In the age of rapid technological advancements in engineering sectors, the production systems are continuously evolving to meet the complex challenges of the present day. Such advancements are raising the robustness, quality and performance barriers of the production systems and of the products due that have to operate under extreme conditions. Among the extreme operating conditions, high temperature environments are considered the most critical in industries as metal forming, aerospace, advanced automotive and power generation to name a few (Rahman et al., 2018). Depending upon the applications, the operating temperature of a given manufactured part may range up to 500°C and in some cases up to 1,000°C. These elevated temperatures (often coupled with thermal fatigue) can have detrimental effects not only on the mechanical properties of the materials but also their surface morphology. This in turn can affect the friction, wear and lubrication characteristics of materials (Semenov, 1995). The harsh operating conditions and complexity of the mechano-chemical processes involved offer a great challenge from the perspective of material design, manufacturing and surface engineering of the industrial production systems and the products.

High temperature tribological processes are extremely complex in nature due to simultaneous interaction of multiple variables involving; thermal softening, surface morphological changes due to oxidation and diffusion, and surface degradation due to thermo-mechanical fatigue and wear (Hardell et al., 2015). Material design and development for high temperature tribological contacts therefore involves the integration of complex chemical compositions with the addition of lubrication media, in order to achieve optimal hardness, toughness, thermal stability, friction and wear (Matthews et al., 2007). Conventionally, thin (few microns thick) wear resistant coatings are produced by thermally activated chemical vapor deposition (CVD), plasma assisted physical vapor deposition (PA-PVD) and pulsed laser deposition (PLD) techniques to improve the tribological performance for various high temperature applications (Mayrhofer et al., 2006). However, the current industrial production focus is not only to address the extreme temperature environments, but also to enhance the product service life alongside taking into account the economic and environmental aspects in single-step processes. This requires development of new materials with enhanced properties and the utilization of advanced and intelligent production techniques (Singh et al., 2017).

Laser-based additive manufacturing (LBAM) is a family of advanced production systems, use to fabricate metal parts, complete functional and functionally graded products (Li et al., 2017; Loh et al., 2018; Ocelík and De Hosson, 2018), see Figure 1. LBAM has revolutionized the manufacturing industry; from concept development to innovative production of application-specific optimized designs (Herzog et al., 2016; Bandyopadhyay and Traxel, 2018; DebRoy et al., 2018). In LBAM, production is carried out by a powder blown system; laser metal deposition (LMD) (Thompson et al., 2015) and laser engineered net shaping (LENS) (Dobbelstein et al., 2018), powder bed fusion system; selective laser melting (SLM) (Zhou Y. H. et al., 2018), and wire-feed system; wire-laser additive manufacturing (WLAM) (Ding et al., 2015). In the powder blown systems, the powder is injected into the laser induced melt pool by a single or multiple nozzles. SLM is a powder bed fusion system, whereby the powder bed is exposed to a single or multiple high energy laser beams, to produce complex parts layer by layer (Parry et al., 2016). In the wire-feed systems (WLAM), wire is used instead of powder to produce the metal components and a laser beam is used as the energy source (Ding et al., 2015). Figure 1 provides an overview of LBAM production systems.

In LBAM, the production is either limited to the development of thin or thick coatings on a substrate (LMD) or manufacturing a full functional metallic product (SLM). In all cases, production through LBAM requires optimization of set of the processing parameters, to avoid defects, such as porosity, pin-hole voids, unmelted powder, micro-cracks and high dilution with the substrate. The primary parameters are laser power, laser scan speed, powder mass flow rate and track overlap or hatch spacing (Yap et al., 2015). LBAM provides freedom of process optimization through on-line process monitoring and in-line quality control. Due to viability of improved mechanical properties, convenience in fabricating intricate products with limited distortion of the product and substrate, strong metallurgical bonding with the substrate, limited HAZ and dilution, LBAM is considered a highly preferable production method over conventional means (Birger et al., 2011; Gibson et al., 2015).

For environmental protection and reduction in CO₂ emission, industrial coating applications like hard chrome plating requires replacement and for that purpose thermal spraying and LMD are the potential candidates (Schopphoven et al., 2016). However, LMD is a far better establish industrial application option than thermal spraying as thermal spraying exhibits poor mechanical bonding with the substrate with the porosity up to 1–2% and is difficult to repair (Schopphoven et al., 2016). Irrespective of the material, due to rapid solidification during LBAM processes, the resulting microstructure is usually fine grain. Cooling rates are faster in the powder bed fusion system compared to those of powder blown systems. LBAM leads to the formation of meta-stable microstructures and non-equilibrium compositions of the resulting phases (Herzog et al., 2016). Trosch et al. (2016) provide a comparison between the microstructures and associated grain sizes of Ni based super alloy (IN 718) produced by SLM, casting and forging. SLM fabrication provided a highly refined compared to the rest. LBAM coupled with CAD-CAM systems has the ability of producing complex shapes in a single production process. This reduces the number of stages within the production cycle, such as turning, milling, drilling and tooling which results in low investment for machinery systems and manpower (Murr et al., 2009; Wang and Ku, 2009). Table 1 lists the advantages of the LBAM processes over established conventional production methods and also lists the current and future challenges to its wider adoption and the further development.

