Journal of Manufacturing and Materials Processing
Article Analytical and Simulation-Based Prediction of Surface Roughness for Micromilling Hardened HSS
Alexander Meijer 1,*, Jim A. Bergmann 2 , Eugen Krebs 1, Dirk Biermann 2 and Petra Wiederkehr 1,2
1 Institute of Machining Technology, TU Dortmund University, 44227 Dortmund, Germany 2 Virtual Machining, Chair for Software Engineering, TU Dortmund University, 44227 Dortmund, Germany * Correspondence: [email protected]; Tel.: +49-231-755-5820
Received: 28 June 2019; Accepted: 8 August 2019; Published: 12 August 2019
Abstract: The high quality demand for machined functional surfaces of forming tools, entail extensive investigations for the adjustment of the manufacturing process. Since the surface quality depends on a multitude of influencing factors in face micromilling, a complex optimization problem arises. Through analytical and simulative approaches, the scope of the experimental investigation to meet the requirements for surface roughness can be significantly reduced. In this contribution, both analytical and simulation-based approaches are presented in the context of predicting the roughness of a machined surface. The consideration of actual tool geometry and shape deviations are used in a simulation system to achieve the agreement with experimental results.
Keywords: surface roughness prediction; geometrical simulation; micromilling
1. Introduction Surface roughness is an important quality criterion of functional components [1]. To achieve low roughness values in manufacturing process chains, finishing operations can be used. Thereby, additional manufacturing steps, like polishing, are often costly and still need to be carried out manually. To design an optimized manufacturing line, the resulting roughness values of each process have to be known. However, due to the dependence on a high number of influencing factors in each machining step, the prediction of these values is challenging. Cutting parameters, choice of material, process dynamics and cutting edge geometry are of decisive importance. This is valid for both the geometrically undefined as well as the geometrically defined cutting edges [2]. First approaches for predicting roughness values were developed for turning processes, by considering the engagement situation and the tool geometry in an analytical model. One approach to calculate the theoretical peak-to-valley roughness Rth as r 2 2 f Rth = rε r (1) − ε − 4 was presented by Bauer [3], which takes the corner radius rε and the feed rate f into account. In literature, however, a more frequently applied equation
f 2 Rth = (2) 8 rε ·
J. Manuf. Mater. Process. 2019, 3, 70; doi:10.3390/jmmp3030070 www.mdpi.com/journal/jmmp J. Manuf. Mater. Process. 2019, 3, 70 2 of 17 by Shaw [4] can be found. Martelotti [5] extended this mathematical relationship, by considering the process specific feed per tooth f z, as well as properties of the tool, such as corner radius rε and number of teeth z, as 2 fz Rth = , (3) fz z 8 r · · − π to calculate Rth for milling processes. Although the occurrence of ploughing effects, tool deviations or geometric properties of the cutting edge are not considered, these equations already provide an approximation of the theoretical roughness depth. For the calculation of the theoretical roughness depth in a face circumferential milling processes, the secondary cutting edges need to be taken into account. Since the resulting machining grooves are influenced by the condition and orientation of the secondary cutting edge, it should be considered for a well-founded prediction of the theoretical roughness depth. In order to gain a more detailed understanding of the generation of a workpiece surface, predictions of topographies for complete parts are preferable. A prediction for a ball-end milling process was presented in the approach of Layegh and Lazoglu [6]. Their model considers the trochoidal motion path of the cutting edge in dependency of the feed per tooth f z, the engagement conditions ap and ae, the tool orientation and the runout, which enables the calculation of a three-dimensional topography. In a face milling process using an end-milling cutter with corner radius, the geometric dependencies are much more complex. The surface topography is not defined by a single cut, but results from a superposition of a large number of cutting motions. Hadad and Ramezani [7] showed that different surface topographies could be generated by changed tool inclinations in face milling processes. Freiburg and Biermann [8] presented an analytical model for high feed milling that considers this relationship. Due to the special geometry of the tools, the transferability to conventional processes is limited [9]. Further approaches can be found in the field of geometric simulations. Kundrák and Felho used a CAD system to determine the surface roughness when using face-milling tools with special cutting inserts [10]. However, this approach does not take the microgeometric properties of the tool, i.e., the actual condition and deviation of the ideal shape of the cutting edge, or trochoidal motion paths of the cutting edges into account [11]. Denkena and Böß were pursuing a