Tribological Behavior and Self-Healing Properties of Ni 3 Al Matrix Self-Lubricating Composites Containing Sn-Ag-Cu and Ti 3 SiC 2 from 20 to 800 ◦ C

: As a high-temperature structural material, Ni 3 Al matrix composites are often used to manufacture basic mechanical components that need to be used in high-temperature conditions. To meet the increasing demand for metal matrix composites with an excellent tribological performance over a wide temperature range, Ni 3 Al matrix self-lubricating composites containing Sn-Ag-Cu and Ti 3 SiC 2 (NST) were synthesized via laser-melting deposition. Dry sliding friction tests of NST against Si 3 N 4 ball were undertaken from 20 to 800 ◦ C to investigate the tribological behavior and wear-triggered self-healing properties. The results show that the tribological behaviors of NST are strongly dependent on the testing temperature and self-healing properties. At low and moderate temperatures from 20 to 400 ◦ C, as the Sn-Ag-Cu ﬂows into the cracks and is oxidized during sliding friction, while the cracks on the worn surface are ﬁlled with oxides consisting mainly of Al 2 O 3 , SnO 2 and CuO. At higher temperatures of 600 and 800 ◦ C, the cracks are ﬁlled by the principal oxides of Al 2 O 3 , TiO 2 and SiO 2 due to the partial decomposition and oxidation of Ti 3 SiC 2 . Compared with other testing temperatures, the recovery ratio relative to the Ni 3 Al base alloy of the cracks on the worn surface of NST is the highest at 400 ◦ C, which is about 76.4%. The synergistic action mechanisms of Sn-Ag-Cu and Ti 3 SiC 2 on the crack self-healing from 20 to 800 ◦ C play a signiﬁcant role in forming a stable solid lubricating ﬁlm, improving the anti-friction and wear resistance of NST. The results provide a solution allowing for metal matrix composites to achieve excellent lubrication stability over a wide temperature range by virtue of the crack self-healing properties.


Introduction
Recently, researchers around the world have shown great interest in self-healing composites because such self-healing properties might increase their service life, reducing maintenance costs and improving product safety and reliability [1]. Self-healing composites can repair stress cracking caused by fatigue wear [2]. These self-healing properties are an effective mechanism by which materials can delay mechanical damage, which can enhance their mechanical and tribological performances [2,3].
To realize the self-healing properties of metal matrix composites, the current methods adopted by domestic and foreign scholars mainly include precipitation self-healing, shape-memory-alloybased self-repairing and the addition of a healing agent to the composites [3,4]. Yang et al. [5] analyzed the self-regulating tribological function of titanium alloy with a MgAl microchannel. The results indicated that the Al 2 O 3 and graphene could enhance the self-recovery performance of the friction interface, resulting in a good self-healing morphology of the worn surface material. Lucci et al. [6] discussed the self-healing properties of a metal matrix

Materials Preparation
The main compositions of Ni 3 Al-based alloy (NBA) are shown in Table 1. Starting materials for NBA, Sn-Ag-Cu and Ti 3 SiC 2 are commercial powders (Changsha Tianjiu Metal Materials Co., Ltd., Changsha, China) with the average sizes of 5-20 µm. Referring to the previous experimental studies of Liu et al. [18] and Xu et al. [19], to obtain good lubrication and mechanical composite properties, the addition ratios of Sn-Ag-Cu and Ti 3 SiC 2 in the matrix were determined to be 10 wt.% and 12 wt.%, respectively. The compositions and microhardness of the as-prepared samples are shown in Table 2. The element ratio of Sn, Ag and Cu was determined to be 50:40:10 [18,20]. The initial powder was prepared according to the corresponding adding ratio and mixed evenly using a common planetary ball mill. Finally, the spherical powder was prepared by a centrifugal atomization equipment (LD-QW/500, Hebei Jingye Additive Manufacturing Co., Ltd., Shijiazhuang, China). Figure 1 shows the flow chart for the preparation process of NST  [21][22][23], the optimum process parameters for LMD obtained after multiple parameter tests are listed in Table 3. According to the lubricant addition ratios and LMD process parameters, the NBA, NST, NT and NS samples were prepared using 3D printing equipment (RC-LDM-8060, Nanjing Yuchen Laser Technology Co. Ltd., Nanjing, China). The dimensions of the samples were 25 mm × 25 mm × 10 mm. To obtain a low surface roughness (0.15 ± 0.02 µm), the surfaces of the NBA, NST, NT and NS were mechanically polished. prepared according to the corresponding adding ratio and mixed evenly using a common planetary ball mill. Finally, the spherical powder was prepared by a centrifugal atomization equipment (LD-QW/500, Hebei Jingye Additive Manufacturing Co., Ltd., Shijiazhuang, China). Figure 1 shows the flow chart for the preparation process of NST via LMD. Referring to relevant studies [21][22][23], the optimum process parameters for LMD obtained after multiple parameter tests are listed in Table 3. According to the lubricant addition ratios and LMD process parameters, the NBA, NST, NT and NS samples were prepared using 3D printing equipment (RC-LDM-8060, Nanjing Yuchen Laser Technology Co. Ltd., Nanjing, China). The dimensions of the samples were 25 mm × 25 mm × 10 mm. To obtain a low surface roughness (0.15 ± 0.02 µm), the surfaces of the NBA, NST, NT and NS were mechanically polished.

