Open access peer-reviewed chapter

Machining Characteristics of Direct Laser Deposited Tungsten Carbide

By Paweł Twardowski and Szymon Wojciechowski

Submitted: November 29th 2011Reviewed: July 17th 2012Published: December 19th 2012

DOI: 10.5772/51439

Downloaded: 3297

1. Introduction

Machinability can be defined as the relative susceptibility of the work material to the decohesion phenomenon and chip formation, during cutting and grinding. This feature depends on work and tool’s material physic-chemical properties and condition, method of machining, as well as cutting conditions [1]. Therefore, there is no unique and unambiguous meaning to the term machinability. This feature, can be described by many various indicators. Each one of them carries out a wide variety of operations, each with a different criteria of machinability. A material may have good machinability by one criterion, but poor machinability by another [2].

To deal with this complex situation, the approach adopted in this chapter is to divide machinability indicators into two groups, namely: physical and technological indicators. Physical machinability indicators include i.a. temperatures, cutting forces, vibrations and residual stresses generated during machining process, because their value have the direct influence on the ensemble of the remaining machining effects. Technological indicators include mainly machined surface texture and tool’s life (relatively tool wear).

The most popular method for producing tungsten carbide components is by powder metallurgy technology. Nonetheless, for individual, small quantity production or product prototyping this method is too costly and time consuming. The alternative to powder metallurgy is Direct Laser Deposition (DLD) technology, which can be used to quickly produce metallic powder prototypes by a layer manufacturing method [3, 4] – Figure 1. The primary objective of DLD technology is the regeneration of machine parts or machine parts manufacturing with the improved surface layer properties, e.g. higher corrosion, erosion and abrasion resistance. Direct Laser Deposition is an extension of the laser cladding process, which enables three dimensional fully-dense prototype building by cladding consecutive layers on top of one another [6]. The DLD technology is increasingly being used in production of functional prototypes, modify or repair components which have excellent hardness, toughness, corrosion and abrasion wear-resistance, e.g. machine parts for the automotive industry – Figure 2. In the near future DLD technology will be used in manufacturing of spare parts in long term space missions [7] or submarines [8].

Figure 1.

Direct laser deposition technology (DLD): a) the scheme of process, b) the view of process [5]

Figure 2.

The application of DLD technology for the crankshafts (a, b) and parts for the automotive industry (c) [5]

Unfortunately, DLD technology has also significant disadvantage. Presently most components produced by DLD technology has an unsatisfactory geometric accuracy as well as surface roughness and requires some post-process machining to finish them to required tolerances [9]. Therefore, the machinability of DLD manufactured materials (e.g. tungsten carbide), require further and extensive studies.


2. Machining of tungsten carbide

Tungsten carbide has excellent physicochemical properties such as, superior strength, high hardness, high fracture toughness, and high abrasion wear-resistance. These properties impinges wide application of tungsten carbide in industry for cutting tools, molds and dies. On the other hand, these unique properties can cause substantial difficulties during machining process, which can result in low machinability. Therefore, machining of tungsten carbide requires the knowledge about the physical effects of the process, as well as appropriate selection of machining method and cutting conditions, enabling desired technological effects. The primary objective of post-process machining of tungsten carbide is to achieve satisfactory geometric and physical properties of its surface texture.

The most popular finishing method of tungsten carbides applied in the tooling industry is grinding with the diamond and CBN (cubic boron nitride) wheels. However, in order to produce optical components made of cemented carbide (e.g. spherical mirrors) the profile quality requires a low surface roughness, a stringent form accuracy on the submicron scale, as well as a low amount of surface damage [10]. Traditional grinding with the diamond wheels can cause machining-induced cracks and damages to the material. To remove these cracks and damage and to obtain a mirror finish, lapping and polishing with fine diamond abrasives are usually employed. Nevertheless, these processes can cause the deterioration of form accuracy and increase the machining cost.

Recently, ultraprecision grinding has been developed that substantially decreases subsurface damage and can precisely control the geometry of the finished surface [11, 12]. This kind of process is conducted on the ultraprecision CNC grinding machines, with three-axes movements, and micro-system to deterministically generate, fine, and pre-polish a plano or spherical surface. Very often these machines have motors with power exceeding 1kW and maximal rotational speeds above 80 000 rpm. The example of ultraprecision set-up is shown in Figure 3a.