Under vacuum or extreme temperature conditions, the use of liquid lubricants (oils and greases) is not always possible or desired. As an alternative, solid lubricants and self-lubricating materials can be utilized to modify the friction and wear in temperature-specific environments (high or cryogenic temperatures) (Donnet and Erdemir, 2004). Solid lubricants are solid materials having low shear strength (Holmberg and Matthews, 2009), and can be added to bulk materials or coatings to lower the friction and wear of the tribological contacts. Alexeyev and Jahanmir (1993) describe the working mechanism of the solid lubricants. An important factor is that solid lubricants deform during sliding and squeeze outward to the counter surface forming a soft interfacial film. Scharf and Prasad (2013) also state that tribological contacts in the presence of solid lubricants, results in the transfer of a thin tribo-film to the counter surface.

In order to enhance the service life of the lubricated contacts, continuous provision of solid lubricants is required. It is essential to maintain an equal percentage of the solid lubricants throughout the service life of the composite materials to exhibit a consistent tribological performance. In the case that one of the contact partners is continuously replaced, like in manufacturing, the use of embedded solid lubricant therefore lead to depletion of the material which contains solid lubricants. Also, in order to maintain a thin film on the surface, generation and supply of the soft phase should balance the consumption of soft phase in the contact (Song et al., 2010). For example in hot rolling, in case of spun cast work roll of indefinite chilled double pour (ICDP) iron material, free graphite present in the microstructure acts as a solid lubricant. Due to intrinsic limitations of the casting process, the percentage fraction of graphite across the work roll shell radius is not homogenously distributed (Luc et al., 2015). As a result the wear performance and mechanical strength are affected. Due to production limitations of conventional processes, LBAM becomes an attractive manufacturing technology, ensuring the homogenous distribution of alloying constituents by precisely tailoring the processing conditions. In LBAM, a variety of solid lubricants can be mixed with the base materials in the form of powders; hence providing freedom to develop application-specific materials (Torres et al., 2017).

A generic classification of the solid lubricants is shown in Figure 2 (left) (Furlan et al., 2018). A production flow diagram is also shown in Figure 2 (right), describing an advanced application-specific production approach based on design of materials with or without addition of solid lubricants, with the utilization of LBAM for high temperature tribological processes.

Quazi et al. (2016) state that solid lubricants, used in additive manufacturing, can be classified in three groups. The first group consists of lamellar structured materials, graphite, transition metal dichalcogenides (TMDs) compounds (MoS₂ and WS₂) and hexagonal boron nitride (hBN). The second group covers soft metals (e.g., Ag, Cu, and Sn) while the third group is comprised of metal-oxide-fluorides (e.g., CaF₂ and BaF₂). At elevated temperatures (above 500°C) lamellar-structure and soft metal based solid lubricants become ineffective due to their thermal decomposition, structural degradation and oxidation. Erdemir (2000) describes the lubricious aspect of the metal-oxides and metalloids at high temperatures. In the metal forming industry, characteristics of the metal-oxides are found to be either abrasive or lubricious. Magnetite (Fe₃O₄), molybdenum oxide (MoO₃), vanadium oxide (V₂O₅), and tungsten oxide (WO₃) are considered as lubricious oxides with weak cohesive bonds (Dohda et al., 2015).

The current paper is focused to provide a comprehensive review of the available literature for the design of materials for high temperature tribological applications, while considering the incorporation of lubricating phase, followed by manufacturing through LBAM production systems. High temperature tribological characteristics of such fabricated coatings and products are discussed. In order to enhance the clarity of the paper, specific applications are addressed with a focus on the metal forming industry (hot rolling, hot stamping, molding and forging) in section Metal Forming, while advanced automotive (engine), aerospace and power generation (nuclear energy) applications are addressed in section Aerospace, Automotive, and Power Generation. Emerging materials, which are promising candidates for new applications are addressed in section Emerging Materials.

In the metal forming industry, components (e.g., work rolls, tools, molds, and dies) are subjected to extremely high thermal (up to 1,200°C in hot extrusion) and mechanical (>1.0 GPa) dynamic loads, which result in wear, fatigue and plastic deformation (Kashani et al., 2007; Birol, 2010). The hot metal forming operations involve multiple transient thermal cycles of varying time durations, which inflict a great challenge to the integrity of the tool and product in terms of dimensional stability and surface finish. Wan et al. (2016) consider surface lubrication as the prime area of optimization in the metal forming for quality production and robustness of the production system.

