Fretting Wear and Scratch Resistance of Cold-Sprayed Pure Cu and Ti

Abstract

The paper analyses the fretting and wear behavior of pure copper and pure titanium coatings realized through cold spray. The coatings were designed and produced by employing processing conditions leading to minimum porosity and high hardness; these conditions were 700 °C and 40 bar for Ti powders and 400 °C and 30 bar for Cu ones. The low porosity and high strength materials led to high resistance to wear damaging through the optimal energy dissipation upon fretting. Due to the sprayed particles deformation mode, the sprayed materials show non-uniform hardening along the deposition distance. As a matter of fact, hardness varied in the range 3.7–4.2 GPa for Ti coatings and 1.5–2 GPa for the Cu ones depending on the distance from the substrate and on the coatings thickness. This influenced the materials properties and the response to the wear damaging. This was demonstrated by the scratch tests performed on coatings with different thicknesses. Those coatings sprayed in major thickness revealed the best wear resistance due to the deformation hardening. The harder coatings also revealed brittle fracture at the experienced highest loads.

Introduction

Cold spray is recognized as an optimal additive manufacturing (AM) technology capable of producing sound bulk components [1,2,3,4] with exceptional performances experienced by copper-, nickel- and titanium-based materials [5,6,7,8,9]. During cold spray process, a high pressurized gas is employed to accelerate metallic particles at temperatures well below their melting points. The sprayed particles severely deform upon impacting on hard substrates leading to compact deposits. This low-temperature thermal spray technology avoids undesirable oxidation processes or phase modifications in the sprayed materials leading to the obtaining of components characterized by good mechanical properties [10].

The sprayed particles exhibit severe plastic deformation upon impacting; this induces many microstructural modifications that are responsible for the bonding to the substrate and among the different particles [11]. The activated microstructural features are dependent on the sprayed particles properties, the substrate surface and mechanical properties and the employed pressure and temperature of the spray gases. As these properties are varied, different coatings behaviors are expected [12]. In particular, the coatings properties are very sensitive to the selected spray parameters [13, 14]. Many scientific evidences underline that the particle–particle cohesion is due to the achievement of the adiabatic shear instability. This phenomenon leads to local temperature increase supporting the particle deformation that behaves as a viscous material. This allows for the oxides rupture with consequent optimal adhesion and particles interlocking [15, 16]. Other scientific evidences underline that peripheral jets form as a consequence of strong pressure waves due to impact leading to the expansion of the particle edge [17]. By considering the sprayed pure metals behavior, the processing conditions variation largely affects the deformation mechanisms and the consequent mechanical and microstructural properties [18,19,20]. In general, processing conditions influence the severe plastic deformation levels; this governs the metallurgical bonding and is revealed by the flattening ratio of the particles after impact. The measurement of the flattening ratio allows for the determination of the deformation behavior of the material at different distances for the surface toward the substrate [21, 22].

Titanium and its alloys show well-known microstructural and mechanical properties [23] allowing them to be applied in many civil and industrial applications from aerospace [24, 25] to biomedical [26] to protective components [27]. Copper and its alloys are mainly employed in those fields requiring materials with high electrical and thermal properties [28,29,30,31].

Ti coatings have been produced in order to increase the resistance to fretting and wear of aluminum and aluminum alloys [32]. Fretting wear evolves through various phenomena due to the continuous contact between two surfaces; the developed microstructural mechanisms lead to fatigue cracking and delamination of the superficial layers. Once continue sliding acts, microcracks nucleate and continue to grow up to fatigue damaging and macroscopic fracture [33]. In general, the fretting behavior of materials involves various microstructural features that continuously interact and overlap during continuous loading [34]. The fretting wear and scratch behavior of cold spray coatings is not so presented in literature [35]. It is well known that material porosity and hardness/elastic modulus are the main factors affecting the wear behavior [36].

In the classical approach, only hardness is considered as the principal aspect governing the wear response of surfaces. As the material hardens, also the elastic modulus starts to play a fundamental role. So, not the hardness and elastic modulus must be taken into consideration to completely characterize such fundamental material behavior. In this direction, the hardness to elastic modulus ratio provides many information about the surface mechanisms acting during sliding. Nanoindentation is a well-established technique developed to precisely measure the local hardness and elastic moduli of bulk materials and coatings [37]. Nano-probe techniques allow for the continuous characterization of mechanical properties as well as the surface ones under contact loading. Anyway, the relationships between local mechanical properties and the wear response are not conclusive. This is complicated in those conditions where complex triaxial stresses act on small volumes [38].