Tools applied in the ultraprecision grinding processes are usually selected as metal-bond diamond cup wheels (Figure 3b) with grit sizes between 15÷25 µm. The selected CNC grinding program includes two parts, i.e. stock removal and spark out. During the stock removal step, the grinding speed is selected in the range of 10÷15 m/s (for a small tool diameters it corresponds to rotational speeds up to 40 000 rpm). The vertical feed rates of the tool spindle are usually selected in the range of 0.05÷0.2 mm/min, and the workpiece spindle rotated at 1000 rpm. During the spark out phase, the workpiece is rotated with a 1000 rpm for about 180 rotations.

Figure 3.

The ultraprecision grinding process of a spherical mirrors: a) set-up [10], b) schematic presentation of the diamond tool [12]

Apart of grinding, recently are seen tendencies to cutting (mainly turning and milling – Figure 4) brittle materials such as, tungsten carbide and reaction-bonded silicon carbide (RB-SiC) by a superhard CBN (cubic boron nitride) and PCD (polycrystalline diamond) cutters in cutting conditions assuring ductile cutting [13, 14]. This technique of cutting can be achieved when depths of cut and feeds (expressed as uncut chip thickness) are extremely low and a quotient of the tool cutting edge inclination angle to uncut chip thickness is greater than unity (rn/h>1). In milling process of tungsten carbide by CBN tools, the transition from ductile to brittle cutting occurs at critical depth of cut apcr.equal to approximately 4.78 μm. Machining with very low cutting conditions is feasible only on ultraprecision machine tools with high rigidity, which is substantial limitation of this technique.

Figure 4a depicts the schematic diagram of the numerically controlled three-axis ultraprecision lathe used in ductile turning experiments. The lathe has two perpendicular hydrostatic tables along the X- and Z-axis direction, in addition to a B-axis rotary table built into the X-axis table. Both X-axis and Z-axis tables have linear resolutions of 1nm, and the B-axis rotary table has an angular resolution of one ten millionths of a degree. The sample can be rotated with the spindle and moved along the Z-axis direction, while the cutting tool can be moved along the X-axis direction and also rotated around the B-axis.

Figure 4.

The set-up of cutting process: a) ductile turning of carbides [15], b) face milling of DLD tungsten carbide [16]

Cutters applied in the ductile cutting experiments, are made of diamond (MCD, PCD) or CBN (cubic boron nitride) materials. The example of turning and milling tool applied in carbide’s machining process is presented in Figure 5. These tools have usually negative geometry (rake γangles lower than 0), and a small values of tool cutting edge inclination angle rn< 6 μm, which is needed to initiation of the ductile cutting. To obtain a crack free surface the tool feed rate fand the cutting depth apmust be very low. Their values are usually selected as: f≈ 1÷75 μm/rev and ap≈ 2÷10 μm. Cutting speeds can be selected in the following range: vc= 50÷600 m/min.

Figure 5.

Tools applied in machining of carbides: a) diamond turning tool [15], b) CBN torus end mill [16]

In order to finish plane surface, made of tungsten carbide, obtained using DLD technology, one can apply face milling process (Figure 4b). Surfaces obtained using DLD technology have significantly higher roughness than ones manufactured by powder metallurgy technology. Therefore, cutting parameters during machining of these surfaces can be higher than those applied in machining of powder metallurgy surfaces, and selected as follows: feed per tooth fz≈ 25÷100 μm/tooth, axial depth of cut ap= 20 μm, radial depth of cut ae= D/2 (half of tool’s diameter).


3. The analysis of physical machinability indicators

In this chapter the analysis of main physical machinability indicators, such as: cutting forces and vibrations will be presented. The set-up of cutting forces and vibrations measurements during face milling process is presented in Figure 6.

The hook up into bed of a machine piezoelectric force dynamometer was used to measure total cutting forces components [16]. Instantaneous force values were measured in feed force Ff, normal feed force FfNand thrust force Fpdirections. Force dynamometer’s natural frequency is equal to 1672 Hz. In order to avoid disturbances induced by proximity of forcing frequency to gauge natural frequency, the band – elimination filter was applied. The acceleration of vibrations of tungsten carbide workpiece during milling was measured using piezoelectric accelerometer. These vibrations were measured in the same directions as cutting force components.

Figure 6.

The set-up of force and vibration measurements during face milling of tungsten carbide [16]

Figure 7 depicts the tool wear (VBc) influence on RMSvalues of vibrations Apand forces Fp.

Figure 7.

