Hermite Quartic Splines for Smoothing and Sampling a Roughing Curvilinear Spiral Toolpath

Abstract

From an industrial point of view, the milling of $2.5D$ cavities is a frequent operation, consuming time and presenting optimization potential, especially through a judicious choice of the tool trajectory. Among the different types of trajectories, some have a general spiral-like aspect and can potentially offer a reduced machining time. They are called curvilinear trajectories and are obtained by interpolation between structure curves, which are the numerical solutions of a partial differential equation. In this case, the machine tool will connect points, and the trajectory will be made up of small segments. While these trajectories exhibit all the necessary qualities on a macroscopic level for rapid tool movement, the tangential discontinuities at a microscopic scale, inherent in the discretization, significantly increase the machining time. This article proposes a method to reparameterize the structure curves of the curvilinear spiral with a set of $C^2$ connected Hermit quartic spline patches. This creates a smooth toolpath that can be machined at an average feedrate closer to the programmed one and will, de facto, reduce the machining time. This article shows that the proposed method increases on two representative geometries of cavities and toolpath quality indicators, and reduces the milling time from $10\%$ to $18\%$ as compared to the PDE curvilinear spiral generation method proposed by Bieterman and Sandström. In addition, the proposed method is suitable for any non-convex pocket, with or without island(s).

1. Introduction

Pocketing $2.5D$ cavities, which is common from an industrial point of view (e.g., in aeronautical structure parts or aerospace electronic crankcase), is a time-consuming operation.

As shown by [1], manufacturing costs are time dependent and typically represent, for dies and molds, $30\%$ of the total price of a piece [2].

In this context, many studies aim to reduce the machining time. The main lines for optimization are enhancing the understanding of cutting phenomena [3,4,5], improving tool performance [6], selecting the best tools, defining the optimal milling parameters [7,8,9], and, finally, enhancing the toolpath geometry [10,11,12].

From this last perspective, the most common approach is to work on the tool trajectory to increase its speed. Multiple studies (e.g., [13,14]) have demonstrated that tangency discontinuities along the trajectory result in increased machining time. These discontinuities necessitate changes in the velocity vector (both in direction and magnitude) along the trajectory, which challenges the machine tool’s acceleration and jerk capabilities. As these capacities are limited, the numerical control system of the machine imposes restrictions on these variations, so the tool requires additional time and distance to achieve the programmed feed rate after negotiating corners or halts along the toolpath. Therefore, it is essential to minimize such discontinuities, for which two methods exist:

• Local adjustments on classical toolpath (Zig-Zag or Contour Parallel) are employed to eliminate or to smooth out the discontinuities [15,16,17];
• Global strategy to build a spiral-like trajectory (or curvilinear spiral). Macroscopically, this kind of toolpath begins at a center point of the pocket and expands outward without “stop and go”. The toolpath morphs progressively to the shape of the pocket boundary. Natively, curvilinear spirals (or spiral-like toolpath) have a higher degree of continuity [18,19,20,21].

Primarily, two approaches are used to build curvilinear spirals:

• Geometrical approaches such as mapping [22,23], morphing [24], or the medial axis method [19,20];
• Differential approaches using an elliptical partial differential equation (PDE) [21] or a level-set propagation model [18]. In those cases, curvilinear trajectories are generated through interpolation between selected structure curves, which are the solutions of the used PDE.

To determine a point on a curvilinear path, an interpolation method is needed. Bieterman et al. [21] use the intersection of a Fresnel vector (winding angle) and two discrete structure curves (Figure 1). The trajectory point is established through a linear angular interpolation between the two intersecting points (Equation (1)):

$${\rho }_S\left({\theta }_i\right)={\rho }_{int}\left({\theta }_i\right)+({\rho }_{ext}\left({\theta }_i\right)-{\rho }_{int}\left({\theta }_i\right)).{\displaystyle \frac{{\theta }_i}{2\pi }},{\theta }_i\in [0,2\pi ]$$

(1)

with ${\rho }_S\left({\theta }_i\right)$, discrete polar equation of a spiral-like turn; ${\rho }_{ext}\left({\theta }_i\right)$, discrete polar equation of the external structure curve; ${\rho }_{int}\left({\theta }_i\right)$, discrete polar equation of the internal structure curve.

This method is effective when the cavity is sufficiently convex (i.e., without significant protrusions; mathematically, when the polar function of the pocket border is explicit). However, for pockets with more complex geometries, a partitioning task is required as proposed by [25] and illustrated in Figure 2.