similar approach applying a process simulation system, in which CAD data of the tool shape can be respected. When mapping the tool shape to the surface topography, only the tool shell is considered [12]. Lavernhe et al. illustrated the influence of microscopic defects at the cutting edge on the generation of surface topographies [13]. The validation was performed for a ball-end milling tool. Denkena et al. combined a material removal simulation with an empirical model to incorporate stochastic variations regarding the machined workpiece material and, thus, achieved a detailed prediction of the surface quality [14]. In summary, promising approaches have been developed for predicting the surface roughness in face milling processes. This was achieved primarily through geometric simulation approaches. However, promising analytical approaches could be identified for special cases. In addition, the studies showed, that the level of detail is essential for a highly valid prediction. In particular, deviations from ideal cutting edges regarding its own macro- and microgeometric properties must be considered. This aspect is gaining importance to ensure predictions for functional surfaces with low roughness values. In this paper, both an analytical and a geometric simulation-based method are presented for the prediction of the surface roughness resulting from face micromilling processes. The analytical model allows a fast but idealized determination of the roughness profile considering special aspects of the face milling process. The geometric simulation approach enables a realistic prediction of a three-dimensional surface topography considering complex engagement conditions and influencing variables like a detailed tool model considering microgeometric properties of the cutting edge, runout, axial offset and specific variations of the process parameter values. In addition, the simulation is used to investigate and visualize the observed effects resulting from the face milling process. J. Manuf. Mater. Process. 2019, 3, 70 3 of 17 J. Manuf. Mater. Process. 2019, 3, x FOR PEER REVIEW 3 of 17
2.2. Experimental Experimental Setup Setup InIn the the following, following, the the experimental experimental setup setup and and boundary boundary conditions conditions of of the the investigation investigation are are introduced.introduced. In In addition addition to a to presentation a presentation of the of machine the machine tool, the tool, cutting the tools,cutting and tools, measuring and measuring systems, thesystems, sample the material sample is brieflymaterial characterized. is briefly characterized.
2.1.2.1. Face Face Micromilling Micromilling Process Process TheThe milling milling experiments experiments werewere carriedcarried outout on a machining machining center center Kern Kern HSPC HSPC 2522. 2522. Due Due to tothe themineral mineral cast cast construction construction of ofthe the machine machine stand stand and and the the installation installation in an in anair-conditioned air-conditioned room room on a onpolymer a polymer concrete concrete foundation, foundation, a high-precision, a high-precision, vibration-reduced vibration-reduced process process could could be ensured. be ensured. The Themachining machining process process and and the the basic basic process process pa parametersrameters are are presented presented in inFigure Figure 1.1 .
FigureFigure 1. 1.Schematic Schematic visualization visualization of of a facea face micromilling micromilling process. process.
TheThe cutting cutting tests tests were were conducted conducted using using a microa micro end-mill end-mill with with a diametera diameter of ofd =d 1= mm1 mm and and two two solidsolid CBN CBN (Cubic (Cubic Boron Boron Nitride)Nitride) cutting edges, edges, a acorner corner radius radius of ofrε =r ε0.02= 0.02mm,mm, and an and average an average cutting cutting edge rounding of S = 0.97 0.16 µm. Compared to solid carbide tools, CBN tools have a edge rounding of 𝑆 = 0.97 ± 0.16± µm. Compared to solid carbide tools, CBN tools have a higher higherresistance resistance to wear, to wear, which which limits limits the time the time variance variance on the on determined the determined surface surface characteristics characteristics [15]. [15 The]. Thetool tool was was selected selected taking taking the the wear-related wear-related shape shape chan changege and and its itseffects effects on onthe the surface surface topography topography into intoaccount. account. Thus, Thus, the the shape shape of of the the tool tool could could be be assu assumedmed to bebe constantconstant forfor each each milling milling experiment experiment withinwithin the the scope scope of of this this paper. paper. A toolA tool with with sharp shar cuttingp cutting edges edges was was chosen chosen to reduce to reduce the occurrencethe occurrence of plastic deformation effects in front of the cutting edge [11]. Cutting speeds were set to v = 120 m/min of plastic deformation effects in front of the cutting edge [11]. Cutting speeds werec set to vc = 120 at a width of cut of a 0.1 mm and a cutting depth of a 0.01 mm. m/min at a width ofe =cut of ae = 0.1 mm and a cutting depthp = of ap = 0.01 mm.