In the extreme working conditions, simultaneous interactions of various wear mechanisms determine the wear behavior of metal forming components (MFCs). The wear mechanisms are abrasion, adhesion, tribo-oxidation and surface fatigue (Ilo et al., 2011). During the contact with the product, the MFCs surface often heats up from room temperature to 500–600°C (due to conduction, deformation and friction) and is subsequently cooled down by a water spray (Colás et al., 1999). The cyclic fatigue due to thermal and mechanical loads promotes compressive stresses during heating, and tensile stresses upon cooling, resulting in degradation of the MFC surface (Fedorciuc–Onisa and Farrugia, 2008; Garza-Montes-de-Oca et al., 2011; Deng et al., 2017). In addition, MFCs also suffer abrasive and oxidative wear. Such wear is the result of a high compressive loads and the slip between the MFCs and the product (Belzunce et al., 2004). The presence of a hard iron oxide layer (≈1,000 HV) on the counter surface continuously abrades the MFCs (Garza-Montes-de-Oca and Rainforth, 2009). MFCs also experience sticking and micro-welding with the product and such adhesion results in surface defects both on the MFCs and the product (Wei et al., 2011).

The tribological behavior of the MFCs has a strong influence on the surface quality of the product and also the life of the MFC. Improving the performance and service life of the MFCs is an important subject for the manufacturer and the metal forming industry, because the MFCs are responsible for the 15% of the overall production cost (Boccalini and Sinatori, 2002). In metal forming industry, the most versatile MFC material is high speed steel due to excellent mechanical properties at high temperatures (Pellizzari et al., 2005, 2009; Aqida et al., 2013). The conventional production of the MFCs is performed by casting, which imposes production limitation on the microstructure and the mechanical properties. That is, slow cooling rates in the casting process results in coarse grain structures and such a microstructure is not effective to the (thermo-mechanical) fatigue stresses to which the MFCs are exposed in the metal forming industry. In the casting process, there is limited freedom on the selection of the shell alloy composition due to compatibility issues of shell-core and also due to segregation of coarse grain boundary carbides.

To overcome the production limitations and to meet the challenges of the metal forming production environment, LBAM offers fabrication and product performance advantages (Nilsson and Olsson, 2013a,b). Due to high cooling rates of LBAM, the microstructure can be much more refined, with higher average matrix-carbides hardness (Sun et al., 2018). Concentrating on LMD, literature shows there to be many possible coating materials for high temperature applications; for example Fe-based alloys, metal silicides, carbides and borides, stellites, superalloys (e.g., Ni- or Co-based) and self-lubricating materials (Leunda et al., 2011; Tuominen et al., 2016; Yao et al., 2018). The conventional processing of these costly alloys is difficult. In most of the cases, laser deposition of these alloys is performed on less expensive low alloy steel substrates. These alloys are reported to exhibit good cladability with low alloy steel substrates (Wang et al., 2006).

By utilizing the 4.0 kW Nd:YAG laser source, a 20 mm thick coatings of high speed steel (HSS) alloy was successfully laser deposited on a 100 mm diameter 42CrMo₄ substrate for fabrication of MFCs (Ur Rahman et al., 2018). See also Figure 3 provides an overview of surface layers developed for and by LBAM. The Figure highlights the layer thicknesses attainable (A), a double layer (B), the limitations - for example the disastrous effect of high thermal residual stresses (C) and the possibilities of the LBAM process to realise 20mm thick tool steel builds (D). The microstructures of the LMD HSS alloys were highly refined with approximate average micro-hardness of 800 HV, are suitable to resist the cyclic thermo-mechanical fatigue (Cong et al., 2018). Figure 4 shows the SEM micrograph of the LMD HSS alloy along with the EDS analysis. The micrographs show the homogenous distribution of the carbides along the grain boundaries and also the presence of nanometer sized carbides within the matrix (Ur Rahman et al., 2019a). The comparative tribological performance of the HSS coatings were tested by using high temperature pin-on-disc tribometer. At room temperature, the LMD HSS coatings showed exceptional tribological performance due to higher micro-hardness when compared to that of cast HSS. At 500°C, the friction and wear were heavily influenced by the microstructural features and oxidation kinetics of laser deposited materials (Hashemi et al., 2017; Ur Rahman et al., 2019a). Figure 5 shows the SEM micrograph of the worn surfaces HSS alloys tested at 500°C. The wear mechanism was found to be the combination of abrasive, adhesive and oxidative wear. Carbide particles were removed during the wear process and metal-oxide-carbide debris were redeposited on the worn surfaces.

In the hot strip mill (HSM), alignment of the rolled material is performed by guiding plates, also known as wear plates. The life time of the guiding plates is limited due to extreme conditions of the HSM, requiring frequent maintenance. Torres et al. (2016a,b) performed high temperature tribological studies (up to 700°C) to find the potential substitution for the reference steel 1.0050. High temperature sliding wear testing was performed on the reference material and three substitute materials gray cast iron, abrasion resistant martensitic grade and Fe-Cr-V hard facing material, where the latter was deposited by LMD. It was found that LMD Fe-Cr-V alloy showed the least wear during the entire temperature range. The lowest wear was attributed due to retention of high hardness at elevated temperatures.