Very few experimental evidences are presented on the scratch response of cold spray deposits [39, 40]. Here, nanoindentation and scratch are employed to continuously characterize the coatings mechanical properties along the deposition path. The analyses of scratch tracks allowed to identify the surface damage consequent to sliding at different load levels. The results are very useful for cold spray design in order to optimize the coatings microstructure, mechanical properties and dimensions.

Experimental Procedure

Materials

Pure copper powders with particle distribution + 18–41 µm and mean dimensions of 27 ± 1.5 µm were provided by Safina (Ploiesti, Romania); pure titanium powders with particle distribution + 15–44 µm and mean dimensions of 30 ± 2 µm were provided by AP&C (Boisbriand, QC, Canada). Granulometry was measured through laser scattering by employing Beckman Coulter LS 13 320 (Brea, CA, USA). Phase analysis was evaluated through XRD Malvern PANalytical X’Pert PRO MPD θ/θ Bragg–Brentano powder diffractometer (Malvern, United Kingdom), with font of Cu Kα (λ = 1.5418 Å) and work power 45 kV–40 mA was used. Scanning electron microscopy (SEM), Thermo Fisher Phenom Pro Desktop SEM (Eindhoven, Netherlands), was employed for microstructural characterization.

The particle dimensions distributions are shown in Fig. 1. The particles are spherical shaped as shown in Fig. 2. The carbon steel substrate was alumina sandblasted before spraying.

Fig. 1

Particle diameter distribution of the employed powders

Fig. 2

Powders aspect (a) Cu and (b) Ti

The X-ray spectra of the employed particles are plotted in Fig. 3.

Fig. 3

X-ray analyses results of the studied particles

Coatings Deposition

The coatings were produced with a CGT Kinetics 4000 (Haun, Germany) with a SiC nozzle. It has a rectangular cross section measuring 2 × 4 mm throat and 2 × 10 mm exit at CPT facilities (Barcelona, Spain). The employed substrate was a C20 carbon steel. The selected cold spray parameters are shown in Table 1. The deposition procedure is show in Fig. 4. The Cu coatings measured 0.1 and 1 mm in thicknesses, after 1 and 10 passes, respectively, Ti coatings measured 0.2 and 1 mm thicknesses, after 1 and 5 passes, respectively.

Table 1 Cold spray parameters

Fig. 4

Robot path employed for cold spray deposition

Coatings Characterizations

Metallographic preparation was performed according to the ASTM E192. Samples were grinded and polished. Leica DMI5000M (Wetzlar, Germany) microscope was employed for optical microscopy observations. The coatings thickness was measured by employing the Leica picture analyzer. The porosity levels and distribution were calculated by using the Image J processing software.

The coating mechanical properties were evaluated by employing an Anton Paar nanoindentation equipment model TTX-NHT2 (Ostfildern, Germany), with a Berkovich diamond indenter. The tests were developed in load control mode, the loading and unloading rates were 20 mN/min, and the fixed dwell time was 5 s. The coatings mechanical properties were obtained through the Oliver and Pharr methods from the load–depth indentations curves.

ASTM C633 standard was employed for adhesion properties characterization of the coatings. Steel cylinders’ top surfaces were sprayed with Cu and Ti powders in the previous described conditions. Then, they were glued to the respective counter-bodies of the same size. The employed glue was a FM-1000-FOOT elastometric wafer (Indestructible Paint Inc.). The adhesive strength of the glue was measured resulting 70 MPa. Tensile tests were then performed on these cylinders in order to measure the adhesive strength. Seven tests per condition were performed.

Scratch tests were performed by using an Anton Paar Revetest instrument (Ostfildern, Germany) with a Rockwell-C diamond indenter. The normal load was linearly varied from 1 to 200 N. The total scratch length was 10 mm. The scratching speed was 10 mm/min. The fretting wear behavior was analyzed by employing a Nanovea Tribometer T500 (Irvine, CA, USA).

Friction is measured thanks to a load cell mounted on the arm. An image processing system mounted on an optical microscope allows to analyze the traces of wear. A profilometer is employed for measuring the tracks traces. From the profilometer analyses, the wear volume loss is then calculated. The test was performed in dry mode by using a tungsten carbide pin.

Results and Discussions

The morphologies of the coatings cross section obtained by optical microscopy are shown in Fig. 5. The porosity of the Cu coatings was 0.15 ± 0.05% and 0.25 ± 0.07%, for 0.2 mm and 1.0 mm, respectively, while the porosity of the Ti coatings was 1.72 ± 0.10% and 1.81 ± 0.08%, for 0.1 mm and 1.0 mm, respectively. The porosity evaluation is fundamental because it strongly influences both the coating adhesion and the overall mechanical behavior.

