1 Introduction

It is well-known that abrasive wear is a severe problem to industrial components and equipment, resulting in energy consumption [1,2,3]. In order to prolong their service life, these components should be fabricated with coatings. Laser cladding is a surface modification technique creating a high-performance coating on the surface of metallic material by a laser beam of high energy densities [4,5,6,7,8]. The technology offers unique superiority in terms of a material with high hardness and high melting point such as ceramic [9], NiTi alloys [10], and nickel-based superalloy [11, 12], etc. Besides, laser cladding is popularly used to manufacture dense metallic parts with high performance, which is applied in aerospace, automotive, and turbines, etc [13,14,15,16,17].

The Nickel-based alloy coatings fabricated by laser cladding have outstanding wear resistance and corrosion resistance [7, 18]. In recent years, more and more scholars have made an achievement in fabricating Ni-based alloy coatings and nickel-based composite coatings to further enhance wear resistance. Wang et al. [19] indicated that wear volume of Ni-based alloy coatings with the addition of Y2O3, CeO2, and La2O3 could be reduced remarkably. Simultaneously, the defects, such as porosity, crack, and lack of fusion could be eliminated. In addition, it was worthy to point out that nano-sized particles could exhibit outstanding mechanical properties compared with micron-sized particles [20]. Zhao et al. [21] observed nanometer La2O3 could refine the microstructure of interdendritic dramatically. Tang et al. [22] reported that Ni60 cladding layers added nano-WC particles displaying high hardness and abrasive wear resistance than the Nickel-based alloy coatings without nano-WC particles. However, Nickel-based alloy coatings have high cracking sensitivity, owing to a large number of hard Cr-rich precipitates and eutectic structures [23, 24].

Although Ni-based alloy coatings fabricated with rare earth, which plays a key role in producing grain refinement effect, might have superior anti-friction properties, coating’s cracking susceptibility could not be reduced, which attributed to the existence of the eutectics network providing a route for crack growth [25]. Higher hardness and wear resistance could be obtained with the addition of hard ceramic particles, such as WC, TiC, and SiC, but the hard phase added to a soft matrix could increase the brittleness of coatings at the same time [26, 27]. Some scholars had refocused on the methods to restrict crack formation. Zhai et al. [6] used alternating electromagnetic force produced by the effects of alternating current to refine grain structure. As a result, by using this approach, approximately 60% of cracks in Nickel-based alloy coatings could be eliminated. Dai et al. [28] suggested that coating’s crack susceptibility could be decreased with the addition of Co element. Lu et al. [29] reported that the crack of nickel-based superalloy coating could be healed by laser remelting technology, which reduced grain sizes and quantity of carbonitride due to element segregation in the heat-affected zone and the coatings. The residual thermal stress is considered the driving force of crack to Ni-based alloy coatings, which usually produce stress concentration around the pores. In order to reduce crack susceptibility, a useful method could minimize pore area by optimized process parameters [30,31,32]. As a common method that, pre-heating had been applied to decrease crack susceptibility [33,34,35]. These studies had been conducted mostly from rare earth additions, optimizing process parameters, and pre-heating the substrate to reduce the crack. However, the existence of micro-cracks of alloys will further promote the propagation of cracks during the surface abrasion process, thereby reducing wear resistance. Therefore, it is necessary to further consider the relationship between crack sensitivity and the wear performance of Nickel-based alloys.

This study focused on the mechanistic studies of cracking in the Ni-based coatings and presenting a fracture criterion for coatings from the viewpoint of fracture mechanics. Experiments, prefabricating metal nets on the subtract, were conducted to confirm the criterion of fracture by laser cladding. The influence rules of crack susceptibility on the variation of the mesh of metal nets were analyzed. Simultaneity, wear resistance of coatings by the addition of CeO2 were investigated on the corresponding mechanical properties, frictional coefficient, and wear volume. The present results will offer an efficient solution to produce components with low crack susceptibility and high wear-resistance coatings fabricated by laser cladding.