Kazadi et al. (2006) show the potential of using LMD to repair general steel mill components. Specifically they apply LMD coatings to foot rolls of two dimensions (substrate = ST55), descaler cassettes (ST50), foot roll shafts (ST50-2), distance sleeves (ST35) and idler rolls (ST50-2). They performed high-speed laser cladding (processing speed ≈ 3 m/min), to avoid excessive heat input and consequential work piece distortion. Several coatings are used, consisting of 316L austenitic stainless steel (distance sleeve and foot roll shaft), 431 martensitic stainless steel (foot roll 630 mm and Idler sleeve), 60S (descaler cassette) and Diamalloy 1008 (foot roll 300). Unfortunately little or no information is given as regards in-service performance.

Lester et al. (2013) conducted comparative room temperature and high temperature (at 700°C) sliding wear tests for the evaluation of tribological performance of laser fabricated and conventionally manufactured alloys for continuous caster rolls used in the compact strip production (CSP). Room temperature tests were performed for LMD WC and high carbon alloy cast roll steel. It was found that LMD WC showed an excellent wear resistance than cast alloy. For high temperature (at 700°C) tribological tests, LMD Stellite 6 outperformed submerged arc clad martensitic stainless steel.

Ur Rahman et al. (2019b) laser fabricated V-rich HSS alloy by varying the laser processing speed and compared the high temperature friction and wear performance with reference to the cast alloy. Laser processing of V-rich HSS alloy at various laser scan speeds modified the morphology of the VC carbides which play essential part during the wear process. SEM micrographs of the microstructures show that morphology of the VC carbides changes from square and round shape to angular and rod shape, see Figures 6A–C relative to the reference cast alloy (Figure 6D). By reducing the size of the carbides below a critical limit reduced their ability to support the counter surface during the wear process, which resulted an increase in wear. It was also reported that improving the morphology of VC carbides by refining the microstructure as in case of V-rich HSS 10V, resulted in stabilizing the friction profile during wear, see Figure 7.

d'Oliveira et al. (2002) compared the deposition of Stellite 6 (Co-Cr-W-C) by plasma transferred arc (PTA) and LMD on a stainless steel (AISI 304) plate (no substrate pre-heating is mentioned). They (cyclically) soak the coatings after deposition at 1,050°C and retest the coating hardness and structural stability. They show that the micro-hardness of the laser deposits drop after exposure to high temperature whereas a micro-hardness stability is reported for PTA coatings. They recommend that hard-faced components for high temperature applications should be processed to realize the stable microstructures. This can be achieved either by appropriate post-heat treatment after LMD or selecting the adequate coating process. This will reduce the modifications of microstructural features, such as carbides morphology, percentage volume fraction, etc., resulting a stable wear behavior at high temperature and reduction in accelerated degradation of surfaces.

Yang (1999) demonstrate the possibility of using a globular Ni-based alloy precursor (Ni48.1-W16.4-Al9.8-Co8.5-Cr5.1-Mo4.8-Fe4.6+Ti2.7) reinforced with “lumpy” WC particles. They chose a mix of 70% Ni-based powder and 30% WC. No information is given with respect to the initial crystallinity of the WC powder employed. As another variant on Ni-based alloys, Wang et al. have published a number of articles on exploring binary and ternary metal-silicide coatings (Duan and Wang, 2002; Wang and Duan, 2002; Cai et al., 2003; Lu and Wang, 2005; Sheng et al., 2008). Sheng et al. (2008) address the microstructure and high temperature wear behavior of laser deposited Ni-Ti-Si ternary metal-silicide coatings. Due to high micro-hardness and elastic modulus, the metal-silicides generally present good abrasive wear resistance. Ternary metal-silicides are reported to exhibit better wear (abrasive and adhesive) resistance when compared to binary metal-silicides (Alman et al., 1995; Newkirk and Hawk, 2001).

Sheng et al. (2008) used commercially pure Ni, Ti and Si powders (powder particle size of 90–250 μm) in the ratio: 70Ni-21Ti-9Si (wt.%) to produce a defect free 2.5 mm thick coating on stainless steel (AISI 304) substrates. The microstructure was comprised of dendritic Ni₁₆Ti₆Si₇ and Fe-Ni-based γ solid solution. The micro-hardness was ~600 HV (500 g). The coatings were tested under pin-on-disk dry sliding conditions at elevated temperatures (400, 500, and 600°C) against the nickel based superalloy GH5K. Neither, substrate pre-heating nor coating post-treatment was reported, however at high temperature the Ni–Ti–Si ternary metal silicide coatings showed an excellent wear resistance. High temperature wear resistance was due to the presence of primary covalent atomic bonds and high micro-hardness of the Ni₁₆Ti₆Si₇ ternary metal silicide. The fracturing of the primary dendrites resulted in the wear of coatings. The unique microstructure as a result of laser fabrication and a transfer layer were found to form which also has a positive role in the wear process.

