# Modeling of Cutting Forces with a Serrated End Mill

Authors: Yu Guo; Bin Lin; Weiqiang Wang
Journal: Mathematical Problems in Engineering
 (2019)

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## Abstract

The paper presents a mechanistic cutting force model of serrated end mill to predict cutting forces. Geometric model of serrated end mill is established, which covers variable helix end mill geometries. In this model, the serration of helical cutting flutes is expressed spatially and the wave of serration is defined to be a sine wave. The spatial vector is applied to define chip thickness so as to enhance the spatial expressiveness of the model, which is perpendicular to the curvature of each flute. Each helical flute is scatted into a series of infinitesimal cutting edges. The infinitesimal cutting forces depend on three cutting force coefficients and three edge force coefficients in the tangential, radial, and axial directions at every cutting element. By integrating the infinitesimal cutting forces along each cutting edge, the milling forces with serrated end mill can be predicted. The model feasibility of the serrated end mill is verified by comparing the predicted and measured cutting forces. Moreover, the model is also verified such that it can also predict cutting forces with other types of end mills, such as variable helix serrated end mill, variable helix end mill, and regular end mill.


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## Body

## 1. Introduction

Nowadays, the manufacturing industry demands high productivity because of the competitiveness environment. In manufacturing industry, milling is one of the most important metal cutting, which is based on removing material by cutting mechanism. The efficiency and stability of milling are conflicted in almost all cases. Therefore, it is necessary to study the mechanism for predicting the cutting forces during milling process, which contributes to optimizing the parameters, designing the clamps and tools, analyzing the deformation, and suppressing the vibration during the milling process [1].Researches on end milling have been done in recent years, which is most focused on the research of mechanics and dynamics models with regular end mills. Merchant [2] proposed a mathematical model, in which the well-known orthogonal cutting model equations were developed. His research provided a good foundation for the later researchers. By analyzing the milling process, Martelloti [3] presented a force model which firstly expressed the cutting thickness with the geometric method. Sutherland and DeVor [4] established a cutting force model to predict the cutting forces and surface error. System deflections which appear on the chip load are studied by the model, and a method is proposed to balance cutting forces and system deflections. Although the proposed model was predicted accurately, it did not consider the characteristic of flexible thin plates during end milling. Budak et al. [5] proposed a method to obtain cutting force coefficients from orthogonal cutting data, which eliminated the calibration of cutter geometry in the experiment. Budak’s method can be used in the multiaxis milling with complex cutter geometries. Li et al. [6] considered the effects of end cutting edge and tool nose radius in the first slice of each tooth, whereas they analyzed other slices in the force model without considering the effects. Liu et al. [7, 8] developed a theoretical dynamic cutting force model with peripheral helical end mills. The model analyzed oblique cutting method, size effect of undeformed chip thickness, and the effective rake angle effect. S. Ratchev et al. [9, 10] proposed an analytical method to predict machining dimensional form error of low rigidity components. FE model was integrated in the force model to analyze the part deflection.In order to obtain high efficiency in milling, some special cutters were invented, such as serrated end mills. Such tools were widely used because of the significant efficiency in material removal rate during milling.Serrated end mills are mostly used in rough milling, which have variation of cutter radius along the flute. Because of the serrated cutting edge profiles, chip load is irregularly distributed both along and between the helical flutes, which contributes in increasing the stability of serrated end mills. Campomanes [11] proposed a mechanics and dynamics model of serrated end mills. In the model, average cutting force coefficients and approximate chip thickness were presented, which was first modeled by Altintas [12]. Campomanes found that when helical flutes were replaced by sinusoidally varying serrated cutting edges, chatter stability can be improved. Merdol and Altintas [13] established a theoretical model about serrated tools. Serrated flute design knots had been fitted to a cubic spline, which were projected on helical flutes. Dombovari et al. [14] proposed a model to predict milling forces with serrated tools. Moreover, the Semidiscretization Method was applied to gain the stability of serrated end mills. In the paper, the practical advantages of serrated tools were confirmed considering the effect of serration. Grabowski et al. [15] presented a method to predict milling forces and studied the stability of complex tools. In the recent study, Ozkirimli et al. [16] proposed a generalized model to analyze the chatter stability for complex milling operations. Sultan and Okafor [17] established a cutting force prediction model of wavy-edge bull-nose helical end mill. It studied the effects of geometric parameters of WEBNHE on the predicted cutting force components and the resultant cutting force. Techranizadeh and Budak [18] investigated the effect of serration and proposed a method for optimizing serration shapes.The previous researches concentrated on serrated end mill separately. Besides, the expression of chip thickness with serrated end mill was not explained clearly. Moreover, the industry process needs higher accuracy and higher efficiency recently. In order to satisfy the demands, end mills with special geometric structure have been widely used. Therefore, it is significant to study the force model with special end mills, which can be utilized to optimize the cutting parameters, design the cutting tools, and analyze the stability during the milling process.The paper establishes a mechanistic cutting force model to predict cutting forces with serrated end mill during end milling process. First, it establishes a geometric model of serrated end mill considering pitch angles and helix angles in each helical cutting flute. In the model, the serration of helical cutting flute is expressed distinctly, which is determined as a sine wave. The chip thickness is also explained in geometry, which is perpendicular to the curvature of each flute. It is expressed distinctly to be the local distance between the previously and the cutting surfaces approximately in the direction of the local normal vectorn→j(t,z) of the flute. In the cutting force model, each flute is scatted into a series of infinitesimal cutting edges. By integrating the infinitesimal cutting forces along each cutting edge of serrated end mill, the cutting forces can be obtained. The viability of the proposed model is verified by comparing the simulated and measured cutting forces with serrated end mill. In addition, some cutting experiments are used subsequently to verify that the model can predict cutting forces with variable helix serrated end mill. Comparing with regular end mill and variable helix end mill, the cutting forces of serrated end mill are smaller. In summary, compared with previous works, this model has more expensive application in milling, especially in the condition of rough milling.