2 Methodology on Crack Suppression

2.1 Crack Formation Mechanism

During laser processing, the mismatch of expansion and shrinkage between the coating and the substrate is generally related to the difference in elastic modulus and thermal expansion coefficients. Based on thermoelasticity theory, the thermal stress σ generated after solidification of the molten pool can be calculated by Eq. (1) [36]:

$$\sigma_{x\max } = - f\left( {x,L} \right)E\Delta \alpha \Delta T,$$
(1)

where ƒ(x, L) is a function of the analysis location and the initial length of the specimen; E is the modulus of elasticity; Δα is the thermal expansion coefficient of deposited material; ΔT is the temperature difference between the analysis position and the restricted area.

In addition, a large temperature gradient along the deposition direction is generated in the molten pool, during which the temperature of the substrate is lower than that of the coatings owing to the good thermal conductivity of the substrate. Therefore, the cladding layer’s shrinkage will be restrained by the substrate when the molten pool cools and solidifies, and the tensile stress is generated in the coating, which might bring a great tendency of cracking [36].

2.2 Elastic and Plastic Fracture in Ni-based Alloy Coating

By observing the cracks, the tensile stress leading to the fracture of the cladding layer is perpendicular to the direction of crack cracking, which belongs to the crack opening type.

The crack tip opening displacement is illustrated in Figure 1(a). The AB segment of the crack surface is extended forward and intersects with the vertical line of tip D at point E. The crack opening displacement δ is measured by 2ED.

Figure 1
figure 1

Cracking mechanism of Ni-based coating [37]: (a) critical opening displacement, (b) microcracks of coating

Full size image

After cladding finished, very high residual tensile stress existed, and the cracks in the cladding layer are caused by the expansion of microcracks under residual tensile stress. It is assumed that there are infinite microcracks of equal length in the direction perpendicular to the scanning direction. The crack length is 2a, and the interval between adjacent cracks is 2h; the uniform tensile stress in the scanning direction is σ; the length of microcrack and its simplified plastic zone is 2c = 2a + 2R, a schematic illustration of the microcracks of the coating as shown in Figure 1(b). Cracking occurs when the crack opening displacement reaches the critical value δc. At this time, the critical tensile stress can be calculated by Eq. (2) [37].

$$\sigma_{sc} = \frac{{\delta_{c}\uppi E}}{{8\sin \int_{\theta }^{{{\uppi \mathord{\left/ {\vphantom {\uppi 2}} \right. \kern-\nulldelimiterspace} 2}}} {\frac{\cos X}{{\sqrt {1 - \sin^{2} \alpha \sin^{2} X} }}\ln \left[ {\frac{{\sin \left( {X + \theta } \right)}}{{\sin \left( {X - \theta } \right)}}} \right]{\text{d}}X} }}.$$
(2)

2.3 Fracture Criterion of Nickel-based Coating

The thermal stress of coating is expressed in two forms, Δα < 0, when the thermal expansion coefficient of the substrate is less than that of the cladding layer, and the coating is subjected to tensile stress. On the contrary, Δα > 0 when the thermal expansion coefficient of the substrate is higher than that of the cladding layer, and the coating is subjected to compressive stress. In order to protect Ni-based coating from cracking, it should be ensured that the maximum tensile stress σxmax in the nickel-based coating is less than the critical tensile stress σsc when there exists crack tendency in cladding layers. According to Eqs. (1) and (2), the micro-crack propagating condition can be described as follows:

$$- f\left( {x,L} \right)E\Delta \alpha \Delta T < \frac{{8\delta_{c} \sin \theta }}{\uppi }\int_{\theta }^{{{\uppi \mathord{\left/ {\vphantom {\uppi 2}} \right. \kern-\nulldelimiterspace} 2}}} {\frac{\cos X}{{\sqrt {1{\text{ - sin}}^{2} \alpha \sin^{2} X} }}\ln \left[ {\frac{{\sin \left( {X + \theta } \right)}}{{\sin \left( {X - \theta } \right)}}} \right]} {\text{ d}}X,$$
(3)

where, \(\alpha = \frac{{\uppi c}}{2h}\), \(\sin \theta = \frac{{\sin ({{\uppi a} \mathord{\left/ {\vphantom {{\uppi a} {2h}}} \right. \kern-\nulldelimiterspace} {2h}})}}{\sin \alpha }\), \(\sin X = \frac{{\sin ({{\uppi x} \mathord{\left/ {\vphantom {{\uppi x} {2h}}} \right. \kern-\nulldelimiterspace} {2h}})}}{\sin \alpha }\).