Ray et al. (2014) employed LMD to improve the service life of lateral rolls in the zero segment of continuous slab caster. Ni based powders with the varying additions of Cr, Mo, B, Nb were deposited. The microstructural characterization revealed the presence of NiCr dendrites are surrounded by Cr and B/Nb enriched hard phases. Hard precipitates improved the wear resistance. During actual performance evaluation, it was found that in the absence of corrosive environment, rolls with improved wear resistance properties produced maximum service life. The lateral rolls cladded with higher percentage of Ni and B were free from cracks and delamination. Two LMD coatings (Stainless steel and Ni alloy) for continuous casting rolls were tested in work of Sanz (2004) against one overlay welding and two chemically hardened HVOF coatings. The laser metal deposits showed less than half the wear rates when compared to that of new generation welded overlay. The wear (abrasive) resistance of LMD coatings was approximately equal to, or somewhat less than welded martensitic stainless steel. LMD coatings of Ni-based and Fe-based alloys and best welded layer showed a similar abrasive wear resistance.

Duan and Wang (2002) studied γ/Cr₃Si metal-silicide coatings showing high-temperature sliding wear resistance. Austenitic stainless steel was the chosen substrate and commercially pure chromium, silicon and nickel elemental powder blends were used as precursors in the wt.% ratio of 54.25Cr-15.75Si-30Ni. The resulting coating (developed with pre-placed powders) with the preferential precipitation of Cr₃Si during solidification as the primary phase. The Cr₃Si primary phase grows freely in the melt pool as primary dendrites. The residual liquid in the inter-dendritic region is enriched with nickel and depleted in chromium and silicon forming the base γ-nickel solid solution, resulting in the γ/Cr₃Si metal-silicide composite coating (Wang and Duan, 2002). The micro-hardness (at room temperature) was found to be almost 1,100 HV and showed an excellent wear resistance (≈6 times better than austenitic stainless steel) at high temperatures (600°C). γ/Cr₃Si metal-silicide laser clad coatings showed excellent wear resistance at high temperatures due to the presence of oxidation and homogeneously dispersed hard and wear resistant Cr₃Si primary dendrites.

Laser deposition of reinforced NiSi silicide intermetallics have been presented in Cai et al. (2003) (Cr-alloyed coatings with Vickers hardness ≈1,000 HV) (Wang et al., 2003) Ni₂Si additions to form coatings of 750 HV micro-hardness and wear resistance (at room temperature) >5 times that of its stainless steel substrate) and Lu and Wang (2005) in which Mo₂Ni₃Si additions result in a coating of ~900 HV which exhibits excellent wear resistance at room temperature, however no high temperature wear testing was presented for either coating system.

Tribaloy (CoMoCrSi alloys) are well-known to exhibit excellent wear and corrosion resistance. Instead of relying on metal carbides for mechanical properties, these alloys gain their strength from the alloying elements like Mo and Si. These alloying elements promote the formation of hard and corrosive resistant microstructure consisting of laves phases (Ya et al., 2018). High temperature wear and corrosion testing of Tribaloy showed that these alloys could be used in mild to high corrosive and/or elevated-temperature environments (Yao et al., 2005, 2006; Tobar et al., 2008).

Tobar et al. (2008) analyzed, laser deposited coatings of CoMoCrSi alloys (Tribaloy-800 and Tribaloy-900) on AISI 304 steel substrate. The defect (porosity and micro cracks) free laser deposits, of about 1 mm thickness, had strong metallurgical bonding with the substrate. Navas et al. (2006) performed tribological testing of Tribaloy T-800 by using ball-on-disk and block-on-ring configurations. The tribological tests were conducted at room temperature. They show that for Tribaloy T-800 coatings, the wear behavior is not strongly influenced by the presence of laves phases. However, the applied load is supported by the laves precipitates homogeneously distributed in the metallic matrix without being removed.

Torres et al. (2018a) worked on the microstructural design of Ni based self-lubricating coatings with the addition of and MoS₂ produced by laser-based additive manufacturing as a first step toward potential use in metal forming. MoS₂ is a lamellar structured solid lubricant (Scharf and Prasad, 2013). During sliding, the strong ionic bond between the Mo and S provides strong resistance to contact load while the crystalline layers of the MoS₂ slide easily and reorient parallel to the sliding direction, providing lubrication. Lei et al. (2015) reported that MoS₂ was decomposed during LMD. However, Torres et al. stated that addition of MoS₂ resulted in the encapsulation of Ag during the laser processing to ensure its uniform distribution across the laser deposits and prevented it to float in the melt pool. Improved retention of the Ag was found during addition of 5 wt.% Ag and 10 wt.% MoS₂ to NiCrSiB powder. A high temperature tribological study was carried out at 600°C under unidirectional sliding. MoS₂ on decomposition formed chromium sulfides which was effective in reducing both friction and wear. Room temperature and high temperature tribological performance was significantly improved compared to reference alloy. No substantive advantage of Ag addition was reported at high temperature, probably due to oxidation (Torres et al., 2018b).