Friction Testing and Material Characterization Methods
The friction tests of NBA, NST, NT and NS samples were executed with a multi-function tribometer (MFT-5000, Rtec, San Jose, CA, USA) for 60 min at 20, 200, 400, 600 and 800 °C. Si3N4 ball was selected as the counter-pair due to its low thermal expansion coefficient and excellent oxidation resistance in a wide temperature range [24]. The sliding speed was

Friction Testing and Material Characterization Methods
The friction tests of NBA, NST, NT and NS samples were executed with a multifunction tribometer (MFT-5000, Rtec, San Jose, CA, USA) for 60 min at 20, 200, 400, 600 and 800 • C. Si 3 N 4 ball was selected as the counter-pair due to its low thermal expansion coefficient and excellent oxidation resistance in a wide temperature range [24]. The sliding speed was 0.2 m/s [25]. The applied load was 12 N [26]. The friction radius was 5 mm. The friction coefficients of the samples were recorded by the device. The wear rates W of the samples were calculated as W = V/(P × S), where V, P and S were the wear volume, applied load and total sliding distance, respectively. As presented in Figure 2b, to obtain the wear volume of the samples, a 2D cross-sectional profile was measured by a profilometer (ST400, Nanovea Corporation, Irvine, CA, USA) along the line AA (see Figure 2a). The depth and width of the wear scar of NST after friction and wear tests at 20 • C were 22 µm and 1.2 mm, respectively. The friction tests were repeated thrice to obtain the mean value. 0.2 m/s [25]. The applied load was 12 N [26]. The friction radius was 5 mm. The friction coefficients of the samples were recorded by the device. The wear rates W of the samples were calculated as W = V/(P × S), where V, P and S were the wear volume, applied load and total sliding distance, respectively. As presented in Figure 2b, to obtain the wear volume of the samples, a 2D cross-sectional profile was measured by a profilometer (ST400, Nanovea Corporation, Irvine, CA, USA) along the line AA (see Figure 2a). The depth and width of the wear scar of NST after friction and wear tests at 20 °C were 22 µm and 1.2 mm, respectively. The friction tests were repeated thrice to obtain the mean value. X-ray diffraction (XRD; D/MAX-RB RU-200B, Rigaku, Tokyo, Japan) was used to identify the phase constitutions of the NBA, NS, NT and NST. The microhardness of each sample was obtained by an HVS-1000 Vickers hardness tester (Beijing times peak Technology Co.Ltd., Beijing, China) with a load of 1 kg and a dwell time of 8 s. The morphologies of the worn surfaces of the NBA, NS, NT and NST were investigated by an electron probe microanalyser (EPMA; JAX-8230, JEOL Ltd., Tokyo, Japan). The elemental compositions of the worn surfaces were acquired using an energy-dispersive spectroscopy (EDS; GENESIS 7000, JEOL Ltd., Japan). To analyze the phase composition of the worn surface, a Raman spectrum (InVia, Renishaw, Gloucester, UK) analysis was performed. The method of cooling fracture was adopted to obtain the cross-section structures of wear scars. The as-prepared samples were incised down to a residual thickness of about 1-1.5 mm at the relative side of the wear scars. After being incised, the samples were cooled for 30 min using liquid nitrogen. The cooled samples were broken by the low shearing force in a dust-free environment. The cross-sectional morphologies of the NBA and NST were characterized using scanning electron microscopy (SEM; JSM-IT300, JEOL Ltd., Japan). Figure 3 presents the XRD patterns of NBA, NS, NT and NST samples. The results show that all samples are mainly composed of the Ni3Al phase, which is the main component of the matrix materials. At the same time, a Ti3SiC2 phase can be found in the NT and NST samples. Ti3SiC2 has a high melting point and high-temperature chemical stability [25], which ensures its stability in the samples' preparation process. The lubricating phases of Sn, Ag and Cu can be found in the NS and NST samples. X-ray diffraction (XRD; D/MAX-RB RU-200B, Rigaku, Tokyo, Japan) was used to identify the phase constitutions of the NBA, NS, NT and NST. The microhardness of each sample was obtained by an HVS-1000 Vickers hardness tester (Beijing times peak Technology Co.Ltd., Beijing, China) with a load of 1 kg and a dwell time of 8 s. The morphologies of the worn surfaces of the NBA, NS, NT and NST were investigated by an electron probe microanalyser (EPMA; JAX-8230, JEOL Ltd., Tokyo, Japan). The elemental compositions of the worn surfaces were acquired using an energy-dispersive spectroscopy (EDS; GENESIS 7000, JEOL