## 2. Modeling of Serrated End Mill

Serrated end mill has wavy flank surface along the flutes. As shown in Figure1, the wave can be determined as a sine wave with amplitudeA and wave length λ. Radius of serrated tool changes along axial direction, which can be calculated by considering the serration wave geometry.Figure 1
Geometric model of serrated end mill.


### 2.1. Serration

By varying the local radiusRj of jth flute at level z, the serration of serrated end mill can be obtained.(1)Rjz=R-△RjzR is the radius of cylindrical serrated end mill shank envelope, and z is the axial depth. △Rj(z) is the variation, which can be calculated by a sine wave with amplitude and wave length.(2)△Rjz=A-Asin⁡γz,jA is the peak-to-peak amplitude. γ(z,j) is the angle of the serration wave in the jth tooth at level ofz, which is shown in Figure 1 and obtained by (3)γz,j=2πz/cos⁡βjλ-∑k=1j-1ϕpjAs shown in Figure1, ∑k=1j-1ϕpj is the phase shift of serration wave and ϕpj is the pitch angle between the subsequence flutes at the tip of end mill.


### 2.2. Geometric Model of the Helical Cutting Edges

As shown in Figure1, the radial immersion angle of point P can be obtained as(4)ϕjt,z=ϕ10-ψjzj=1ϕ10+∑j=2Nϕpj-ψjz1<j≤Nϕ 10 is the rotation angle at level z=0, which can be seen as a reference edge. It can be determined by the spindle speed n, time t, and the initial angular position ϕ0.(5)ϕ10=2πnt+ϕ0As shown in Figure1, ψjz is the radial lag angle, which is related to axial depthz, radiusR of cylindrical serrated end mill shank envelope, and local helix angle βj in each flute. It can be calculated by (6)ψjz=ztan⁡βjRWhen the peak-to-peak amplitude A is zero, the proposed model can predict cutting forces with variable helix end mill. What is more, the proposed model can turn to be regular cutting force model if A=0 and local helix angleβj is invariable.As shown in cylindrical serrated end mill in Figure2, the point P can be determined by vector P→j(t,z) from origin O.(7)P→jt,z=Pxt,zi→+Pyt,zj→+Pzt,zk→(8)Pxt,z=Rjzsin⁡ϕjt,zPyt,z=Rjzcos⁡ϕjt,zPzt,z=Rψjztan⁡βjFigure 2
Axial immersion angle and radius.The axial immersion angleκj(t,z) is associated with the scalar product of the tangent and normal vectors, which can be obtained by (9)κjt,z=a⁡cos⁡t→jt,z·v→jt,zt→jt,zwheretj→t,z is the tangent to the serrated flute and can be expressed by (10)t→jt,z=dP→jt,zdzThe unit vector points outward inXY plane, which can be calculated as(11)v→jt,z=sin⁡ϕjt,zi→+cos⁡ϕjt,zj→Substituting (10) and (11) into (9), the full definition of axial immersion angle κj(t,z) is obtained as(12)κjt,z=acos⁡d/dzRjzd/dzRjz2+tan⁡βj/RRjz2+1