Fig. 5

Images of coatings. (a, b) Cu 0.1 mm, (c, d) Cu 1.0 mm, (e, f) Ti 0.2 mm, and (g, h) Ti 1.0 mm

The porosity of Cu coatings was lower than the values presented by Yin et al. [7] and Huang et al. [28], who obtained the best value of 1.67 ± 0.21% and 0.8 ± 0.4%, even with higher temperature, 650 and 800 °C, respectively, than the used in this work. The porosity of Ti coatings reached very low levels [25, 41], 1.8 ± 0.08% and 1.0%, respectively. As the impact velocity increases, the particles flatten more severely; this is favored by increases in gas temperature and pressure. By tuning an ideal impact velocity, a very high particles flattening is obtained and a reduction of the deposit porosity can be recorded. This is accompanied with the particle–particle voids filling as the severe plastic deformation increases [42]. Metallurgical bonding is favored by the increases in impact energy as a consequence of the increases in severe plastic deformation [18]. The deformation level is evaluated through the single particle splatting that leads to the transformation from the spherical shape to the pancake-like one. With low impact energy, particles retain their spherical shape and the particle–particle voids are not filled sufficiently. Now, the main factors influencing the energy at impact are the particles velocity and the impact temperature; the particles energy upon impact is intrinsically related to the particle velocity at the same temperature; as a consequence, porosity shows a dependence on the temperature at impact with an exponential behavior [43].

Figure 5d shows how particles strongly deform by impacting on the substrate; their shape becomes elliptical. This is very different from the Ti powders, Fig. 5h, where the particles deformation is less pronounced. The microhardness of the coatings was 100 ± 11 HV_0.2 123 ± 8 HV_0.2, for Cu 0.1 mm and 1.0 mm, respectively, and 224 ± 9 HV_0.2, 209 ± 23 HV_0.2, for Ti 0.2 mm and 1.0 mm, respectively.

As largely described in the introduction, it is believed that deep analyses of surface response to complex loading require the precise probing of both hardness and elastic modulus in all the coatings volume [44]. Initially, nanoindentations were performed on the polished surface of the spayed copper and titanium. The results for all the sprayed thicknesses are shown in Fig. 6.

Fig. 6

Nanoindentation curves. (a) Cu 0.1 mm, (b) Cu 1.0 mm, (c) Ti 0.2 mm, and (d) Ti 1.0 mm coatings

In the first stage of indentation, the deformation is pure elastic for very low loads levels. By increasing the indentation force, the curve does not show the classical Hertian trend. This is due to the fact that shear deformation accumulates in the tip region with consequent plastic deformation behavior. This is due to the dislocations accumulation in the strained region; this accumulation is governed by dislocation pile-up that increases as the plastic strain continues. The indentations track on the Cu coatings surfaces is illustrated in Fig. 7a and b. The typical copper ductility is revealed by the intense plastically deformed region around the track. This behavior appears very limited for the titanium coatings, this was due to the higher stiffness of this material if compared with the copper one, and this can be clearly viewed from the indentations tracks in Fig. 7c and d.

Fig. 7

Indentations aspect: (a) Cu 0.1 mm, (b) Cu 1.0 mm, (c) Ti 0.2 mm, and (d) Ti 1.0 mm coatings

For all the sprayed coatings, hardness decreases from the substrate toward the surface (Fig. 8).

Fig. 8

Hardness variation as a function of the distance from the substrate for all the cold-sprayed coatings

This behavior is attributed to the continuous deformation experienced by the coating as a consequence of the progression of impact; in fact, the material continues to develop hardening as a consequence of particles impacting on the previously sprayed material up to the end of the coating deposition. The first deposited particles adhere to the substrate in the first stages of the cold spray process. The further sprayed particles splat by deforming on the previously sprayed material by contributing to the global severe plastic deformation of the coating. In addition, voids are filled as the process continues to evolve. This void filling as well as the continuous plastic deformation contributes to the hardness increase. Obviously this increase is more pronounced as the material is closer to the substrate.

The samples aspect after adhesion tests is shown in Fig. 9.

Fig. 9

Coated cylinders after tensile tests performed for adhesion measurement

The measured adhesion strength was 48 ± 4 MPa for copper coatings and 61 ± 5 MPa for titanium coatings. The aspect of the coating materials after tests revealed decohesion among the particles with local plasticity behavior around each particle. This local plastic deformation resulted more pronounced in the case of copper coatings with respect to the titanium ones (Fig. 10).

