2 , PbO, and Ag 2 O. Therefore, the adhesive wear and plastic flow was the main wear mechanism with slight abrasive wear (as distinct on account of the slight wear trenches on the Inconel 718 disk).
At 600 • C, the worn surface of TSC-PA was surrounded by a relatively smooth and continuous tribolayer after tribology testing (see Figure 6g). This surface was covered with a sufficiently thick tribo-oxidation film containing TiO 2 , SiO 2 , PbO, and AgO (see Figure 7). In comparison with 400 • C, AgO was found on the worn surface of TSC-PA at 600 • C instead of Ag 2 O. Interestingly, the existence of AgO played a significant role in the decrease of friction and wear of the tribopair. The worn surface of Inconel 718 was embraced by a tribo-oxidation film, which was transferred from TSC-PA (see Figure 6h). The serious plastic flowing resulted in the adhesive wear. Mutual transfer of matter between the pin and the disk was verified by the EDS results in Table 3. Moreover, with the increase in temperature, especially at above 400 • C, oxygen contents of the pin and the disk were higher, which indicated the thicker thickness of the tribo-oxidation film (see Table 3). Therefore, the friction coefficient of TSC-PA was lower and more stable and its wear rate was low due to the moderately thick oxides. The wear mechanism was adhesive wear at this temperature.
At 800 • C, the worn surface of TSC-PA was surrounded by a tribo-oxidation film, which was smoothest and densest among all temperatures (see Figure 6). With the thickness of the tribofilm increasing, the covering of the Inconel 718 surface increased. Matter accumulation on the Inconel 718 led to seizure of the contact. The tribofilm reached a critical thickness so that it was easily peeled off from TSC-PA (see Figure 6i). The Inconel 718 showed a smooth tribofilm with large negative wear (see Figures 5b and 6j). Of course, mutual transfer of matter between the pin and the disk was also confirmed by the EDS data in Table 3. The wear mechanism was adhesive wear and tribochemistry of elements of Pb, Ag, Ti, and Si to form TiO 2 , SiO 2 , PbO, and AgO (see Figure 7).
Conclusively at RT and 200 • C, the abrasive wear ascribed to the peeling-off and pulled-out of Ti 3 SiC 2 grains dominated the wear mechanism of TSC-PA, leading to the indispensable friction and wear. As the temperature increased, the formation of tribooxidation films was favorable for the reduction in friction and wear of the tribopair. As for the reason why the Inconel 718 disk showed negative wear at elevated temperatures. We proposed that with the temperature increasing, especially at 800 • C, the formed oxidation film was so thick that it was easily peeled-off from the TSC-PA pin and transferred to the Inconel 718 disk, leading to the negative wear of the disk. Additionally, the transition of wear mechanism from abrasive wear to adhesive wear occurred with the increasing temperature. The co-addition of PbO and Ag worked together in the improvement of the tribological behavior of TSC-PA at elevated temperatures, which shed light on the effectiveness of co-addition of solid lubricants in MAX phases at elevated temperatures.

Conclusions
The Ti 3 SiC 2 -Pb-Ag self-lubricating composite (TSC-PA) was successfully sintered by spark plasma sintering technique in vacuum, and its friction and wear behavior were investigated by sliding it against Inconel 718 using a pin-on disk setup at RT and elevated temperatures in air. The results found that the TSC-PA was mainly composed of Ti 3 SiC 2 , Pb, and Ag. The mechanical properties of the TSC-PA were relatively weaker than that of TSC monolithic. As the temperature increased, the average friction coefficient of TSC-PA/Inconel 718 decreased. The wear rate of TSC-PA exhibited a downward trend and that of Inconel 718 decreased, too, with the rise in the temperature. Interestingly, the wear rate of Inconel 718 was positive wear only at RT and changed to negative wear at other temperatures. The wear mechanism was abrasive wear at low and medium temperatures and turned to adhesive wear at higher and elevated temperatures. The tribochemistry of the sliding contact plays an important part in the transition of the wear theories. It was an effective method of the co-addition of solid lubricants in MAX phases.

Data Availability Statement:
The data presented in this study are available within the article.