2.2.2.2. Workpiece Workpiece Material—1.3344 Material—1.3344/AISI/AISI M3:2 M3:2/S/S 6-5-3 6-5-3 TheThe tool tool steel steel 1.3344 1.3344 (AISI (AISI M3:2) M3:2 was) was used used as as sample sample material material for for the the presented presented investigations. investigations. ThisThis steel steel is a cobalt-free,is a cobalt-free, powder-metallurgically powder-metallurgically produced produced high-speed high-speed steel (HSS), steel which (HSS), was which hardened was to 63 1 HRC. Due to its high strength, and in particular its transverse strength, this high-performance hardened± to 63 ± 1 HRC. Due to its high strength, and in particular its transverse strength, this high- high-speedperformance steel high-speed is preferably steel used is preferably for the manufacturing used for the of manufacturing highly stress loaded of highly dies stress andmolds loaded [16 dies]. Therefore,and molds the [16]. material Therefore, is ideally the suitedmaterial for is the ideally production suited offor cold the workproduction tools such of cold as puncheswork tools and such dies, as toolspunches for cold and extrusion, dies, tools deep for drawing, cold extrusion, sintering deep tools, dr asawing, well assintering conventional tools, cuttingas well toolsas conventional with high demandscutting tools on tool with life. high Due demands to the high on tool strength life. Due and to hardness the high of strength the material, and hardness a lower proportionof the material, of plastica lower deformation proportion occurs of plastic during deformation the machining occurs process during compared the machining to non-hardened process compared steels [17 to] and, non- therefore,hardened a highsteels degree [17] and, of shape therefore, accuracy a high can degr be assumedee of shape regarding accuracy the can geometric be assumed engagement regarding of the the toolgeometric [18]. engagement of the tool [18]. 2.3. Measuring Systems 2.3. Measuring Systems In order to characterize the condition of micro end-mills, the scanning electron microscope Mira3 In order to characterize the condition of micro end-mills, the scanning electron microscope Mira3 from Tescan and the strip projection microscope MicroCAD plus from LMI was used. The latter from Tescan and the strip projection microscope MicroCAD plus from LMI was used. The latter enabled detailed recordings of the cutting edge microgeometry. The determined characteristic enabled detailed recordings of the cutting edge microgeometry. The determined characteristic values values of the microgeometry were then utilized to model the tools in the simulation system used. of the microgeometry were then utilized to model the tools in the simulation system used. The machined surface topography was measured using the confocal white-light microscope µsurf from
J. Manuf. Mater. Process. 2019, 3, 70 4 of 17
The machined surface topography was measured using the confocal white-light microscope µsurf fromJ. Nanofocus. Manuf. Mater. Process. Analyses 2019, 3, ofx FOR measured PEER REVIEW surface topographies were conducted using the metrology 4 of 17 software MountainsMap Premium 7.4 from Digital Surf. A cut-off wavelength of λ = 0.25 was selected Nanofocus. Analyses of measured surface topographies were conducted usingc the metrology to determine the surface characteristics of the measured and simulated surfaces. Surface profiles were software MountainsMap Premium 7.4 from Digital Surf. A cut-off wavelength of λc = 0.25 was extractedselected from to measurementsdetermine the surface in feed characteristics direction. of the measured and simulated surfaces. Surface profiles were extracted from measurements in feed direction. 3. A New Analytical Approach for Surface Roughness Determination In3. A the New following Analytical section, Approach an analytical for Surface model Roughness for describing Determination the theoretical roughness depth Rth in a circumferentialIn the following face milling section, process an analytical is presented. model for As describing described the in theoretical Equations roughness (1)–(3), thedepth theoretical Rth roughnessJ.in Manuf. a circumferential depth Mater. Process. can be2019 calculatedface, 3, x FORmilling PEER based processREVIEW on is a two-dimensionalpresented. As described cross-section in Equations of the (1)–(3), geometric 4 ofthe 17 tool theoretical roughness depth can be calculated based on a two-dimensional cross-section of the engagementNanofocus. and, Analyses thus, indicatesof measured the highestsurface topographies expected roughness were conducted depth alongusing thethe feedmetrology direction. In additiongeometric to thetool processengagement parameter and, thus, values indicates used th ine highest Equation expected (1), the roughness angle ψ depthof the along face-sided the feed minor softwaredirection. MountainsMapIn addition to the Premium process parame7.4 fromter Digital values Surf.used Ain Equationcut-off wavelength (1), the angle of λ𝜓c of= 0.25the face-was cutting edge (see Figure2c) is taken into account, which plays a decisive role for the resulting surface selectedsided minor to determine cutting edge the (seesurface Figure characteristics 2c) is taken of into the account, measured which and playssimulated a decisive surfaces. role Surfacefor the topographyprofilesresulting inwere surface a circumferential extracted topography from measurements in face a circumferential milling process.in feed face direction. milling process.