In another study, Torres et al. (2018c) modified the Ni based coatings with the additions of soft-metal solid-lubricants Ag and Cu. TMDs WS₂ and MoS₂ were used for the encapsulation of the soft-metal solid-lubricants due to their decomposition in the melt pool. Tribological behavior was investigated up to 600°C under reciprocating sliding conditions. Self-lubricated Ni based coating showed improved tribological performance due to presence of lubricious sulfides.

Liu et al. (2013a) fabricated self-lubricating coatings of NiCr/Cr3C₂-WS₂-CaF₂ mixed powders by LMD for high temperature tribological applications. Friction and wear characteristics of these laser coatings under different temperatures and loads were studied against Si₃N₄ ceramic counter surface. These coatings exhibited excellent tribological behavior under moderate temperatures and loads.

Additive manufacturing processes are extensively employed in aerospace, automotive and power generation sectors due to their ability to manufacture geometrically complex parts by substituting several individual machining processes (Sexton et al., 2002). The main advantage of additive manufacture is to fabricate component of advance alloys which are difficult to machine and or would offer serious tooling problems. In these sectors many systems are subjected to high temperature, high stress and vibration effect, leading to erosion and creep (Kathuria, 2000; Kaierle et al., 2017). A few examples of these are engine bearings, cylindrical liners, valves, gas/steam turbine blades, bearing rings, casings, bearing and bushings for space satellites, rocket nozzles, hypersonic aircrafts and missiles, nuclear and chemical vessels. Aggressive operating conditions require novel high performance wear resistant alloys with self-lubricating characteristics (Zhu et al., 2013). Ti alloys and Ni based super alloys are extensively used under such conditions to ensure the high reliability and surface integrity (Pusavec et al., 2011; Rynio et al., 2014). As an example, in the gas turbine engine, compressor stages, combustion chamber, and the turbines stages of the gas turbine engine are produced from Ti and Ni alloys (Ulutan and Ozel, 2011).

Ti-based alloys are corrosion resistive and biocompatible, also possess a high strength to weight ratio with low elastic modulus and density (Liu et al., 2014; Khorasani et al., 2015). These are widely used in biomedical, power generation and aerospace industries (Yamada, 1996; Brandl et al., 2010). However, due to poor high temperature tribological characteristics (high and unstable coefficient of friction and lower abrasive and adhesive wear resistance) and low micro-hardness, the use of these alloys is limited (Li et al., 2012, 2015). There is an increasing intent on enhancing the surface properties of Ti alloys in general by utilizing the LBAM processes (Szost et al., 2016). In different trials self-lubricating composite coatings were deposited on Ti alloys by using LMD and such additions on Ti alloys resulted in friction reduction and improved anti-wear characteristics (Candel et al., 2010; Feng et al., 2012; Weng et al., 2015; Zhai et al., 2017). However, powder is preplaced on the substrate, rather than being injected in the laser-induced melt pool, in most of the mentioned applications.

Ocelík et al. (2005) deposited metal-matrix composite layer of TiB/Ti−6Al−4V on Ti−6Al−4V substrates by LMD. Laser metal deposits consisted of two distinct microstructures, primary and eutectic TiB particles dispersed in the matrix of Ti−6Al−4V. The sliding wear tests were performed under boundary lubrication conditions at a low constant sliding speed of 0.01 m/s and at contact pressures of 20 and 100 MPa. The metal-matrix composite layer of TiB/Ti−6Al−4V showed outstanding wear resistance and friction improvement. The deposited layer was strongly adhered due to excellent interfacial bonding between the Ti−6Al−4V matrix and the in situ TiB. At 20 MPa, TiB2/Ti−6Al−4V performed best, while at 100 MPa the eutectic microstructure of TiB/Ti−6Al−4V showed good wear resistance.

Liu et al. (2014) produced defect free novel coatings of γ-NiCrAlTi/TiC + TiWC₂/CrS + Ti₂CS on Ti6Al4V alloy substrate. The coatings were produced by preplaced NiCr/Cr₃C₂-WS₂ mixed powders. The microstructure of the coatings consisted of α-Ti, TiC, TiWC2, γ-NiCrAlTi, Ti₂CS and CrS phases. A high temperature tribological study was carried out (at 20, 300, 600°C) using a ball-on-disc tribometer under dry sliding conditions. Micro-hardness of the coating was almost 3-fold higher; 1,005 HV0.2. The friction coefficient and wear rate were greatly decreased due to combined effect of TiC and TiWC₂ carbides and CrS and Ti₂CS sulfides, possessing excellent self-lubricating properties.

Solid lubricant hBN exhibits chemical inertness and oxidation resistance. Similar to graphite, hBN also has a lamellar structure, but exhibits lower friction in high temperature tribological applications (Tomala et al., 2014; Kostoglou et al., 2015; Podgornik et al., 2015). Lu et al. (2016) produced crack and pore free Ni60-hBN composite coatings on Ti6Al4V substrate by varying the hBN content. The coatings had a strong metallurgical bond with the substrate. LMD Ni60 composite coatings were composed of TiO₂, γ-NiCrAlTi, TiC and TiB₂ phases while LMD Ni60-10%hBN composite coatings consisted of hBN, γ-NiCrAlTi, TiC and TiB₂ phases. The micro-hardness of the composite coatings with 10% hBN was ~1,155 HV0.2. The tribological testing of the composite coatings were conducted at temperatures (20, 300, and 600°C) under dry sliding conditions. Ni60-10%hBN composite coatings exhibited excellent tribological characteristics at high temperatures (300 and 600°C).