### 2.3. Chip Thickness

During milling process, the chip thickness is identified to be perpendicular to the curvature of the serrated flute. As shown in Figure3, chip thickness can be represented as the local distance between the previous and the cutting surfaces approximately in the direction of the local normal vector n→j(t,z) of the flute.Figure 3
Chip thickness with serrated end mill.The chip thickness between thejth and the (j+1)th flutes can be obtained by(13)hg,jt,z≈Δr→jt,zn→jt,zThe equation cannot strictly represent the physical chip thickness. In Figure3, the local movement of the jth flute relative to the (j+1)th flute at the same angular position can be expressed as(14)Δr→jt,z=r→jt,z-r→j-1t,z=Rjz-Rj-1zsin⁡ϕjt,z+ftjt,zRjz-Rj-1zcos⁡ϕjt,z0j≥2R1z-RNzsin⁡ϕ1t,z+ft1t,z)R1z-RNzcos⁡ϕ1t,z0j=1where the feed can be calculated as follows:(15)ftjt,z=Vfφjz2πnBetween thejth and (j+1)th flutes of serrated end mill in the axial direction, the pitch angle can be shown as(16)φjz=2π+ϕjt,z-ϕNt,z=ϕp1-ztan⁡βj+N-1-tan⁡βjRj=1ϕjt,z-ϕj-1t,z=ϕpj-ztan⁡βj-tan⁡βj+1R1<j≤NThe unit normal vector of thejth flute at level z for uneven radius can be obtained by(17)n→jt,z=sin⁡κjt,zsin⁡ϕjt,zsin⁡κjt,zcos⁡ϕjt,zcos⁡κjt,zThe effective chip thickness along axial direction can be evaluated as(18)hjt,z=Gjt,zhg,jt,zSince the milling is effective only when the edge of end mill is cutting,Gjt,z determines whether the jth tooth is cutting.(19)Gjt,z=1ϕst,j≤ϕjt,z≤ϕex,j0ϕjt,z<ϕst,j,ϕjt,z>ϕex,jϕ s j, ϕej are the positive entry angle and the positive exit angle, which can be obtained by the integral interval for the effective cutting region. As shown in Figure 4, the intersection C=(ϕst,j(t),ϕex,j(t)) can be obtained by the intervals A=(ϕj(t,0),ϕj(t,ap)) and B=(ϕst,ϕex).(20)C=ϕsjt,ϕejt→ϕst,jt=max⁡ϕjt,0,ϕstϕex,jt=min⁡ϕjt,ap,ϕexFigure 4
The two cases of the current cutting regions: (a) or (b). Blue regions represent the portion of the workpiece. Red wavy lines represent the cutting edge of the tool.
(a) (b)whereϕst and ϕex can be calculated by radial depth of cut ae and radius of cylindrical serrated end mill shank envelope in different milling modes.(21)ϕst=π-arccos⁡1-aeR,ϕex=πdownϕst=0,ϕex=arccos⁡1-aeRup