Eq. (3) presents the factors that influence the microscopic cracks, including material thermophysical parameters (E, Δα, ΔT), specimen length, the critical crack opening displacement when cracking occurs. In terms of crack susceptibility, the majority of these researches mainly focused on temperature gradient ΔT [38, 39]. The authors conclude that preheating of the matrix seemed to be an effective method for reducing the residual stress. However, there is little information about the thermal expansion coefficient on cracks sensibility. Related pieces of literature revealed that the thermal expansion coefficient is the main factor affecting the distortion and residual stresses while the impact of the elastic is relatively tiny. Hence, this paper focuses mainly on the thermophysical parameters Δα [40]. Cracks could be suppressed by reducing the absolute difference of thermal expansion coefficient between the Ni-based coating and the substrate.

3 Experiment Procedures

3.1 Initial Materials

A medium carbon steel plate (0.45 wt.% C) was selected as the substrate material, and its dimension was 55 mm × 37 mm × 10 mm. 304 stainless steel net with eight different mesh (8 mesh, 10 mesh, 12 mesh, 14 mesh, 16 mesh, 20 mesh, 24 mesh, and 30 mesh, respectively) were selected for an experiment. To demonstrated the detail of the mesh, a list was established in Table 1. The chemical composition of the 45 steel and the 304 stainless steel net was shown in Table 2. Ni60 powders with a particle size of 40–80 μm were used as the raw powder. The chemical composition of the powder is listed in Table 3. The CeO2 particles with the contents of 4% were adsorbed on the Ni60 powders by mechanical ball grinding, and the morphology of two kinds of powders was shown in Figure 2.

Table 1 The detail of 304 stainless steel
Full size table
Table 2 Chemical composition of 45 steel and 304 stainless steel net (wt%)
Full size table
Table 3 Chemical composition of Ni60 powders (wt%)
Full size table
Figure 2
figure 2

SEM micrographs: (a) Ni60 powders, (b) Ni60 powders with the addition of 4% CeO2

Full size image

3.2 Experiment Apparatus and Process Parameters

Ni-based composite coatings were performed on the LDM-800 laser additive manufacturing system built by Shenyang Aerospace University, as schematically shown in Figure 3. It consists of a 6 kW IPG fiber laser, a three-axis motion execution system, a three-bin coaxial powder feeder (RC-PGF-D3), a coaxial powder feeding system with a Precitec laser cladding head (YC52), and an oxygen analyzer and control system. Pure argon with 99.99% purity was used to deliver the powders and shield the molten pool from oxidation, which ensured the oxygen level was below 50 ppm. The reciprocating scanning strategy was adopted, and the single-track cladding layer length was 35 mm. The process parameters of laser cladding were shown in Table 4. Before the experiment, the powder was dried in a vacuum oven at 80 °C for 8 h in order to increase fluidity. The substrate was ground and polished with sandpaper to remove the oxide layers, then the substrate was cleaned with ethanol. The 304 stainless steel net was washed with acetone to remove oil and then placed on the substrate.