RMSvalues of thrust forceFpand thrust vibrationsFpin function of tool wearVBc. Cutting conditions:vc= 68 m/min,vf= 180 mm/min,ap= 0.02 mm,ae= 6 mm

On the base of conducted investigations, clear relation between progressing tool wear and RMSvalues of forces and vibrations in thrust direction (Fp, Ap) can be seen. Above-mentioned relation is expressed by the correlation coefficient R2>0.8. Tool wear growth induced force Fpand vibration Apincrease, which stays in agreement with investigations [17] related to machining of hardened steel. It was stated that in machining process of tungsten carbide typical abrasion wear, (characterized by VBcindicator) concentrated mainly on flank face can be found. This phenomenon is probably caused by a friction of hard carbide particles on CBN tool flank face [18]. As a result, progressing abrasion of the tool binder induces the growth of friction force, which in turn is related to force and vibration (Fp, Ap) increase. It is necessary to mention that, in remaining cutting force and vibration directions (Ff, Af, FfN, AfN) no correlation with tool wear VBcwas found out (correlation coefficient R2 was lower than 0.1).

In order to analyze forcing frequencies affecting cutting force components during milling of tungsten carbide, the FFT (Fast Fourier Transform) spectra were determined (Figure 8). From the Figure 8 it is resulting, that primary forcing frequency is tooth passing frequency zfo.Since number of teeth: z=2, the zfofrequency overlaps with the second harmonics of spindle speed frequency – 2fo. Therefore 2foand zfofrequencies are dominant. It means that the dominative factor in FfNand Fpforce time courses is milling process kinematics related to the cutting force generated by the each of teeth. Primary harmonic component zfois accompanied by so-called „collateral bands” with the following values: zfo+ foand zfo – fo.They appearance is related to the occurrence of radial run out phenomenon. From the Figure 8 it can be also seen that frequency spectra of FfNand Fpforce components consist of spindle speed frequency polyharmonics. Similar dependencies were observed for majority of investigated cutting force components frequency spectra.

Figure 8.

Frequency spectra ofFfNandFpforce components

Figure 9 compares cutting forces in function of feed per tooth obtained during milling of tungsten carbide and hardened X153CrMoV12 steel (with 60 HRC hardness). It was observed that both in milling of tungsten carbide and hardened steel, cutting forces (Ff, FfN, Fp) are increasing monotonically with feed per tooth fzgrowth, what is typical dependency occurring in metal cutting processes. In tungsten carbide milling process, the highest force values appeared in thrust direction (Fp), independently of feed per tooth fzvalue. As it was mentioned before, this phenomenon is probably caused by a friction of hard carbide particles on CBN tool flank face, which affects tool wear increase, and hence friction and thrust force Fpgrowth (it is worth indicating that after second experimental trial tool wear was VBc≈ 0.07 mm). In case of milling of hardened steel, thrust force Fphas lower values than those obtained during milling of tungsten carbide. This is attributed to the significantly lower hardness of hardened steel (in comparison to tungsten carbide), which reduces tool wear intensity (tool wear after second trial: VBc≈ 0), and thus values of thrust force Fp. The influence of work material’s hardness on the cutting force values during machining is described in details in [19].

Figure 10 depicts RMSvalues of vibrations in function of feed per tooth fzduring milling of tungsten carbide.

Figure 9.

RMSvalues of force components in function of feed per toothfzin milling of: a) tungsten carbide, b) hardened steel

Figure 10.

RMSvalues of vibrations (Af,AfN,Ap) in function of feed per toothfzin milling of tungsten carbide

From the Figure 10 it can be seen, that feed per tooth fzgrowth induces monotonic increase of vibrations in all measured directions (Af, AfN, Ap). It was observed that independently of feed per tooth fzvalue, vibrations in the thrust direction Aphave the smallest values, in comparison to the other measured directions. The reason of this phenomenon is probably connected with the highest tool stiffness in the thrust direction (parallel to rotational axle). The highest acceleration of vibration values (independently of feed per tooth fzvalue) occurred in the feed normal direction AfN. According to research: [20, 21], it could be caused by the direct contact of cutter radius and tool flank face with the machined surface, which is the major source of forcing vibrations, and also the smallest damping ratio in the feed normal direction compared to the other two axes.

In order to estimation of cutting forces in the broad range of cutting conditions, cutting force models can be applied. Majority of models assume that cutting force is proportional to sectional area of cut and the specific cutting pressures. Figure 11 depicts, empirically determined course of the specific cutting pressure in function of mean uncut chip thickness ki=f(h), in milling of tungsten carbide, while table 1 specific cutting pressure (kc, kcN, kp) regression equations.