### 2.4. Cutting Force Model

The cutting forces with serrated end mill are modeled similar to that with regular end mill when the influence of serration geometry in cutting mechanism is not considered. The helical flutes are scatted into a series of infinitesimal cutting edges. The differential tangential, radial, and axial cutting forces (dFt/dFr/dFa) can be calculated by the differential chip thickness hj(z,t) and the differential flute segment length db, which can be obtained by (25).(22)dFt=Gjz,tKtchg,jz,t+KredbdFr=Gjz,tKrchg,jz,t+KtedbdFa=Gjz,tKachg,jz,t+Kaedb(23)db=dzsin⁡κjCutting force coefficients (Ktc,Krc,Kac) and edge force coefficients (Ktc,Krc,Kac) in the tangential, radial, axial directions can be obtained by the experiment. As shown in Figure 5, differential forces (dFt,dFr,dFa) can be converted into the components in X-Y-Z coordinates.(24)dFxdFydFz=-cos⁡ϕjt,z-sin⁡ϕjt,zsin⁡κj-sin⁡ϕjt,zcos⁡κjsin⁡ϕjt,z-cos⁡ϕjt,zsin⁡κj-cos⁡ϕjt,zcos⁡κj0cos⁡κj-sin⁡κjdFtdFrdFaFigure 5
Process of serrated end mill.Instantaneous milling forces with serrated end mill can be predicted by integrating differential cutting forces along each flute in the axial direction.(25)FxtFytFzt=∑j=1N∫0apdFxt,z∑j=1N∫0apdFyt,z∑j=1N∫0apdFzt,zIn the above equation,ap is axial cutting depth with serrated end mill.


## 2.1. Serration

By varying the local radiusRj of jth flute at level z, the serration of serrated end mill can be obtained.(1)Rjz=R-△RjzR is the radius of cylindrical serrated end mill shank envelope, and z is the axial depth. △Rj(z) is the variation, which can be calculated by a sine wave with amplitude and wave length.(2)△Rjz=A-Asin⁡γz,jA is the peak-to-peak amplitude. γ(z,j) is the angle of the serration wave in the jth tooth at level ofz, which is shown in Figure 1 and obtained by (3)γz,j=2πz/cos⁡βjλ-∑k=1j-1ϕpjAs shown in Figure1, ∑k=1j-1ϕpj is the phase shift of serration wave and ϕpj is the pitch angle between the subsequence flutes at the tip of end mill.


## 2.2. Geometric Model of the Helical Cutting Edges

As shown in Figure1, the radial immersion angle of point P can be obtained as(4)ϕjt,z=ϕ10-ψjzj=1ϕ10+∑j=2Nϕpj-ψjz1<j≤Nϕ 10 is the rotation angle at level z=0, which can be seen as a reference edge. It can be determined by the spindle speed n, time t, and the initial angular position ϕ0.(5)ϕ10=2πnt+ϕ0As shown in Figure1, ψjz is the radial lag angle, which is related to axial depthz, radiusR of cylindrical serrated end mill shank envelope, and local helix angle βj in each flute. It can be calculated by (6)ψjz=ztan⁡βjRWhen the peak-to-peak amplitude A is zero, the proposed model can predict cutting forces with variable helix end mill. What is more, the proposed model can turn to be regular cutting force model if A=0 and local helix angleβj is invariable.As shown in cylindrical serrated end mill in Figure2, the point P can be determined by vector P→j(t,z) from origin O.(7)P→jt,z=Pxt,zi→+Pyt,zj→+Pzt,zk→(8)Pxt,z=Rjzsin⁡ϕjt,zPyt,z=Rjzcos⁡ϕjt,zPzt,z=Rψjztan⁡βjFigure 2
Axial immersion angle and radius.The axial immersion angleκj(t,z) is associated with the scalar product of the tangent and normal vectors, which can be obtained by (9)κjt,z=a⁡cos⁡t→jt,z·v→jt,zt→jt,zwheretj→t,z is the tangent to the serrated flute and can be expressed by (10)t→jt,z=dP→jt,zdzThe unit vector points outward inXY plane, which can be calculated as(11)v→jt,z=sin⁡ϕjt,zi→+cos⁡ϕjt,zj→Substituting (10) and (11) into (9), the full definition of axial immersion angle κj(t,z) is obtained as(12)κjt,z=acos⁡d/dzRjzd/dzRjz2+tan⁡βj/RRjz2+1