Figure 3
figure 3

A schematic illustration of the laser cladding process

Full size image
Table 4 Parameters of experiments
Full size table

3.3 Characterization of the Coating

After the experiments, cross-sections of all coatings were obtained by using the wire cutting machine, then the specimens were polished with 400# to 1500# grit sandpapers, and the microstructure was observed by an etchant (H2O and HNO3 and HF with a ratio of 7:3:1). The microstructure of coatings was studied and analyzed by metallographic microscope (MR5000). Zeiss sigma500 scanning electron microscope (SEM) equipped with an energy dispersive spectrometer (EDS) was employed to further confirm the microstructure and identify the chemical compositions of the coatings. The phase constitution of the cladding layer was performed using D/max-2500/PC X-ray diffraction (XRD) with a copper target, and the range of diffraction angle (2θ) was selected as 10°–90°, X-ray tube high voltage: 40 kV, X-ray light tube current: 100 mA. The XRD was implemented with a voltage of 40 kV, a current of 30 mA, a continuous scanning speed of 8°/min, and scanning from 10° to 90°. The microhardness of cladding layers from the surface to the bottom was tested using an HVS-1000 Vickers microhardness tester with a loading force of about 0.98 N for 10 s. One point was measured vertically every 0.1 mm at the cladding layer, each point was measured three times, and the final microhardness was the average value of measurements. The friction and wear tests were carried out on the MS-G5000 wear experimental machine, and the Si3N4 balls were employed as friction pairs with a diameter of 5 mm. The tests were conducted with a rotation speed of 200 r/min and a radius of 5.5 mm, and 45 min friction tests with a 3 N normal load. The wear tracks after the 310 m sliding test were observed with a Keyence Digital Microscope VHX-500F. The wear volumes were assessed by the Alpha-Step D-100 profilometer.

4 Results and Discussion

4.1 Effect of the Stainless Steel Net on Cracks and Wear Resistance of Nickel-based Composite Coatings

4.1.1 Macroscopic Morphology Analysis of Nickel-based Composite Coating

When the cladding layers were detected by dye penetrant test, there are transverse and longitudinal cracks in the Ni-based coating without the net, as illustrated in Figure 4. This is attributed to the thermal stresses that develop during solidification acting on grain boundaries, which is the main cause of cracking tendency. It is believed that cracks occur when the stress exceeds the yield limit of materials. It is well known that Austenitic stainless steel offers a comprehensive property of lower yield strength, better antioxidant properties, strong toughness, and weldability. The stainless steel nets were prefabricated on the substrate before the laser cladding experiment to obtain the coating Ni-based composite coating, which was achieved after solidification. Experimental results showed that the 304 stainless steel net (7 × 10−6‒21 × 10−6/K) on the substrate with different mesh leading to the cracks in the cladding layer decreased. Since the thermal expansion coefficient of 304 stainless steel net is higher than that of the 45 steel (11.9 × 10−6‒13.1 × 10−6/K). The stainless steel net, which was prefabricated on the surface of 45 steel substrates, can be regarded as a part of the substrate. At this time, the overall thermal expansion coefficient α0 = (α45 + α304) is greater than 45 steel. The absolute difference between the thermal expansion coefficient of the substrate after pre-fabricated the 304 stainless steel net and the Ni-based coating (13.9 × 10−6‒20 × 10−6/K) decrease. From the above Eq. (2), the thermal stress of the cladding layer decreased, which led to reduce the crack sensitivity. However, there still existed cracks in Ni-based composite coating with the addition of stainless steel nets of 16 mesh and 24 mesh. It demonstrated that the mesh number of the net is not the larger the better, nor the smaller the better. There exist a critical range to inhibit both the initiation and growth of the crack.

Figure 4
figure 4

Crack observation by dye penetrant test: (a) Ni60, (b) Ni60 coating+ 8 mesh, (c) Ni60 coating+ 10 mesh, (d) Ni60 coating+ 12 mesh, (e) Ni60 coating+ 14 mesh, (f) Ni60 coating+ 14 mesh, (g) Ni60 coating+ 20 mesh, (h) Ni60 coating+ 24 mesh, (i) Ni60 coating+ 30 mesh