Ni-based super alloys with a wide range of alloy compositions are used in various industrial applications over the past four decades in cast, wrought and powder metallurgy forms. Inconel 718 (IN 718) belongs to the group of Ni-based super alloys. Due to the low content of aluminum and titanium, this alloy is known for its good weldability. Therefore, IN 718 is ideally suited for LBAM processes (Strößner et al., 2015).

Jia and Gu (2014) produced IN 718 parts by using SLM at four different energy densities (η) 180, 275, 300, and 330 J/m. The tribological performance was evaluated at room temperature by using a ball-on-disc tribometer. Steel GCr15 ball was used as a counter surface. The coefficient of friction was reported to slightly decrease from 0.62 to 0.58 for SLM parts produced at higher η. A similar decreasing trend was recorded in the wear rate with increasing η. The wear performance was indicated to be primarily influenced by micro-hardness and related microstructural features of SLM parts. The lower hardness at lower laser energy density input triggered the higher wear rate due to mechanical shear force between the sliding surfaces. The wear resistance was enhanced at higher laser energy densities, owing to the refined microstructures, as well as improved micro-hardness due to presence of γ′ phase.

Li et al. (2013) developed self-lubricating Ni-based alloy (Ni-Cr-Mo-Al-10wt.%Ag-10wt.%BaF₂/CaF₂) for a wide range of temperature applications (25–800°C) by sintering process. It is challenging to design a self-lubricating material for high temperature application without compromising the strength of material. The composite resulted in a remarkable self-lubricity (μ ≈ 0.25) and high strength. Similarly Cheng et al. (2017) characterized the NiCrAlMo-12.5wt.%Ag-X wt.%CaF₂/BaF₂ (X = 5 or 10) solid-lubricating composites by using pin-on-disc configuration for high temperature tribological applications. It was concluded that reducing the fluoride eutectic content leads to the significant improvement in the wear resistance above 600°C.

Xiao et al. (2018) evaluated the tribological performance of graphene-IN 718 composites produced by SLM. SLM is shown here to be a viable fabrication technique to produce graphene nano-platelets reinforced IN 718. The tribological tests were conducted under ambient condition (temperature of 13 ± 5°C and relative humidity of 55–65%) by using a ball-on-disk WTM−2E tribological tester. The wear counterpart was a GCr15 ball with 3 mm in diameter. The recorded friction coefficient and wear rate were 22.4 and 66.8% lower than that of pure IN 718. The decrease in friction coefficient and wear rate were the result of improved hardness due to composite reinforcement and the formation of graphene nano-platelets protective layer on the worn surfaces.

Liu et al. (2013b) investigated self-lubricating LMD coatings of NiCr–Cr₃C₂ with 30% WS₂ and 30% WS₂(Ni–P) at 25, 300, and 600°C. Solid lubricant WS₂ forms lubricious film in the tribological contacts characterized by a low shear strength and a lamellar structure. WS₂ resists oxidation up to 539°C and dissolves at higher laser irradiation without encapsulation (Särhammar et al., 2014; Sateesh et al., 2015; Quan et al., 2017). The powder supply for laser processing was preplacing the powder on the substrate. The microstructure of the NiCr–Cr₃C₂/30%WS₂ coating consisted of Cr₇C₃ dendrite, γ-(Fe, Ni)/Cr₇C₃ eutectic and WS2 solid. High temperature tribological tests revealed that NiCr–Cr₃C₂/30%WS₂(Ni–P) showed improved performance from room temperature to 600°C.

Yang et al. (2012) produced wear resistant NiCr/Cr₃C₂ coatings and high temperature self-lubricating wear resistant NiCr/Cr₃C₂-30% WS2 coatings by LMD. Microstructural characterization reveled that NiCr/Cr₃C₂coatings consisted of Cr₇C₃ primary phase and γ-(Fe, Ni)/Cr₇C₃ eutectic colony. The NiCr/Cr₃C₂-30%WS₂ coatings consisted of Cr and W carbides with minor lubricious phases of WS₂ and CrS. The high temperature tribological characterization was performed by using a ball-on-disc tribometer (at 17, 300, and 600°C). The NiCr/Cr₃C₂-30%WS₂ coatings showed lower wear till 600°C but exhibited higher wear at 600°C. Laser deposition with the addition of WS₂ are considered suitable from room temperature to 300°C.