Ltd., Japan). To analyze the phase composition of the worn surface, a Raman spectrum (InVia, Renishaw, Gloucester, UK) analysis was performed. The method of cooling fracture was adopted to obtain the cross-section structures of wear scars. The as-prepared samples were incised down to a residual thickness of about 1-1.5 mm at the relative side of the wear scars. After being incised, the samples were cooled for 30 min using liquid nitrogen. The cooled samples were broken by the low shearing force in a dust-free environment. The cross-sectional morphologies of the NBA and NST were characterized using scanning electron microscopy (SEM; JSM-IT300, JEOL Ltd., Japan). Figure 3 presents the XRD patterns of NBA, NS, NT and NST samples. The results show that all samples are mainly composed of the Ni 3 Al phase, which is the main component of the matrix materials. At the same time, a Ti 3 SiC 2 phase can be found in the NT and NST samples. Ti 3 SiC 2 has a high melting point and high-temperature chemical stability [25], which ensures its stability in the samples' preparation process. The lubricating phases of Sn, Ag and Cu can be found in the NS and NST samples.  Figure 4 shows the friction coefficients and wear rates of NBA, NS, NT and NST sliding against Si3N4 ball at 12 N-0.2 m/s for 60 min at different temperatures. As presented in   Figure 4 shows the friction coefficients and wear rates of NBA, NS, NT and NST sliding against Si 3 N 4 ball at 12 N-0.2 m/s for 60 min at different temperatures. As presented in Figure 4a, the friction coefficient of each sample decreases from 20 to 400 • C. At 400 • C, the friction coefficient of NST is 0.22, which is similar to that of NS. As the temperature increases to 800 • C, the friction coefficient of NST increases to 0.29, which is similar to that of NT. As presented in Figure 4b, the wear rate of each sample decreases from 20 to 400 • C. At 400 • C, the wear rate of NST is 6.2 × 10 −6 mm 3 N −1 m −1 , which is similar to that of NS. At 600 and 800 • C, the wear rate of NST increases to 8.7 × 10 −6 and 1.25 × 10 −5 mm 3 N −1 m −1 , respectively, which is similar to that of NT. Compared with NBA, NS and NT, NST shows lower friction coefficients (0.22-0.29) and wear rates (0.62-1.25 × 10 −5 mm 3 N −1 m −1 ) from 20 to 800 • C due to the synergistic action mechanism of Sn-Ag-Cu and Ti 3 SiC 2 on the crack self-healing.  Figure 4 shows the friction coefficients and wear rates of NBA, NS, NT and NST sliding against Si3N4 ball at 12 N-0.2 m/s for 60 min at different temperatures. As presented in Figure 4a, the friction coefficient of each sample decreases from 20 to 400 °C. At 400 °C, the friction coefficient of NST is 0.22, which is similar to that of NS. As the temperature increases to 800 °C, the friction coefficient of NST increases to 0.29, which is similar to that of NT. As presented in Figure 4b, the wear rate of each sample decreases from 20 to 400 °C. At 400 °C, the wear rate of NST is 6.2 × 10 −6 mm 3 N −1 m −1 , which is similar to that of NS. At 600 and 800 °C, the wear rate of NST increases to 8.7 × 10 −6 and 1.25 × 10 −5 mm 3 N −1 m −1 , respectively, which is similar to that of NT. Compared with NBA, NS and NT, NST shows lower friction coefficients (0.22-0.29) and wear rates (0.62-1.25 × 10 −5 mm 3 N −1 m −1 ) from 20 to 800 °C due to the synergistic action mechanism of Sn-Ag-Cu and Ti3SiC2 on the crack self-healing.  Figure 5 shows the dynamic friction coefficients of NST varying with the sliding time at 200, 400, 600 and 800 °C. The fluctuations in the friction coefficients with the sliding time at 400 and 600 °C are more stable than those obtained at 200 and 800 °C, due to the excellent crack self-healing properties of NST at 400 and 600 °C, which improves the tribological performances of the NST. Moreover, the testing temperatures have a certain influence on the duration of the running-in process of NST. Compared with other testing temperatures, the duration of the running-in process of NST at 400 °C is shorter, which can be attributed to the formation of a more stable solid lubricating film on the friction contact surface of NST within a shorter friction time.  Figure 5 shows the dynamic friction coefficients of NST varying with the sliding time at 200, 400, 600 and 800 • C. The fluctuations in the friction coefficients with the sliding time at 400 and 600 • C are more stable than those obtained at 200 and 800 • C, due to the excellent crack self-healing properties of NST at 400 and 600 • C, which improves the tribological performances of the NST. Moreover, the testing temperatures have a certain influence on the duration of the running-in process of NST. Compared with other testing temperatures, the duration of the running-in process of NST at 400 • C is shorter, which can be attributed to the formation of a more stable solid lubricating film on the friction contact surface of NST within a shorter friction time.  