Full size image

4.1.2 Analysis of Cross-section Morphology of Nickel-based Composite Coating

From Figure 5, some large pores exist in Ni-based composite coating with 8 mesh stainless steel net prefabricated on the substrate. Because there is a gap between the stainless steel net and the substrate, when the melting pool rapidly solidified, the gas in the gap can not be eliminated in time, forming pores. Compared with the cross-section morphology of Ni-based coating without the net, there was incomplete melting stainless steel wire in the Ni-based composite coating which the stainless steel net was prefabricated on the substrate with 10 mesh, and the presence of microcracks in the Ni-based composite coating which the stainless steel net with 12 mesh was prefabricated on the substrate. However, there were no obvious cracks or pores appeared in the composite coating, which the stainless steel net with 14 mesh was prefabricated on the substrate. It was found that there were small cellular pores in the nickel-based composite coating which the stainless steel net with 24 mesh and 30 mesh were prefabricated on the substrate through an optical microscope. When the specimen is subject to external forces, the existence of porosity has a positive effect on crack propagation, improving the crack sensitivity and decreasing the mechanical property of specimens. The above studies suggested that the precipitating gas hole existed in the nickel-based composite coating, and the gas content in a molten solute increased during the solidification of molten metal and the gas that precipitated near the bottom of grain boundaries. Similarly, it has a large driving force to precipitate gas. The solute of lower solubility is enriched at the intergranular phase, which provides geometric stabilization for bubble micronuclei. The shrinkage cavity is associated with solidification shrinkage, and it is in a vacuum state at the initial stage, which creates favorable conditions for bubble precipitation.

Figure 5
figure 5

Cross-section morphology of nickel-based composite coating with the addition of stainless steel net: (a) Ni60 coating+ 8 mesh, (b) Ni60 coating+ 10 mesh, (c) Ni60 coating+ 12 mesh, (d) Ni60 coating+ 14 mesh, (e) Ni60 coating+ 24 mesh, (f) Ni60 coating+ 30 mesh

Full size image

4.1.3 Analysis of Microhardness of the Nickel-based Composite Coating

The microhardness profile along the depth direction of Ni60A coatings are shown in Figure 6. It can be showed that the microhardness increases with increasing mesh number of the stainless steel nets. When the stainless steel net was prefabricated on the substrate, the microhardness of the composite coating decreased. Due to the stainless steel net was melted at high temperatures, the Fe content increased. As a result, the precipitation of the hard phase was suppressed in the melt pool, which caused a reduction in the microhardness [41]. However, it was found that the microhardness of the coating was improved as the number of meshes of stainless steel net increases. When the stainless steel net with 14 mesh was prefabricated on the substrate, the highest average microhardness of the cladding layer reaches 565HV0.2, which was approximately 2.6 times higher than that of the substrate. Due the fact that as the number of the mesh of the stainless steel net increase, the diameter of wire become increasingly slender. Besides, the content of Fe element decrease with the reduction of the mass of stainless steel net per unit area prefabricating on the substrate, which contributes to the precipitation of the hard phase increases. When 4 wt.% CeO2 was added in Ni-based composite coating which the stainless steel net with 14 mesh was prefabricated on the substrate, the average hardness of the Ni-based composite coating was found to be 425 HV0.2 which showed a 31% reduction compared to Ni-based composite coating without rare earth oxides, but it was still about 2 times as much as that of the 45 steel substrate. Due to the addition of CeO2, the laser energy absorbed by molten pool increases, increasing the convection and inducing a large number of Fe elements from the substrate to come into the molten pool [42].

Figure 6
figure 6

Microhardness of nickel-based compositions coatings

Full size image

4.1.4 Analysis of Friction Coefficient of the Nickel-Based Composite Coating

Figure 7 presents how the friction coefficient of the surface of the 45 steel and cladding layer varies with time at 3 N load. When the surface has undergone a relatively short running in stage, the contact area between the surface and Si3N4 ball is smaller and had large contact stress. The microconvex bodies on the surfaces were abraded vigorously improving the friction coefficient. When the friction coefficient leveled off, it was demonstrated that the wear process gradually enters a stable stage. As shown in Figure 6, the 45 steel shows the highest friction coefficient, and the average friction coefficient is 0.76. As the difference between the hardness of 45 steel and Si3N4 ball is more significant, the steel surface is highly susceptible to damage. In the process of friction and wear, the production of wear debris increased frictional resistance, the friction coefficient increased. The Ni60 coating exhibited an average friction coefficient of 0.50  due to the precipitation of borides and carbides can significantly improve the hardness of the cladding coating, offering the advantage of resistance to abrasive wear. When the stainless steel net was prefabricated on the substrate with 8 mesh, 10 mesh, 12 mesh, and 14 mesh, respectively, the friction coefficient increased with the number of mesh decreasing. The average friction coefficients of Ni-based composite coating with different stainless steel net were 0.64, 0.59, 0.57 and 0.46, respectively. When the stainless steel net with 14 mesh was prefabricated on the substrate,the friction coefficient of Ni-based composite coating was reduced by 70% compared to 45 steel, the friction coefficient was decreased by 8%. The above analysis demonstrated that the Ni-based composite coating with the addition of austenitic stainless net possessed batter antiwear and friction-reduction behavior. The relative investigations reveal that the pores and cracks of the Ni-based alloy coating with the addition of 4 wt.% CeO2 are increased compared with that of the coating without CeO2 [43]. Therefore, when the Ni-based composite coating with the addition of stainless with 14mesh and 4 wt.% CeO2, the average friction coefficient was 0.49. Compared with the Ni60 coating without rare earth oxides, the friction coefficient of N Ni-based composite coating was increased by 6.5%. Compared with 45 steel, the friction coefficient of Ni-based coating was decreased by 36%.