Zhao et al. (2019) fabricated self-lubricating wear resistant coatings on stainless steel substrate by combining LMD and vacuum pressure thermal diffusion welding (VPTW). The fabricated coatings consist of separate layers of wear resistant-NiCrSiB and self-lubricating Cu-coated graphite. Microstructure of the wear resistant layers consist of γ-matrix (Ni, Fe) and Cr carbides (Cr₇C₃ and Cr₂₃C₆) while self-lubricating layers consist of Cu-matrix and graphite. Layers are strongly bonded with each other and the substrate. The tribological properties of the coatings were evaluated at room temperature through reciprocating friction and wear tester Bruker UMT-3. The results indicated better antifriction properties compared to the reference materials (as received substrate, NiCrSiB and Cu-graphite coating) due to formation of self-lubricating tribofilm on the wear resistant worn layers. Abrasive wear along with delamination wear were found to be the main wear mechanisms.

High entropy alloys (HEAs) are a relatively new class of materials, with a novel alloy concept. HEAs are advanced materials with unique properties and such properties cannot be achieved by the conventional micro-alloying approach based on only one dominant element (Zhang et al., 2014). HEAs consist of at least five metal constituents in equi-molar or near equi-molar ratios (5–35 at.%), with face-centered cubic (fcc) and body-centered cubic (bcc) solid solutions instead of intermetallic and complex brittle phases (Ocelík et al., 2016; Li et al., 2018). HEAs are described as an ideal solution as the configuration entropy of these is equivalent to that of idea gas (Ye et al., 2016), see Figure 8A. A model ternary alloy configuration entropy (ΔS_mix J/mol·K) map is shown in Figure 8B, the alloy composition closer to the center of map reaches to the maximum value.

HEAs are the focus of increasing scientific attention due to enormous possibilities of alloy combinations and the chance of tailoring the constituent elements to achieve the final properties (Brif et al., 2015). Conventionally HEAs are produced by vacuum arc melting (Senkov and Woodward, 2011). HEAs are reported to have excellent mechanical properties and an enhanced high temperature stability (Lu et al., 2015). Senkov et al. (2011) developed two HEAs (Nb₂₅Mo₂₅Ta₂₅W₂₅ and V₂₀Nb₂₀Mo₂₀Ta₂₀W₂₀) which exhibited yield strength of ≈600–800 MPa (at ≥900°C) exceptionally higher to those of Ni-based super alloys (IN 718 and Haynes 230). Chuang et al. (2011) designed a series of wear resistant HEAs (Al_xCo_1.5CrFeNi_1.5Ti_y) by varying contents of Al and Ti and compared with the conventional wear resistant steel alloys (SUJ2 and SKH51) of similar micro-hardness. Wear resistance of HEAs was 2-fold than those of conventional steels due to their excellent resistance to oxidation and thermal softening.

LBAM is one of the new potential production route for HEAs (Popov et al., 2019). Ocelík et al. (2016) attempted to produce the AlCoCrFeNi and AlCrFeNiTa HEAs coatings on stainless steel substrate by using LMD (laser power ≈ 600–650 W). It was concluded that LMD is a versatile approach to synthesize HEAs with additive manufacturing processing. However, LMD of HEAs using feeding of mixture of powders is affected by the in-take of particular powders, melting temperatures, laser scan speed and laser power. Zhang et al. (2011) produced 6FeNiCoSiCrAlTi HEA coating with simple bcc solid solution phase on a low carbon steel substrate by using LMD. Microstructural analysis showed the presence of equiaxed polygonal grains, discontinuous interdendritic segregation with bcc structure. The micro-hardness of the coating was 780 HV0.5, much higher than most of the HEAs produced by other fabrication techniques.

Brif et al. (2015) utilized SLM for production of an equiatomic FeCoCrNi HEA. The microstructural and mechanical characterization of SLM parts were performed to investigate the feasibility of producing HEAS in additive manufacturing. Characterization confirmed that SLM fabricated FeCoCrNi HEA preserved its single-phase solid-solution state. Mechanical testing revealed high strength and ductility of FeCoCrNi HEA, comparable to that of stainless steels.

Due to the recent development in the concept of HEAs, limited literature on the tribological characterization of HEAs was found. The available data shows the exceptional performance of these alloys at high temperatures. No specific literature was found on tribological performance of LBAM-HEAs. The reported production methods of the tested HEAs were plasma sintering and arc melting (Poletti et al., 2017; Mathiou et al., 2018; Wang et al., 2018; Zhou R. et al., 2018). Zhang et al. (2017a,b) prepared CoCrFeNi HEA matrix self-lubricating composite by CoCrFeNi HEA powder, nickel-coated graphite powder and nickel-coated MoS₂ powder. The method of preparation was spark plasma sintering. The composite exhibited excellent tribological properties from room temperature to 800°C when tested in air on a ball-on-disk high temperature tribometer. Synergistic lubricating effect of graphite and MoS₂ resulted in the reduction of friction coefficients and wear rates from room temperature to medium temperatures. At high temperatures, various metal oxides were formed on the composite surfaces which improved the tribological properties.

This review has presented a comprehensive state-of-art for application-specific material designs followed by LBAM for high temperature tribological applications.

NU and DM were responsible for the final editing. All authors have contributed equally to the content of the final manuscript.