## 2.3. Chip Thickness

During milling process, the chip thickness is identified to be perpendicular to the curvature of the serrated flute. As shown in Figure3, chip thickness can be represented as the local distance between the previous and the cutting surfaces approximately in the direction of the local normal vector n→j(t,z) of the flute.Figure 3
Chip thickness with serrated end mill.The chip thickness between thejth and the (j+1)th flutes can be obtained by(13)hg,jt,z≈Δr→jt,zn→jt,zThe equation cannot strictly represent the physical chip thickness. In Figure3, the local movement of the jth flute relative to the (j+1)th flute at the same angular position can be expressed as(14)Δr→jt,z=r→jt,z-r→j-1t,z=Rjz-Rj-1zsin⁡ϕjt,z+ftjt,zRjz-Rj-1zcos⁡ϕjt,z0j≥2R1z-RNzsin⁡ϕ1t,z+ft1t,z)R1z-RNzcos⁡ϕ1t,z0j=1where the feed can be calculated as follows:(15)ftjt,z=Vfφjz2πnBetween thejth and (j+1)th flutes of serrated end mill in the axial direction, the pitch angle can be shown as(16)φjz=2π+ϕjt,z-ϕNt,z=ϕp1-ztan⁡βj+N-1-tan⁡βjRj=1ϕjt,z-ϕj-1t,z=ϕpj-ztan⁡βj-tan⁡βj+1R1<j≤NThe unit normal vector of thejth flute at level z for uneven radius can be obtained by(17)n→jt,z=sin⁡κjt,zsin⁡ϕjt,zsin⁡κjt,zcos⁡ϕjt,zcos⁡κjt,zThe effective chip thickness along axial direction can be evaluated as(18)hjt,z=Gjt,zhg,jt,zSince the milling is effective only when the edge of end mill is cutting,Gjt,z determines whether the jth tooth is cutting.(19)Gjt,z=1ϕst,j≤ϕjt,z≤ϕex,j0ϕjt,z<ϕst,j,ϕjt,z>ϕex,jϕ s j, ϕej are the positive entry angle and the positive exit angle, which can be obtained by the integral interval for the effective cutting region. As shown in Figure 4, the intersection C=(ϕst,j(t),ϕex,j(t)) can be obtained by the intervals A=(ϕj(t,0),ϕj(t,ap)) and B=(ϕst,ϕex).(20)C=ϕsjt,ϕejt→ϕst,jt=max⁡ϕjt,0,ϕstϕex,jt=min⁡ϕjt,ap,ϕexFigure 4
The two cases of the current cutting regions: (a) or (b). Blue regions represent the portion of the workpiece. Red wavy lines represent the cutting edge of the tool.
(a) (b)whereϕst and ϕex can be calculated by radial depth of cut ae and radius of cylindrical serrated end mill shank envelope in different milling modes.(21)ϕst=π-arccos⁡1-aeR,ϕex=πdownϕst=0,ϕex=arccos⁡1-aeRup