Figure 7
figure 7

Friction coefficient of nickel-based composite coatings

Full size image

4.1.5 Analysis of Wear Scar Morphology and Wear Amount of Nickel-based Composite Coating

The surface morphologies of the wear scars can be revealed by Figure 8, the depth and width of the wear scar of the modified nickel-based composite coating were less than 45 steel, and it was demonstrated that the modified coatings are apparently much excellent wear-resistant than 45 steel. Under cyclic contact stresses, the surface of 45 steel was presented severe wear, and the contact-welding was generated in a local high-temperature environment. Adhesion occurred due to the bonding of the two contact surfaces atoms. The adhesive spots were sheared off and spalled during the subsequent sliding friction. Because of the lower hardness of 45 steel, the microcracks were generated and propagated freely. Then a large number of fatigue spalling pits were found on the worn surface. The bulk of wear debris exhibited large plastic deformation after repeated rolling. As time progresses, part of the undischarged wear debris adhered to the worn surface and wear continued. According to the above analysis, the wear mechanisms of the 45 steel were fatigue wear and adhesive wear. When stainless steel net was prefabricated on the substrate, as the mesh number increased, the width of the wear scars narrower. It was demonstrated that the antifriction properties of Ni-based composite coating improve as the mesh number increased. It can be consistent with the variation of the friction coefficient of Ni-based alloy composite coating. The Ni-based alloy coating that the stainless steel net with 10 mesh was prefabricated on the substrate after the addition of the rare earth oxide 4 wt.% CeO2, the width of the wear scars slightly increased, and the fatigue spalling pits were not found, which indicated that there are no large pieces of wear debris on the worn surface. In summary, when the content of CeO2 was 4 wt.%, the nickel-based composite coating, which the stainless steel net with 14 mesh was prefabricated on the substrate, showing better wear resistance.

Figure 8
figure 8

The surface morphologies of the wear scars of Nickel-based composite coatings: (a) 45 steel, (b) Ni60 coatings, (c) Ni60 coating+ 8 mesh, (d) Ni60 coating+ 10 mesh, (e) Ni60 coating+ 12 mesh, (f) Ni60 coating+ 14 mesh, (g) Ni60 coating+ 14 mesh+ 4%CeO2

Full size image

To further investigate the wear properties of nickel-based composite coating by laser cladding, the wear volumes of the specimens were quantified separately using a surface profiler, as observed in Figure 9. In fact, in a radial section profile of erasion trace, the outside edges are significantly higher than that of the inner ones due to the plastic deformation of the wear debris produced by the surface spalling after repeated rolling. Through comparative analysis, it can be found that the 45 steel had the widest section profile of erasion trace, and the maximum depth was 7 μm, and the wear volume of that was 3.75 × 10−5 mm3·N−1·m−1. The width of the erasion trace of Ni60 coating decreased significantly, and the wear volume of that was 1.47 × 10−5 mm3·N−1·m−1, which was 60.8% lower than that of 45 steel. The width of the erasion trace of the Ni-based composite coating that the stainless steel net with 14 mesh was prefabricated on the substrate decreased significantly, and the wear volume of that was 2.89 × 10−5 mm3·N−1·m−1, which was 22.9% lower than that of 45 steel. When the rare earth oxide 4 wt.% CeO2 was added to it, the depth of the erasion trace of Ni-based composite coating decreased significantly, and the wear volume of that was 0.56 × 10−5 mm3·N−1·m−1, which was 80.6% lower than that of Ni-based coating without rare earth oxide, and 85.1% lower than that of 45 steel substrate. Although the rare earth oxide 4 wt.% CeO2 was added in the Ni-based composite coating which the stainless steel net with 14 mesh was prefabricated on the substrate reducing the microhardness, the abrasion wears resistance of it improved substantially. This is consistent with previous studies [44, 45], indicating that there is no correlation between wear resistance and hardness in multiphase materials. Hardness describes only the hard body’s penetration resistance, but it does not include mechanisms of formation and propagation of cracks which finally lead to the separation of the material [46]. The wear resistance of multiphase materials was controlled not only by the hard phase of materials but also by the strength and toughness of the matrix phase.