Figure 6 presents the worn surface morphologies of NBA, NS, NT and NST at 400 °C. As presented in Figure 6a, obvious furrows and some cracks indicate that the main wear mechanisms of NBA at 400 °C are a mixture of abrasive wear and fatigue wear [27]. As presented in Figure 6c, obvious spalling and cracks indicate that the main wear mechanism of NT at 400 °C is fatigue wear [27]. As presented in Figure 6b,d, a relatively complete   mechanisms of NBA at 400 • C are a mixture of abrasive wear and fatigue wear [27]. As presented in Figure 6c, obvious spalling and cracks indicate that the main wear mechanism of NT at 400 • C is fatigue wear [27]. As presented in Figure 6b,d, a relatively complete lubrication film and a few cracks appear on the worn surfaces of NS and NST. Figure 6e,f shows the EDS results of the areas marked by boxes A and B in Figure 6d. The element contents of O, Sn and Ag in the crack-healing region B are obviously higher than those of region A at the edge of the worn surface of NST. This demonstrates that the Sn-Ag-Cu flows into the crack and is partially oxidized at 400 • C, which can promote the crack self-healing of NST.   Figure 7a,b, obvious spalling and some cracks indicate that the main wear mechanisms of NBA and NS at 600 °C are fatigue wear [27]. As presented in Figure 7c,d, relatively complete lubrication film and fine cracks can be observed on the worn surfaces of NT and NST. At 600 °C, the anti-friction performance of the worn surfaces of NT and NST may be attributed to the slippage between the layered structures of Ti3SiC2, which can contribute to the dispersal of shear stress and the formation of a solid lubrication film [19]. The major wear mechanisms of NT and NST are plastic deformation and slight oxidative wear [24]. At 600 °C, the oxidized layer can reduce the direct contact between the friction pairs, providing an excellent self-lubricating effect [8]. Figure 7e,f shows the EDS results of the areas marked by boxes A and B in Figure 7d. The element contents of O, Ti and Si in the crack healing region B are obviously higher than those of region A at the edge of the worn surface of NST. The differences in element contents can probably be ascribed to the aggregation and oxidation of the Ti3SiC2 with a multilayer structure on the friction contact surface under the action of sliding friction, promoting crack healing and the formation of solid lubrication film of NST.

Self-Healing Behavior and Mechanism
The effect of crack healing of the NST is evaluated by the recovery ratio λ, and λ can be calculated by Equation (1) [28,29].
λ= (1) where WNBA and WNST are the average values of crack widths on the worn surfaces of NBA and NST, respectively.  As presented in Figure 7a,b, obvious spalling and some cracks indicate that the main wear mechanisms of NBA and NS at 600 • C are fatigue wear [27]. As presented in Figure 7c,d, relatively complete lubrication film and fine cracks can be observed on the worn surfaces of NT and NST. At 600 • C, the anti-friction performance of the worn surfaces of NT and NST may be attributed to the slippage between the layered structures of Ti 3 SiC 2 , which can contribute to the dispersal of shear stress and the formation of a solid lubrication film [19]. The major wear mechanisms of NT and NST are plastic deformation and slight oxidative wear [24]. At 600 • C, the oxidized layer can reduce the direct contact between the friction pairs, providing an excellent self-lubricating effect [8]. The average crack widths on the worn surfaces of NBA, NS, NT and NST are listed in Table 4. At 400 °C, the recovery ratios relative to NBA of the cracks on the worn surfaces of NS, NT and NST are about 73.2, 40.8 and 76.4%, respectively. The crack recovery ratios of NS and NST are close at 400 °C. In addition, at 600 °C, the recovery ratios of the cracks on the worn surfaces of NS, NT and NST are about 34.2, 77.3 and 75.4%, respectively. The crack recovery ratios of NT and NST are close at 600 °C. It can be concluded that the additions of Sn-Ag-Cu and Ti3SiC2 to the NST play a significant role in the crack self-healing that occurs at 400 and 600 °C, respectively.  The effect of crack healing of the NST is evaluated by the recovery ratio λ, and λ can be calculated by Equation (1) [28,29].