## 2.4. Cutting Force Model

The cutting forces with serrated end mill are modeled similar to that with regular end mill when the influence of serration geometry in cutting mechanism is not considered. The helical flutes are scatted into a series of infinitesimal cutting edges. The differential tangential, radial, and axial cutting forces (dFt/dFr/dFa) can be calculated by the differential chip thickness hj(z,t) and the differential flute segment length db, which can be obtained by (25).(22)dFt=Gjz,tKtchg,jz,t+KredbdFr=Gjz,tKrchg,jz,t+KtedbdFa=Gjz,tKachg,jz,t+Kaedb(23)db=dzsin⁡κjCutting force coefficients (Ktc,Krc,Kac) and edge force coefficients (Ktc,Krc,Kac) in the tangential, radial, axial directions can be obtained by the experiment. As shown in Figure 5, differential forces (dFt,dFr,dFa) can be converted into the components in X-Y-Z coordinates.(24)dFxdFydFz=-cos⁡ϕjt,z-sin⁡ϕjt,zsin⁡κj-sin⁡ϕjt,zcos⁡κjsin⁡ϕjt,z-cos⁡ϕjt,zsin⁡κj-cos⁡ϕjt,zcos⁡κj0cos⁡κj-sin⁡κjdFtdFrdFaFigure 5
Process of serrated end mill.Instantaneous milling forces with serrated end mill can be predicted by integrating differential cutting forces along each flute in the axial direction.(25)FxtFytFzt=∑j=1N∫0apdFxt,z∑j=1N∫0apdFyt,z∑j=1N∫0apdFzt,zIn the above equation,ap is axial cutting depth with serrated end mill.


## 3. Experimental Verification

The cutting force model proposed by the paper was verified with a series of cutting experiments as follows. To achieve stable milling process, milling conditions were selected. The cutting forces were recorded by the dynamometer (Kistler9257A), and the sampling frequency was 10000 Hz. The tests were conducted with workpiece material Al7075 alloy. The tests were conducted with four types of end mills which were shown in Figure6 and detailed in Table 1.Table 1
Geometry parameters of four types of end mills.
No. Type Diameter (mm) Pitch angle (°) Helix angle (°) Amplitude (mm) Wave length (mm) 1 Regular serrated end mill 10 90°-90° -90°-90° 35°-35° -35°-35° 0.3 2 2 Variable helix serrated end mill 10 96°-84° -96°-84° 44°-41° -44°-41° 0.3 2 3 Variable helix end mill 10 96°-84° -96°-84° 44°-41° -44°-41° / / 4 Regular end mill 10 90°-90° -90°-90° 35°-35° -35°-35° / /Figure 6
Four types of end mills.The average milling force method proposed by Altintas et al. [19] was used to calibrate the cutting force coefficients. According to the approach, cutting tests were conducted with constant axial depth of cut and radial depth of cut at different feed rates. Groove milling was adopted. The spindle speed was set as 2000 rpm, and the axial depth of cut was 1 mm. The feed rates were 0.01,0.015,0.02,0.025,0.03 mm/tooth. The formulas of the average cutting forces can be deduced as(26)F-=F-cft+F-ewhere(27)F-=F-xF-yF-zT,F-c=-Nap4KrcNap4KtcNapπKacT,F-e=-NapπKreNapπKteNap2KaeT.F - x, F-y, and F-z are the average forces in X, Y, and Z directions; Ktc,Krc,Kac are the cutting force coefficients, Ktc,Krc,Kac are the edge force coefficients; ft is the feed rate.The average milling forces at different feed rates are shown in Figure7. The cutting force coefficients and the edge force coefficients can be calibrated, which are listed in Table 2.Table 2
Cutting force coefficients and edge force coefficients.
No. K t c K r c K a c K t e K r e K a e 1 757.4 -260.4 -37.1 17.7 -12.9 -4.3 2 754.3 -252.5 -39.7 15.8 -11.4 -3.9 3 760.7 -255.8 -41.3 14.4 -12.0 -4.5 4 762.5 -253.4 -43.2 15.0 -11.8 -4.1Figure 7
Average cutting forces at different feed rates inX, Y, and Z directions.