Figure 9
figure 9

Radial wear scar profile: (a) 45 steel, (b) Ni60 coatings, (c) Ni60 coating+ 14 mesh, (d) Ni60 coating+ 14 mesh+ 4%CeO2

Full size image

4.2 Microstructure and Phase Analysis of CeO2 to Nickel-based Composite Coating

4.2.1 XRD Phase Analysis of Nickel-based Composite Coating

To further investigate the mechanism of reduction of hardness and increase of wear resistance of Ni-based composited coating with the addition of 4 wt. % CeO2, Figure 10 exhibits the phase composition of materials using the XRD technique. Ni60 coating was mainly composed of the matrix γ-(Ni, Fe) solid solution and the reinforcement phases such as M23C6, M7C3 and hard phase CrB, CeCr2B. Due to the high contents of Fe, Ni and Cr of 304 stainless steel, peaks of nickel-based composite coating that the stainless steel net with 14 mesh was prefabricated on the substrate intensified at 2θ = 44.1°. But there was no difference in phase composition compared to Ni60 coating. The appearance of peak broadening at the diffraction angle of about 51.0° and 75.3° was obtained through the addition of the rare earth oxide 4 wt.% CeO2 into Ni-based composite coating, and there are mainly hard phase CrB and eutectic phase M23C7, at the same time, a new phase of CeCr2B appeared.

Figure 10
figure 10

XRD phase diagram of nickel-based composite coating

Full size image

4.2.2 Microstructure Analysis of Nickel-based Composite Coating

Figure 11 and Table 5 reveal the micro-morphologies and the constituent phases of the nickel-based composite coatings. Figure 11(a) shows that nickel-based composite coating mainly consists of bulk phase with irregular shape A, interdendritic eutectics with the rod-shaped structure B cellular dendrite phase C. Since B and C belong to low atomic number elements, they can not be determined by EDS analysis. The estimation of the constituent phases can be done as follows. Through XRD analysis and reference to the relevant literatures, the following can be inferred. The bulk eutectic contains a high concentration of Ni, Cr, and Fe, a slight amount of C elements, and B poor. It could be inferred that this phase is probably borides CrB. The interdendritic eutectics with the rod-shaped structure are identified as γ-(Fe, Ni) + M7C3 (M = Fe, Ni, Cr) with fewer quantities of C. As shown in Table 3, the relatively high content of Ni is overwhelmingly in cellular dendrite phase in which relatively low contents of C and Cr are dissolved. It can be confirmed that the cellular dendrite is the primary γ-(Fe, Ni) solid solution.

Figure 11
figure 11

(a) Nickel-based composite coating+ 14 mesh, (b) Nickel-based composite coating+ 14 mesh + 4% CeO2

Full size image
Table 5 EDS composition analysis of Nickel-based composite coating+ 14 mesh and Nickel-based composite coating+ 14 mesh + 4% CeO2(mass fraction (%))
Full size table