Fig. 10

Surface aspect of copper (a, b) and titanium (c, d) after tensile adhesion tests

It can be stated that the failure mode was mainly cohesive. This behavior is related to the energy that is dissipated along with the propagation of cracks' delamination. This is related to the interface energy at the coating–substrate interface and then to the adhesion strength. The coatings’ adhesion strength of the coating is very high if compared to the data belonging to other thermal spray coatings [22].

The coatings mechanical properties as well as the coatings–substrate adhesion were further studied by employing surface scratches at continuously increasing vertical loads. The vertical loads–scratch depths curves are plotted in Fig. 11 for all the sprayed coatings.

Fig. 11

Vertical load versus scratch depth. (a) Cu 0.1 mm, (b) Cu 1.0 mm, (c) Ti 0.2 mm, and (d) Ti 1.0 mm coatings

For the Cu coating with 0.1 mm in thickness, the linear behavior is altered around the scratch depth of 100 µm because of the indent reaching the substrate. The scratched coatings behavior is revealed by the scratch tracks after loading. These are shown in 10, for Cu and Ti coatings.

The deep observation of the load–depth behavior allows to identify the various critical loads (CL). Coatings are progressively damaged upon scratch and consequently some specific mechanisms can be individuated as the vertical load increases. The mechanisms are cracking, fractures and final decohesion. The observation of these features permits to identify the critical loads that produce such damaging. As the vertical load increases, stress in the coating increases by inducing specific mechanisms in the track. For the case of the studied coatings, the different damage mechanisms were identified through scanning electron microscopy observations of the tracks after scratching. As expected, the coatings show a different scratch behavior depending on the material composition and on the coating thickness. First of all, from the load–depth curves it appears how the copper coatings show a very regular curve while the titanium coatings show continuous variation revealing many microstructural modifications related to the material behavior during scratches. The most regular scratch behavior is shown by the copper coating with 1 mm thickness where the scratch does not show to produce damage in the unscratched material or fractures on the scratch surface. The scratch evolves through the formation of many peripheral copper flakes. Obviously, the flakes volume increases as the maximum load increases (Fig. 12b). By observing the titanium cold-sprayed coating with the same thickness (1 mm), they were observed many microstructural features inside the track and in the peripheral material. The occurrence of the critical loads means that the deformation mode is varying as the scratch continues at increased vertical loads. By setting a linearly increasing vertical load during scratch, a continuous series of damaging mechanisms is observed in the track. The damage mechanisms usually lead to the coating delamination [45]. The first critical load is normally associated with the initial damage mechanisms developing as a consequence of scratching. In the present case, it was individuated as the appearance of the first cracks on the scratch tracks where the compression forces of the indent are predominant with respect to the tangential forces (Fig. 13).

Fig. 12

Scratch tracks. (a) Cu 0.1 mm, (b) Cu 1.0 mm, (c) Ti 0.2 mm, and (d) Ti 1.0 mm coatings

Fig. 13

First cracks appearance in the scratch track of the cold-sprayed Ti with 1 mm thickness

By comparing the cracks presence with the load–depth curve, it is possible to affirm that this first critical load is 48N at 46 µm penetration depth. The cracks intensity is enhanced as the vertical load is linearly increased. As the vertical load increases, higher compressive state is induced on the surface with consequent damage loading of the scratched material. The second critical load was attributed to the appearance of tongue-shaped cracks (Fig. 14).

Fig. 14

Tongue shaped cracks in the scratch track of the cold-sprayed Ti with 1 mm thickness

These are due to a more complex multiaxial stress field induced in the material as the scratch proceeds. The second critical load was recorded at 100N at 90 µm penetration depth. The last critical load is characteristic of cold-sprayed coatings; in this case the damage is transferred to the material surrounding the scratch with the increase in compressive stresses leading to particles decohesion (Fig. 15a) that becomes very remarkable at the vertical maximum load (Fig. 15b).

Fig. 15

Macrodamage leading to particles decohesion in the cold-sprayed Ti with 1 mm thickness

This behavior starts at the load of 127N. By comparing these features to the scratch behavior observed in the cold-sprayed titanium with a coating thickness of 0.2 mm, the first cracks appear at a load of 50 N, comparable with the observations of the coating with 1 mm thickness (Fig. 16a). The pronounced tongue-shaped cracks appear at 85 N (Fig. 16b), while the pronounced damage in the material surrounding the scratch with particles decohesion is observed at a vertical load of 135 N (Fig. 16c). The scratch track at the maximum vertical force is shown in Fig. 16d.