where W NBA and W NST are the average values of crack widths on the worn surfaces of NBA and NST, respectively. The average crack widths on the worn surfaces of NBA, NS, NT and NST are listed in Table 4. At 400 • C, the recovery ratios relative to NBA of the cracks on the worn surfaces of NS, NT and NST are about 73.2, 40.8 and 76.4%, respectively. The crack recovery ratios of NS and NST are close at 400 • C. In addition, at 600 • C, the recovery ratios of the cracks on the worn surfaces of NS, NT and NST are about 34.2, 77.3 and 75.4%, respectively. The crack recovery ratios of NT and NST are close at 600 • C. It can be concluded that the additions of Sn-Ag-Cu and Ti 3 SiC 2 to the NST play a significant role in the crack self-healing that occurs at 400 and 600 • C, respectively.  Figure 8 presents the worn surface morphologies of NST at 200 and 800 • C. As shown in Figure 8a, obvious furrows and some cracks can be observed at 200 • C, which results in an increase in the surface roughness and frictional resistance of the worn surface of NST [22]. The main wear mechanism of NST at 200 • C is abrasive wear [27]. As presented in Figure 8b, obvious spalling and oxides indicate that the main wear mechanisms of NST at 800 • C are adhesive wear and oxidative wear [24]. As the temperature increases to 800 • C, the loose oxidative layer results in a rough worn surface, which is consistent with the high wear rate of oxidation wear [30]. The EDS result shown in Figure 8d also confirms that the O content of the worn surface material of NST is higher at 800 • C compared with other testing temperatures. At 800 • C, a lubricating film with rich multi-metal oxides is formed due to the high-temperature oxidation, which plays an important role in anti-friction and wear resistance during high-temperature friction [31]. In addition, excessive oxidation leads to the spalling of the lubricating film under cyclic friction contact stress at 800 • C, which will increase the wear rate of NST. O content of the worn surface material of NST is higher at 800 °C compared with other testing temperatures. At 800 °C, a lubricating film with rich multi-metal oxides is formed due to the high-temperature oxidation, which plays an important role in anti-friction and wear resistance during high-temperature friction [31]. In addition, excessive oxidation leads to the spalling of the lubricating film under cyclic friction contact stress at 800 °C, which will increase the wear rate of NST. Figure 9 presents the typical worn surface morphologies of Si3N4 balls against the NST at 200, 400, 600 and 800 °C. As presented in Figure 9a, some furrows are visible on the worn surface of Si3N4 ball at 200 °C, indicating that the main wear mechanism is abrasive wear at 200 °C. As presented in Figure 9b, some flaky transfer film can be seen on the worn surface of Si3N4 ball at 400 °C. The transfer film produced by the NST during dry friction can play an antifriction role [32]. As presented in Figure 9d, a lot of wear debris can be found on the worn surface of Si3N4 ball at 800 °C. As the testing temperature increases to 800 °C, due to the excessive oxidation of the worn surface material, the lubrication film is easy to flake off under cyclic friction contact stress, resulting in a lot of wear debris adhering to the worn surface of the Si3N4 ball.   Figure 9 presents the typical worn surface morphologies of Si 3 N 4 balls against the NST at 200, 400, 600 and 800 • C. As presented in Figure 9a, some furrows are visible on the worn surface of Si 3 N 4 ball at 200 • C, indicating that the main wear mechanism is abrasive wear at 200 • C. As presented in Figure 9b, some flaky transfer film can be seen on the worn surface of Si 3 N 4 ball at 400 • C. The transfer film produced by the NST during dry friction can play an antifriction role [32]. As presented in Figure 9d, a lot of wear debris can be found on the worn surface of Si 3 N 4 ball at 800 • C. As the testing temperature increases to 800 • C, due to the excessive oxidation of the worn surface material, the lubrication film is easy to flake off under cyclic friction contact stress, resulting in a lot of wear debris adhering to the worn surface of the Si 3 N 4 ball.  Figure 10 shows the Gibbs free energy (ΔG°) used to form the oxides, which can be used to determine the precedence of oxidation of NST during sliding friction [2]. It can be seen that the Gibbs free energy of Al used to form the Al2O3 is the lowest. Therefore, under low and moderate temperatures, it can be inferred that the preferred oxides are mainly Al2O3, followed by SnO2. In addition, it can be deduced that the oxides preferentially formed at high temperatures are mainly Al2O3, followed by TiO2 and SiO2. The prediction of the oxidation sequence of the main elements in NST shows the selective oxidation of Al2O3, SnO2, TiO2 and SiO2, as demonstrated by the XRD results of worn surfaces of NST at 400 and 600 °C, as presented in Figure 11. The XRD results show that there are some oxides of Ni2O3, Al2O3, SnO2 and CuO at 400 °C. At 600 °C, the main oxides are Al2O3, SnO2, TiO2, SiO2, NiO and NiAl2O4. The oxides generated by partial oxi-  Figure 10 shows the Gibbs free energy (∆G • ) used to form the oxides, which can be used to determine the precedence of oxidation of NST during sliding friction [2]. It can be seen that the Gibbs free energy of Al used to form the Al 2 O 3 is the lowest. Therefore, under low and moderate temperatures, it can be inferred that the preferred oxides are mainly Al 2 O 3 , followed by SnO 2 . In addition, it can be deduced that the oxides preferentially formed at high temperatures are mainly Al 2 O 3 , followed by TiO 2 and SiO 2 .  