Figure 11.

Specific cutting pressurekiin function of mean uncut chip thicknessh

From the Figure 11 it can be seen, that mean uncut chip thickness hgrowth is accompanied by the specific cutting pressure (kc, kcN, kp) decrease. This phenomenon stays in agreement with the dependency observed in metal cutting processes. Between experimental specific cutting pressure values and calculated ones (based on regression analysis) some divergences can be seen. These divergences are expressed by the correlation coefficient R2>0.87 (table 1). Above-mentioned divergences have disadvantageous influence on mechanistic cutting force model accuracy. The reason of their occurrence could be attributed to milling process dynamics (e.g. machine tool stiffness).

Specific cutting pressure componentSpecific cutting pressure ki
Regression equationR2
Tangentialkc= 388.9 h-0.8720.873
RadialkcN= 385.4 h-0.8450.901
Thrustkp= 644.1 h-0.7980.915

Table 1.

Regression equations of specific cutting pressure components


4. The analysis of technological machinability indicators

Machined surface texture and tool wear are the essential factors determining cutting ability in practical applications. One of the most popular geometrical tool wear indicators is tool wear on the flank face designated by the VB. Its value can be measured using stereoscopic microscopes. The method of tool wear measurement is depicted in Figure 12. Machined surface texture can be examined using three and two dimensional (3D, 2D) measurements. 3D measurements can be achieved using stationary profilometer Hommelwerke T8000 (Figure 13). Two dimensional measurements can be made by T500 profilometer (Hommelwerke), equipped with T5E head and Turbo DATAWIN software. The sampling length lr= 0.8 mm, the evaluation length ln= 5 lr= 4.8 mm, the length of wave cut – off λc(cut – off) = 0.8 mm and ISO 11562(M1) filter are usually applied in the measurements. As a result of 2D measurements the surface profile charts are received. On the basis of surface profile charts the Raand Rzparameters can be calculated using appropriate software.

Figure 12.

Tool’s flank wear measurement

Figure 13.

The view of stationary profilometer Hommelwerke T8000

Figure 14 depicts the tool wear progress in function of cutting time during face milling of tungsten carbide (manufactured by DLD technology) with CBN cutters. As it can be seen, tool wear process for each tooth is similar, i.e. there are no significant deviations of VBcvalues for respective teeth. Introducing arbitrary dullness criterion VBc= 0.2 mm, it can be seen that twofold cutting speed vcincrease, caused almost eightfold tool life Tdecrease. On the basis of acquired data the sexponent used in Taylor`s equation (T= CT/vcs, where CTis constant dependent of workpiece properties) can be estimated, but it is necessary to emphasize that determining the sexponent from two experimental values is not very accurate. After consideration of the vc1, vc2, T1and T2the s= 2.65 was obtained. This value is located in the range of the sexponents characteristic for high speed milling of hardened steel, thus the intensity of cutting speed vcinfluence on tool life Tin tungsten carbide milling is similar to those for hardened steel. Moreover the tool wear concentrates on the flank face of the tool (see Figure 14c). Because of this, the relations between the tool wear and both forces and vibrations in thrust direction were observed (see Figure 7).

Figure 14.

a), b) Tool wear in function of cutting timetsfor two investigated cutting speedsvc; c) tool wear comparison for exemplary dullness criterionVBc= 0.2 mm (z1,z2– number of tooth,T1,T2– tool life)

Figure 15 compares the surface texture of tungsten carbide sample manufactured by DLD technology before and after milling.

Figure 15.

Surface texture of tungsten carbide manufactured by DLD technology, before and after machining: a) 2D surface profile, b) image of surface

It can be seen, that tungsten carbide sample manufactured by DLD technology has an unsatisfactory geometric accuracy and unreasonable surface roughness. Furthermore, from the surface profile and the FFT analysis (Figure 16) it is resulting, that surface texture after DLD process has a random character. The FFT analysis of surface profile consists also of constituent related to the half of the evaluation length (2.4 mm), which means that DLD surface profile is affected by the waviness. Therefore, it needs further finishing process. After milling, machined surface is much smoother and characterized by significantly lower values of surface roughness parameters.

Figure 16.

FFT analysis of surface profile after DLD process of tungsten carbide

Figure 17 depicts 3D surface roughness charts and power density spectra (PDS) obtained after milling of tungsten carbide.