Fig. 16

Damage in the cold-sprayed Ti coating with 0.2 mm thickness

Now, also if the mechanical and microstructural behaviors of the two coatings appear very similar, it is believed that the coating thickness influences the scratch behavior. This is very pronounced in a very ductile material as copper. As a matter of fact, the scratch aspect of the coating with 0.1 mm thickness shows a very different behavior if compared to the coating with 1mm thickness. In fact, in this case, small tongue cracks appear on the crack surface at a load of 80 N (Fig. 17a); the dimension of these cracks increases up to the maximum vertical load (Fig. 17b) revealing a larger sensibility to the increase in compressive stresses in cold-sprayed coatings with small thicknesses.

Fig. 17

Damage in the cold-sprayed Cu coating with 0.1 mm thickness

The employed vertical loads were set to 50, 100 and 150 N. The wear traces for Cu and Ti at 150 N for all the thicknesses are shown in Fig. 18.

Fig. 18

Wear traces by fretting at a maximum load of 150 N. (a, b) Cu and (c, d) Ti coatings

Figure 19 shows the wear aspect and profiles. They were employed to calculate the wear damaging in terms of weight loss.

Fig. 19

Wear traces for the studied coatings after wear at a maximum load of 150 N

As expected, the material volume loss increases as increasing the fretting load. The weight loss is more pronounced for the thicker coatings at the same maximum load level. This was due to the increased hardening of the sprayed particles observed as the coatings thickness increases. This was shown by the lower slope of the load-weight loss curves by increasing the maximum load from 50 N to 100 and 150 N. As the maximum wear force increases, the material under wear is progressively more hard as a function of the distance from the substrate. The harder material is more resistant to the wear damaging (Fig. 20).

Fig. 20

Weight loss after wear testing. (a) Cu and (b) Ti coatings

Due to the relative movement of the contact interfaces, direction and magnitude of the force are constantly changing. This leads to the variation of the contact mechanisms and consequently to the wear behavior. The friction coefficient is the ratio between the tangential contact force during the pin slip and the normal load applied to the contact surface. Cold-sprayed coatings experience low friction at ambient temperature. The friction coefficient decreases as the maximum load increases; this confirms the described mechanisms due to the increase in hardness as approaching the substrate. The fretting wear of the studied coatings is plotted in Fig. 21 for the different applied maximum loads.

Fig. 21

Fretting wear experienced by all the coatings at different loads

The effect of material hardness on the fretting wear damaging is still under debate. Recent evidences of fretting behavior of heavily hardened steels show that hardness differences reduce damaging while increased weight loss is recorded as the hardness decreases [46, 47]. Various results show the hardness behavior effect on fretting wear damaging [48]. Here, the materials hardening produced higher resistance against wearing. The hardened volume leads to friction reduction and to reduced damaging in the inner material. As the fretting material is harder, it is able to dissipate more energy being capable of resulting more stiff to wear damaging. So, the principal conclusion is that the hardness variation of cold-sprayed materials governs the weight loss and the frictional behavior of the coatings. This behavior reveals a direct relationship between the nanoindentation evolution and the fretting wear damaging.

Conclusions

The wear and fretting behavior of Ti and Cu cold-sprayed coatings with different thickness was described in the present paper. Low porosity was revealed for all the coatings; this was attributed to the optimal processing parameters selected for spraying. Nanoindentation hardness was higher for the thicker coatings because of the increases particles deformation as the particles continue to splat on the substrate and on the previously deposited particles. The coatings behavior was very different for the two materials during scratch and also for different thicknesses. The most regular scratch behavior is shown by the copper coating with 1 mm thickness where the scratch does not show to produce damage in the unscratched material or fractures on the scratch surface. Many damage features are revealed by titanium cold-sprayed coatings with micro-fractures and particles decohesion appearing as the vertical scratch load increases. Also the thickness influences this behavior; this was revealed by the Cu coatings 0.1 mm thick where different fractures appear in the scratch track revealing a completely different behavior with respect to the 1-mm-thick coating. The fretting results showed that the volume reduction increases for lower coatings thickness. This aspect was due to the enhanced particles severe plastic deformation observed as the coatings thickness is increased. As the maximum force increases, in fact, the fretting material is linearly harder by moving from the surface toward the substrate. This hardening induces higher resistance to wear damaging.