Figure 10 shows the Gibbs free energy (ΔG°) used to form the oxides, which can be used to determine the precedence of oxidation of NST during sliding friction [2]. It can be seen that the Gibbs free energy of Al used to form the Al2O3 is the lowest. Therefore, under low and moderate temperatures, it can be inferred that the preferred oxides are mainly Al2O3, followed by SnO2. In addition, it can be deduced that the oxides preferentially formed at high temperatures are mainly Al2O3, followed by TiO2 and SiO2. The prediction of the oxidation sequence of the main elements in NST shows the selective oxidation of Al2O3, SnO2, TiO2 and SiO2, as demonstrated by the XRD results of worn surfaces of NST at 400 and 600 °C, as presented in Figure 11. The XRD results show that there are some oxides of Ni2O3, Al2O3, SnO2 and CuO at 400 °C. At 600 °C, the main  The prediction of the oxidation sequence of the main elements in NST shows the selective oxidation of Al 2 O 3 , SnO 2 , TiO 2 and SiO 2 , as demonstrated by the XRD results of worn surfaces of NST at 400 and 600 • C, as presented in Figure 11. The XRD results show that there are some oxides of Ni 2 O 3 , Al 2 O 3 , SnO 2 and CuO at 400 • C. At 600 • C, the main oxides are Al 2 O 3 , SnO 2 , TiO 2 , SiO 2 , NiO and NiAl 2 O 4 . The oxides generated by partial oxidation of the worn surface material of NST at 400 and 600 • C can contribute to crack self-healing. In addition, during high-temperature friction, the tribochemistry reactions of the solid lubricants produce various oxides with a lubrication effect on the worn surface, which have good anti-friction effects [33]. In addition, TiC and TiO 2 with high hardness can reinforce the lubricating film of NST [34,35], improving the wear resistance of NST at high temperatures. Furthermore, as shown in Figure 10, the SnO 2 , CuO, TiO 2 and Al 2 O 3 have a higher elastic modulus when compared with the NST matrix, which can prevent the premature fracture or spalling of the solid lubrication film [36]. Relevant research [37,38] also showed that these compounds had a good anti-friction effect under high temperatures, which would reduce the friction coefficient of NST during sliding friction. Relevant studies have shown that materials with crack self-healing properties need to exhibit fluidity to cracks and adhesion to crack surfaces to achieve crack-filling [39]. Therefore, it can be inferred that the oxidation of Sn, Cu and Ti3SiC2 may be a vital reason for the self-healing behavior of cracks. The chemical equations for calculating the relative volume expansion generated by the generation of principal oxides are as follows: Ti3SiC2 + 6O2→3TiO2 + SiO2 + 2CO2 (4) The relative volume expansions generated by the oxidation of Sn, Cu and Ti3SiC2 are 32.9%, 77.8% and 93.4%, respectively. This confirms that the formation of oxides such as SnO2, CuO, TiO2 and SiO2 promotes the self-healing of NST by filling the cracks. Figure 12 presents the Raman spectra of the worn surfaces of NST at 400 and 600 °C. As shown in Figure 12a, at 400 °C, the main oxides of Al2O3, SnO2, CuO and Ni2O3 are found on the worn surface of NST at 400 °C, in agreement with the XRD results. It can be concluded that the lubricating phase Sn-Ag-Cu is partially oxidized at 400 °C, which is helpful for the crack self-healing of NST. As shown in Figure 12b, rich oxides consisting of Al2O3, SnO2, CuO, TiO2 and SiO2, NiO and NiAl2O4 are formed at 600 °C. During the high-temperature friction, the Al element in the NST preferentially oxidized to Al2O3, which has a certain anti-wear effect at high temperatures [31]. These oxides promote crack Relevant studies have shown that materials with crack self-healing properties need to exhibit fluidity to cracks and adhesion to crack surfaces to achieve crack-filling [39]. Therefore, it can be inferred that the oxidation of Sn, Cu and Ti 3 SiC 2 may be a vital reason for the self-healing behavior of cracks. The chemical equations for calculating the relative volume expansion generated by the generation of principal oxides are as follows: Ti 3 SiC 2 + 6O 2 →3TiO 2 + SiO 2 + 2CO 2 (4) V R/Ti 3 SiC 2 = 3V TiO 2 + V SiO 2 − V Ti 3 SiC 2 V Ti 3 SiC 2 = (3M TiO 2 × ρ SiO 2 + M SiO 2 × ρ TiO 2 ρ Ti 3 SiC 2 ρ TiO 2 × ρ SiO 2 ×M Ti 3 SiC 2 − 1 = 93.4% (7) The relative volume expansions generated by the oxidation of Sn, Cu and Ti 3 SiC 2 are 32.9%, 77.8% and 93.4%, respectively. This confirms that the formation of oxides such as SnO 2 , CuO, TiO 