It can be seen, that 3D surface topographies after milling (Figure 17) are affected by the cutter’s projection into the workpiece. This observation is also confirmed by the power density spectra which represent wavelengths of surface irregularities generated during machining. Surface profiles consist of wavelengths related to the feed per tooth value (fz= 0.05 mm) which is related to the kinematic-geometric projection of cutter into the workpiece, and feed per revolution value (f= 0.1 mm) which can be induced due to radial run out phenomenon.

Figure 18 depicts examples of profile charts and corresponding to them Raand Rzparameters for various feed per tooth fzvalues. As it can be seen the fourfold feed per tooth fzincrease did not make any significant qualitative and quantitative surface texture changes. It denotes that feed insignificantly influences surface roughness, what is not in full agreement with the results shown in Figures 17a and 17b. For some instances, characteristic kinematic-geometric projection of cutting edge into the workpiece can be seen, however in a wider surface roughness range, there is no typical relation. Figure 19 depicts surface roughness parameters Raand Rz(for vc= 68 m/min) in function of feed per tooth fz.

Figure 17.

surface roughness chart and corresponding Power Density Function during: a) milling with cutting speedvc= 68 m/min, b) milling with cutting speedvc= 150 m/min

From these charts no influence of feed per tooth fzon surface roughness is seen, despite for fz= 0.1 mm/tooth. In this case the theoretic value of Rztis comparable to real Rzvalue. It is commonly known that the increase of feed per tooth fzis accompanied by the increase of surface roughness. Theoretically, the lower feed is fixed, the lower surface roughness is generated. Nevertheless in practice, differences between theoretical and real surface roughness values are increasing with feed decrease. Similar conclusions can be proposed from cumulative Raand Rzcharts for all apand fzcombinations (see Figure 20).

Twofold apand fourfold fzgrowth caused insignificant Raand Rzchange. Therefore in the range of conducted research non monotonic increase of surface roughness in function of investigated factors was stated.

Figure 18.

Examples of profile charts for various feed per toothfzvalues: a)fz= 0.025 mm/tooth, b)fz= 0.05 mm/tooth, c)fz= 0.075 mm/tooth, d)fz= 0.1 mm/tooth

Figure 19.

Surface roughnessRaandRzin function of feed per toothfz

Figure 20.

Surface roughnessRaandRzin function of feed per toothfzand depth of cutap


5. Summary and conclusions

The development of modern tool materials such as diamonds (PCD, MCD) and cubic boron nitrides (CBN), as well as ultraprecision and rigid machine tools enables machining of tungsten carbides. These materials have excellent physicochemical properties such as, superior strength, high hardness, high fracture toughness, and high abrasion wear-resistance. On the other hand, these unique properties can cause substantial difficulties during machining process, which can result in low machinability. From the carried out experiments it can be seen, that during machining of tungsten carbides, excessive values of vibrations and intense tool wear growth can occur.

Figure 21 depicts schemes of tungsten carbide products manufacturing processes.

Figure 21.

The schemes of manufacturing processes of various products made of tungsten carbide: a) cutting insert, b) spherical surface, c) end product made by DLD technology

The application of ductile cutting to production of cutting inserts (Figure 21a) shortens manufacturing process by the elimination of one partial process (e.g. polishing). However ductile cutting occurs only in the range of extremely low values of depths of cut and feeds. Therefore, this kind of process can be achieved only on very rigid and ultraprecision machine tools, what is substantial limitation of this method. Ultraprecision machine tools can be also applied to grinding of very accurate spherical surfaces. This process also shortens manufacturing process by the elimination of polishing or lapping (Figure 21b). In case of tungsten carbide products obtained by DLD (direct laser deposition) technology (Figure 21c), grinding or cutting (e.g. milling, turning) can be applied as the finishing process. However cutting enables also the shaping of manufactured part, by the possibility of higher cutting conditions application in comparison to grinding. Nevertheless, during cutting of tungsten carbide, intense tool wear growth can occur, and thus this process requires the selection of appropriate cutting conditions.

Deliberations presented in this chapter reveal, that efficient machining process of tungsten carbide parts is feasible, however it requires the knowledge about the physical effects of the process, as well as appropriate selection of machining method and cutting conditions, enabling desired technological effects.

© 2012 The Author(s). Licensee IntechOpen. This chapter is distributed under the terms of the Creative Commons Attribution 3.0 License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

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Paweł Twardowski and Szymon Wojciechowski (December 19th 2012). Machining Characteristics of Direct Laser Deposited Tungsten Carbide, Tungsten Carbide - Processing and Applications, Kui Liu, IntechOpen, DOI: 10.5772/51439. Available from:

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