Figure 11(b) shows that nickel-based composite coating with the addition of 4 wt.% CeO2 mainly consists of blocky phase D, flake-like eutectic phase E, cellular dendrite phase F. Compared to coating without rare earth oxide, the Fe element content increased, and the Cr element content decreased. On the one hand, the laser energy absorbed by the molten pool increases due to the addition of CeO2, increasing the convection and inducing the excessive melting of the substrate [42]. It contributes to an amount of Fe coming into the molten pool. On the other hand, Fe and Cr belong to the elements of the third period, and the radius of the Fe atom is close to that of the Cr atom. When the Fe concentration is higher, the Cr atoms are replaced with Fe to form a solid solution phase. A new phase CeCr2B is formed after the addition of CeO2 since the addition of CeO2 are comparatively less in quantity and the finite dimensions of the probe, the element of Ce fails to detect. Combined with XRD analysis and relevant references, the blocky phase (marked with D in Figure 11(b)) may be identified as CrB with significant quantities of Fe. The flake-like eutectic phase (marked with E in Figure 10(b)) may be identified as γ-(Fe, Ni) + M23C7 (M = Fe, Ni, Cr) eutectics with small quantities of Si. The cellular dendrite phase may be identified as γ-(Fe, Ni) solid solution with small quantities of C, Cr and Si.

Through comparative analysis, when 4 wt.% CeO2 was added in Ni-based composite coating which the stainless steel net with 14 mesh was prefabricated on the substrate, the size of the cellular dendrons increases and the resistance of the crystal boundary reduces. When an external force was applied, the plasticity distortion was very easy to go through the crystal boundary from one crystal grain to another [47]. Besides, hardness describes only the hard body’s resistance to penetration [46]. The hardness of the coating was reduced. When the cladding layer was subjected to thermal stress, part of the internal stress will be removed by plastic deformation, which would reduce the cracking tendency. It can be seen from Figure 11(b) that the size of the bulk phase decrease. When the melt pool temperature is higher than 2050 ℃, CeO2 could be decomposed to Ce ion. In addition, Ce enriches as an inner adsorption element mainly at the grain boundary, which decreases the interfacial energy and Gibbs free energy of the cladding layer, and reduces the driving force for crystal growth, thereby hindering the growth of crystals [48]. From this, hard phases (CeCr2B) were distributed at grain boundaries of bulk phases. The ductile phase γ-(Fe, Ni) was precipitated after the primary hard phase during laser cladding, and the ductile phase was prone to inhibition, so the amount of the hard phase decreased would increase the number of ductile phases. When the surface layer was subjected to external force, it can reduce the probability of damage to the surface layer in an elastic deformation manner within a certain range. The softer matrix phase was worn, and the hard phase, which plays a certain supporting and bearing role was not easy to be peeled off due to its small size, thus, reducing the viscous force. In addition, the softer matrix phase acted as inlaying wear debris and hard particle, therefore the wear resistance was improved greatly.

5 Conclusions

  1. (1)

    The fracture criterion of  the nickel-based coating was presented basing on thermoelasticity theory and fracture mechanics. Factors that influence the Microscopic cracks included material thermophysical parameters (E, Δα, ΔT), specimen length and critical crack opening displacement when cracking occurs.

  2. (2)

    The difference in thermal expansion coefficient Δα was reduced by prefabricating an austenitic stainless net on the surface of the substrate, and a significant number of the transverse and longitudinal cracks were disappeared in the Ni-based coating.

  3. (3)

    As the number of meshes of stainless steel net increased, the average microhardness of the nickel-based composite coating improved, and the friction coefficient decreased. When the stainless steel net with 14 mesh was prefabricated on the substrate, the highest average microhardness of nickel composite coating was 565 HV which was 2.6 times higher than that of the substrate and the average friction coefficient of Ni-based composite coating was reduced by 70% compared to 45 steel. Comparing with the Ni60 coating, the friction coefficient was decreased by 8%.

  4. (4)

    After the 4 wt.% CeO2 was added to Ni-based composite coating that the stainless steel net was prefabricated on the substrate with 14 mesh, comparing with coating without rare earth oxides, the average hardness showed a 36% reduction and the average coefficient of friction increased by 6.5%. But the wear resistance improved substantially. The wear volume of that was 0.56 × 10−5 mm3·N−1·m−1, which was 80.6% lower than that of Ni-based coating without rare earth oxide, and 85.1% lower than that of 45 steel substrate.