2 and SiO 2 promotes the self-healing of NST by filling the cracks. Figure 12 presents the Raman spectra of the worn surfaces of NST at 400 and 600 • C. As shown in Figure 12a, at 400 • C, the main oxides of Al 2 O 3 , SnO 2 , CuO and Ni 2 O 3 are found on the worn surface of NST at 400 • C, in agreement with the XRD results. It can be concluded that the lubricating phase Sn-Ag-Cu is partially oxidized at 400 • C, which is helpful for the crack self-healing of NST. As shown in Figure 12b, rich oxides consisting of Al 2 O 3 , SnO 2 , CuO, TiO 2 and SiO 2 , NiO and NiAl 2 O 4 are formed at 600 • C. During the high-temperature friction, the Al element in the NST preferentially oxidized to Al 2 O 3 , which has a certain anti-wear effect at high temperatures [31]. These oxides promote crack self-healing during sliding friction, thus improving the tribological properties of NST from 20 to 800 • C. In addition, Figure 13 presents the representative cross-sectional morphologies of NBA and NST at 400 and 600 °C. As shown in Figure 13a,c, no obvious solid lubricating film can be seen in the cross-section of NBA. Some cracks with average widths of about 10.9 and 35.6 nm can be seen in the cross-sections of NBA at 400 and 600 °C, respectively. As shown in Figure 13b,d, obvious solid lubricating films can be observed in the crosssection of NST. A few fine cracks with average widths of about 3.2 and 5.9 nm can be seen in the cross-sections of NST at 400 and 600 °C, respectively. Some self-healing areas can be seen at the ends of the cracks on the cross-sections of NST. As shown in Table 5, the recovery ratios relative to NBA of the cracks on the cross-sections of NST at 400 and 600 °C are approximately 70.6% and 83.4%, respectively. Figure 14 shows the EDS profiles of the the regions marked in boxes in Figure 13b,d. Positions A and C are located in the matrix of NST. Positions B and D are located in the crack self-healing areas. As presented in Figure 14a,b, the element contents of Sn, Cu and O in position B are higher than those in position A. This suggests that Sn-Ag-Cu flows into the crack and is easy to oxidize at 400 °C, promoting the crack self-healing of NST. As presented in Figure 14c,d, the element contents of Ti, Si and O in position D are higher than those in position C. The EDS results further confirm the thermal decomposition and oxidation of Ti3SiC2 at 600 °C, which significantly contribute to the crack self-healing property of NST. In addition, Figure 13 presents the representative cross-sectional morphologies of NBA and NST at 400 and 600 • C. As shown in Figure 13a,c, no obvious solid lubricating film can be seen in the cross-section of NBA. Some cracks with average widths of about 10.9 and 35.6 nm can be seen in the cross-sections of NBA at 400 and 600 • C, respectively. As shown in Figure 13b,d, obvious solid lubricating films can be observed in the cross-section of NST. A few fine cracks with average widths of about 3.2 and 5.9 nm can be seen in the cross-sections of NST at 400 and 600 • C, respectively. Some self-healing areas can be seen at the ends of the cracks on the cross-sections of NST. As shown in Table 5, the recovery ratios relative to NBA of the cracks on the cross-sections of NST at 400 and 600 • C are approximately 70.6% and 83.4%, respectively. Figure 14 shows the EDS profiles of the the regions marked in boxes in Figure 13b,d. Positions A and C are located in the matrix of NST. Positions B and D are located in the crack self-healing areas. As presented in Figure 14a,b, the element contents of Sn, Cu and O in position B are higher than those in position A. This suggests that Sn-Ag-Cu flows into the crack and is easy to oxidize at 400 • C, promoting the crack self-healing of NST. As presented in Figure 14c,d, the element contents of Ti, Si and O in position D are higher than those in position C. The EDS results further confirm the thermal decomposition and oxidation of Ti 3 SiC 2 at 600 • C, which significantly contribute to the crack self-healing property of NST. trix of NST. Positions B and D are located in the crack self-healing areas. As presented in Figure 14a,b, the element contents of Sn, Cu and O in position B are higher than those in position A. This suggests that Sn-Ag-Cu flows into the crack and is easy to oxidize at 400 °C, promoting the crack self-healing of NST. As presented in Figure 14c,d, the element contents of Ti, Si and O in position D are higher than those in position C. The EDS results further confirm the thermal decomposition and oxidation of Ti3SiC2 at 600 °C, which significantly contribute to the crack self-healing property of NST.       