3. A New Analytical Approach for Surface Roughness Determination In the following section, an analytical model for describing the theoretical roughness depth Rth in a circumferential face milling process is presented. As described in Equations (1)–(3), the theoretical roughness depth can be calculated based on a two-dimensional cross-section of the geometric tool engagement and, thus, indicates the highest expected roughness depth along the feed direction. In addition to the process parameter values used in Equation (1), the angle 𝜓 of the face- sided minor cutting edge (see Figure 2c) is taken into account, which plays a decisive role for the resulting surface topography in a circumferential face milling process. FigureFigure 2. Schematic 2. Schematic view view on on (a )(a a) a two two dimensional dimensional en engagementgagement situation situation during during milling, milling, (b) two (b) two consecutive tooth feeds, (c) single milling marks with influencing parameters. consecutive tooth feeds, (c) single milling marks with influencing parameters.
The macroscopicThe macroscopic shape shape of of the the tool tool and and thethe chosenchosen process process parameters parameters determine determine the geometric the geometric cutter-workpiece-engagement and, thus, induce the resulting milling marks, as illustrated in Figure cutter-workpiece-engagement and, thus, induce the resulting milling marks, as illustrated in Figure2. 2. The depth of these marks depends on the feed per tooth fz, the corner radius rε and the angle of the f r The depthminor ofcutting these edge marks ψ. depends While the on feed the feedper pertooth tooth definesz, thethe cornerwidth radiusof the millingε and themarks, angle the of the minorinterrelation cutting edge of theψ. Whilecorner radius the feed and per the tooth angle defines of the minor the width cutting of edge the determine milling marks, the vertical the interrelation depth. of the corner radius and the angle of the minor cutting edge determine the vertical depth. 𝑦= 𝑚⋅x+b where 𝑚=tan(ψ and 𝑏=0 (4) Figure 2. Schematic view on (a) a two dimensional engagement situation during milling, (b) two consecutive tooth feeds,y (c=) singlem x milling+ b wheremarks withm = influencingtan(ψ) and parameters.b = 0 (4) 𝑟 = (𝑥−𝑥 · + (𝑦−𝑦 where 𝑥 = 𝑓 and 𝑟=𝑦 =𝑟 (5) 2 2 2 The macroscopicr = shape(x x mof) the+ tool(y andym the) choswhereen processxm = f zparametersand r = y determinem = rε the geometric (5) − − cutter-workpiece-engagement and, thus, induce the resulting milling marks, as illustrated in Figure Based on the cross-section of the machining mark shown in Figure2, an approach for calculating 2. The depth of these marks depends on the feed per tooth fz, the corner radius rε and the angle of the the maximumminor cutting depth edge of theψ. markWhile was the derived,feed per usingtooth thedefines combination the width of of a linearthe milling and circular marks, equationthe (see Figureinterrelation3). By of inserting the corner Equation radius and (4) the into angle Equation of the minor (6), parameters cutting edge candetermine be substituted the vertical as depth.
𝑦= 𝑚⋅x+b where! 2𝑚=tan(ψ and 𝑏=0 (4) 2 y 2 rε = fz + (y rε) . (6) ( ) − − 𝑟 = (𝑥−𝑥 + (𝑦−𝑦tan ψ where 𝑥 = 𝑓 and 𝑟=𝑦 =𝑟 (5)
Figure 3. Illustration of the basic geometric relationship of a machining mark in context of tool shape.
Based on the cross-section of the machining mark shown in Figure 2, an approach for calculating the maximum depth of the mark was derived, using the combination of a linear and circular equation (see Figure 3). By inserting Equation (4) into Equation (6), parameters can be substituted as