### 3.1. Regular Serrated End Mill

Milling forces in three directions were measured by a dynamometer (Kistler 9257A) fixed on the worktable of the machining center. The cutting parameters of the milling process were shown in Table3 and the experimental configuration was expressed in Figure 8. Some comparisons of simulated and measured cutting forces with regular serrated end mill (No. 1) were shown by Figures 9–13.Table 3
Milling force experimental program.
Test No. Axial depth of cut (mm) Radial depth of cut (mm) Spindle speed (r/min) Feed velocity (mm/min) Mode of milling 1 2 4 2000 120 Down 2 3 4 2000 80 Down 3 3 4 2000 120 Down 4 3 4 2000 160 Down 5 4 4 2000 80 Down 6 4 4 2000 120 Down 7 4 4 2000 160 Down 8 2 4 2500 120 Down 9 3 4 2500 80 Down 10 3 4 2500 120 Down 11 3 4 2500 160 Down 12 4 4 2500 80 Down 13 4 4 2500 120 Down 14 4 4 2500 160 Down 15 2 4 3000 120 Down 16 3 4 3000 80 Down 17 3 4 3000 120 Down 18 3 4 3000 160 Down 19 4 4 3000 80 Down 20 4 4 3000 120 Down 21 4 4 3000 160 DownFigure 8
Photograph of experimental setup.Figure 9
Comparison of measured and simulated cutting forces for test 4.Figure 10
Comparison of measured and simulated cutting forces for test 6.Figure 11
Comparison of measured and simulated cutting forces for test 12.Figure 12
Comparison of measured and simulated cutting forces for test 19.Figure 13
Comparison of measured and simulated cutting forces for test 21.In the condition of down-milling, the experiments were conducted at various depths of cut, spindle speeds, and feed velocities. As shown in the results, it can be found that the simulated and measured cutting forces were essentially consistent in the peak and the approximate trend. Because of the self-excited vibration during milling process, some errors existed between the simulated and measured cutting forces within each cycle.


### 3.2. Variable Helix Serrated End Mill

In the proposed model, radial immersion angle took pitch angle and helix angle into account. As a result, it can be also utilized in predicting the cutting forces with variable helix serrated end mill (No. 2). Some comparisons of simulated and measured cutting forces with variable helix serrated end mill (No. 2) were shown in Figures14–16.Figure 14
Cutting forces with variable helix serrated end mill for test 3.Figure 15
Cutting forces with variable helix serrated end mill for test 10.Figure 16
Cutting forces with variable helix serrated end mill for test 17.Some tests were conducted with variable helix serrated end mill. The experimental program can be obtained in Table1. Figures 15–18 showed that the simulated and measured cutting forces with variable helix serrated end mill also had essential consistence in the peak and the approximate trend. The results verified the reliability of the model in predicting cutting forces with variable helix serrated end mill.Figure 17
Cutting forces for test 13: (a) regular serrated end mill; (b) regular end mill.
(a) (b)Figure 18
Cutting forces for test 13: (a) variable helix serrated end mill; (b) variable helix end mill.
(a) (b)


### 3.3. Comparison of Cutting Forces

Serrated end mills (No. 1 and No. 2) have smaller cutting forces than variable helix end mill (No. 3) and regular end mill (No. 4) in the same cutting parameters because of the serration wave, which can be observed in Figures17 and 18. In above, serrated end mill is more suitable to be used in rough cutting process than regular end mill and variable helix end mill.