Figure 15 presents the schematic diagrams of the crack self-healing of wear scar of NST during sliding friction from 20 to 400 • C, as well as higher temperatures of 600 and 800 • C. As shown in Figure 15a, at low and moderate temperatures, Sn-Ag-Cu melts and flows into the cracks during sliding friction. Meanwhile, the cracks are gradually filled with the formation of rich oxides, thus promoting self-healing of the NST. As shown in Figure 15b, at higher temperatures of 600 and 800 • C, Ti 3 SiC 2 on the subsurface of the wear scar plays a significant role in supporting the solid lubricating film of the NST [11]. The synergistic effects of the enhancement of Ti 3 SiC 2 , Al 2 O 3 and SiO 2 and the lubrication of SnO 2 and TiO 2 are conducive to forming a stable lubricating film [37]. In addition, under high-temperature friction, the cracks are filled by the oxides due to the partial decomposition and oxidation of Ti 3 SiC 2 , promoting the crack self-healing of NST. Figure 15c shows the evolution of various oxides in the solid lubrication film during the dry sliding friction of NST against the Si 3 N 4 ball from 20 to 800 • C. The composition of the oxides varies with temperature, which is related to the Gibbs free energy of the various oxides. The oxides generated on the worn surface of NST mainly include Al 2 O 3 , SnO 2 , Ni 2 O 3 and CuO from 20 to 400 • C. As the temperature rises from 400 to 800 • C, the oxide Al 2 O 3 forms, together with SnO 2 , CuO, TiO 2 , SiO 2 , NiO and NiAl 2 O 4 . These rich oxides can enhance the anti-friction and wear resistance of NST [40]. In brief, the synergistic action mechanisms of Sn-Ag-Cu and Ti 3 SiC 2 regarding crack self-healing from 20 to 800 • C play a significant role in forming a stable solid lubricating film, improving the anti-friction and wear resistance of NST. generated on the worn surface of NST mainly include Al2O3, SnO2, Ni2O3 and CuO from 20 to 400 °C. As the temperature rises from 400 to 800 °C, the oxide Al2O3 forms, together with SnO2, CuO, TiO2, SiO2, NiO and NiAl2O4. These rich oxides can enhance the antifriction and wear resistance of NST [40]. In brief, the synergistic action mechanisms of Sn-Ag-Cu and Ti3SiC2 regarding crack self-healing from 20 to 800 °C play a significant role in forming a stable solid lubricating film, improving the anti-friction and wear resistance of NST.

Conclusions
In this paper, to meet the increasing demand for the metal matrix composites with excellent tribological performance over a wide temperature range, the tribological behavior and self-healing properties of NST were studied from 20 to 800 °C. The main conclusions are as follows: (1) The tribological behaviors of NST are strongly dependent on the testing temperature and self-healing properties. Compared with NBA, NS and NT, NST shows lower friction coefficients (0.22-0.29) and wear rates (0.62-1.25 × 10 −5 mm 3 N −1 m −1 ) from 20 to 800 °C.
(2) At low and moderate temperatures from 20 to 400 °C, as the Sn-Ag-Cu flows into the cracks and is oxidized during sliding friction, the cracks on the worn surfaces are filled with the oxides consisting mainly of Al2O3, SnO2 and CuO, promoting the self-healing of the NST. Compared with other testing temperatures, the recovery ratio relative to NBA of the cracks on the worn surface of NST is the highest at 400 °C, which is about 76.4%.
(3) At higher temperatures of 600 and 800 °C, the cracks are filled by the oxides consisting mainly of Al2O3, TiO2 and SiO2 due to the partial decomposition and oxidation of Ti3SiC2, which will be conducive to the self-healing of the NST during sliding friction.
(4) The synergistic action mechanisms of Sn-Ag-Cu and Ti3SiC2 on crack self-healing from 20 to 800 °C play a significant role in forming a stable solid lubricating film on the worn surface, improving the anti-friction and wear resistance of NST.

Conclusions
In this paper, to meet the increasing demand for the metal matrix composites with excellent tribological performance over a wide temperature range, the tribological behavior and self-healing properties of NST were studied from 20 to 800 • C. The main conclusions are as follows: (1) The tribological behaviors of NST are strongly dependent on the testing temperature and self-healing properties. Compared with NBA, NS and NT, NST shows lower friction coefficients (0.22-0.29) and wear rates (0.62-1.25 × 10 −5 mm 3 N −1 m −1 ) from 20 to 800 • C.
(2) At low and moderate temperatures from 20 to 400 • C, as the Sn-Ag-Cu flows into the cracks and is oxidized during sliding friction, the cracks on the worn surfaces are filled with the oxides consisting mainly of Al 2 O 3 , SnO 2 and CuO, promoting the self-healing of the NST. Compared with other testing temperatures, the recovery ratio relative to NBA of the cracks on the worn surface of NST is the highest at 400 • C, which is about 76.4%.
(3) At higher temperatures of 600 and 800 • C, the cracks are filled by the oxides consisting mainly of Al 2 O 3 , TiO 2 and SiO 2 due to the partial decomposition and oxidation of Ti 3 SiC 2 , which will be conducive to the self-healing of the NST during sliding friction.
(4) The synergistic action mechanisms of Sn-Ag-Cu and Ti 3 SiC 2 on crack self-healing from 20 to 800 • C play a significant role in forming a stable solid lubricating film on the worn surface, improving the anti-friction and wear resistance of NST.

Data Availability Statement:
The data presented in this study are available on request from the corresponding author.