## 3.1. Regular Serrated End Mill

Milling forces in three directions were measured by a dynamometer (Kistler 9257A) fixed on the worktable of the machining center. The cutting parameters of the milling process were shown in Table3 and the experimental configuration was expressed in Figure 8. Some comparisons of simulated and measured cutting forces with regular serrated end mill (No. 1) were shown by Figures 9–13.Table 3
Milling force experimental program.
Test No. Axial depth of cut (mm) Radial depth of cut (mm) Spindle speed (r/min) Feed velocity (mm/min) Mode of milling 1 2 4 2000 120 Down 2 3 4 2000 80 Down 3 3 4 2000 120 Down 4 3 4 2000 160 Down 5 4 4 2000 80 Down 6 4 4 2000 120 Down 7 4 4 2000 160 Down 8 2 4 2500 120 Down 9 3 4 2500 80 Down 10 3 4 2500 120 Down 11 3 4 2500 160 Down 12 4 4 2500 80 Down 13 4 4 2500 120 Down 14 4 4 2500 160 Down 15 2 4 3000 120 Down 16 3 4 3000 80 Down 17 3 4 3000 120 Down 18 3 4 3000 160 Down 19 4 4 3000 80 Down 20 4 4 3000 120 Down 21 4 4 3000 160 DownFigure 8
Photograph of experimental setup.Figure 9
Comparison of measured and simulated cutting forces for test 4.Figure 10
Comparison of measured and simulated cutting forces for test 6.Figure 11
Comparison of measured and simulated cutting forces for test 12.Figure 12
Comparison of measured and simulated cutting forces for test 19.Figure 13
Comparison of measured and simulated cutting forces for test 21.In the condition of down-milling, the experiments were conducted at various depths of cut, spindle speeds, and feed velocities. As shown in the results, it can be found that the simulated and measured cutting forces were essentially consistent in the peak and the approximate trend. Because of the self-excited vibration during milling process, some errors existed between the simulated and measured cutting forces within each cycle.


## 3.2. Variable Helix Serrated End Mill

In the proposed model, radial immersion angle took pitch angle and helix angle into account. As a result, it can be also utilized in predicting the cutting forces with variable helix serrated end mill (No. 2). Some comparisons of simulated and measured cutting forces with variable helix serrated end mill (No. 2) were shown in Figures14–16.Figure 14
Cutting forces with variable helix serrated end mill for test 3.Figure 15
Cutting forces with variable helix serrated end mill for test 10.Figure 16
Cutting forces with variable helix serrated end mill for test 17.Some tests were conducted with variable helix serrated end mill. The experimental program can be obtained in Table1. Figures 15–18 showed that the simulated and measured cutting forces with variable helix serrated end mill also had essential consistence in the peak and the approximate trend. The results verified the reliability of the model in predicting cutting forces with variable helix serrated end mill.Figure 17
Cutting forces for test 13: (a) regular serrated end mill; (b) regular end mill.
(a) (b)Figure 18
Cutting forces for test 13: (a) variable helix serrated end mill; (b) variable helix end mill.
(a) (b)


## 3.3. Comparison of Cutting Forces

Serrated end mills (No. 1 and No. 2) have smaller cutting forces than variable helix end mill (No. 3) and regular end mill (No. 4) in the same cutting parameters because of the serration wave, which can be observed in Figures17 and 18. In above, serrated end mill is more suitable to be used in rough cutting process than regular end mill and variable helix end mill.


## 4. Conclusions

The paper presents an analytical model, which can be utilized to predict cutting forces with serrated end mills during end milling process. The serrated end model redefines the serration and covers variable helix end mill geometries. Moreover, the model has a good spatial expressiveness and research expansibility. The following should be noted:(1) The geometric model of serrated end mill takes pitch angle and helix angle into account in each helical cutting flute. The force model can be utilized to predict cutting forces with variable helix serrated end mill.(2) Chip thickness of serrated end mill is developed in the force model, which applied spatial vector to define chip thickness so as to enhance the spatial expressiveness of the model. The characteristic of chip thickness is expressed with serrated end mill, which is discontinuous during milling process.(3) The proposed model can also be turned to be regular cutting model and is verified by experiments. Comparing with cutting forces with regular end mill and variable helix end mill, cutting forces with serrated end mills are smaller. Because of the serration wave, serrated end mill is more suitable to be used in rough cutting process.So as to verify the viability of the proposed model, various cutting tests with regular serrated end mill and variable helix serrated end mill were conducted. By comparing the measured and predicted cutting forces, the variability of the proposed model was verified. The proposed model can also be utilized to analyze the stability during end milling process and extended to be a generalized model with complex tool geometries furtherly. Besides, the proposed model also provides a reference for cutting mechanism with serrated tools, which contributes to tool optimization and design.



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*Source: 1796926-2019-03-11.xml*