Moreover, the structure curves are constructed through interpolations between a series of points calculated using finite element method software. In the context of G1 linear interpolation, the trajectory consists of numerous small segments. Although the trajectory may exhibit characteristics adapted to high feed rates on a macroscopic scale, the tangency discontinuities inherent to this method significantly increase the machining time on a smaller scale. Since ’polynomial’ interpolators are not yet widely adopted in the industry, efforts are needed to smooth the toolpath and improve its degree of continuity.

The simplest method to achieve this objective is the use of a Finite Impulse Response filter (FIR); [21] suggests a moving average technique. However, the use of such filters may result in a loss of tool position control, potentially leading to a machining in inappropriate zones. Other various studies [22,26,27] achieve three of five-axis trajectory smoothing, via B-splines or Bézier curves.

Table 1. Research timeline.

Years	Authors	Main Focuses	Benefits and Limitations
<2000	Held	Generation of toolpaths on arbitrary geometry Zig-zag or parallel contour	/
2003	Bieterman [21]	Spiral toolpath PDE approach	Suitable only for globally convex pocket Not suitable for pocket with island
2004	Pateloup [28]	Corner smoothing	Local smoothing
2009	Held [29]	Spiral toolpath Geometric approach	Use of Voronoï diagrams Not suitable for island
2011	Xiong [18]	Spiral toolpath PDE approach Level set propagation	No smoothing Suitabel for pockets with island but with composite spiral
2011	Banerjee [30]	Spiral toolpath PDE approach	Only globally convex pocket Suitable for pocket with a centered island $G^1$ toolpath
2013	Xu [23]	Spiral toolpath Geometric approach Mapping	Not suitable for pocket with island No smoothing
2018	Held [19]	Spiral toolpath Geometric approach	Simplier to implement Polygonal spiral ($G^0$)
2023	Hua [27]	Curve smoothing B-Spline	Not integrated in a spiral construction

shows a summary of the methods proposed in the literature summarizing their main focuses.

This article proposes a method to reparameterize the structure curves of the curvilinear spiral with a set of Hermit quartic spline patches $C^2$ connected (continuity in tangency and curvature). Analytically, the spiral-like toolpath, formed through linear combination of these curves, maintains the $C^2$ continuity, ensuring a smaller machining time.

Moreover, the proposed method eliminates the need of Fresnel’s vector to establish the spiral parametrization, so the toolpath can be directly created without partitioning the pocket. It allows a generalization of Bieterman’s procedure for any $2.5D$ pocket geometries, even with non-convex geometry.

2. Methodology for Smoothing Toolpaths

Figure 3 summarizes the proposed method and the structure of the following paragraphs.

2.1. Determining a Closed Contour

The first step involves establishing a closed contour to define a layer of the $2.5D$ pocket, which will be milled layer by layer. As the paper is focused on the roughing operation, an offset distance from the border must be accounted for regarding the radial width of the cut of the finishing pass ($D_{offset}={\displaystyle \frac{{\varphi }_{tool}}{2}}$).

2.2. Solving a Steady State Thermal Problem

Given their smooth nature [31], the solutions of a $2D$ thermal problem (i.e., isotherms) are chosen for building structure curves: a layer of the pocket is uniformly heated while the border is maintained at $0\left[K\right]$. The heat equation is (Equation (2)):

$$\rho c{\displaystyle \frac{\partial T}{\partial \tau }}=\overrightarrow{\nabla }\left(\lambda \overrightarrow{\nabla }T\right)+q,\partial \Omega =0\left[K\right]$$

(2)

with $\rho$, the areal density of the layer [kg/m²]; c, the specific heat of the layer [J/(kgK)];$T(x,y)$, the temperature field on the layer [K]; $\tau$, the time [s]; $\lambda$, the thermal conductivity of the material [W/K]; q, the areal heat source [W/m²]; $\partial \Omega$, the border condition.

The stationary equation with $q=1[W/m^2]$ and $\lambda =1[W/K]$ is expressed in Equation (3) and is equivalent to Equation (4) proposed by [21]. Note that the values of q and $\lambda$ do not alter the general shape of the solution temperature field but only impact the maximum temperature:

$$-\Delta T={\displaystyle \frac{q}{\lambda }},\partial \Omega =0\left[K\right]$$

(3)

$$-\Delta \varphi (x,y)=1,\partial \Omega =0$$

(4)

2.3. Building Smooth Curves from Temperature Field

Equation (3) is solved using a classical finite element method (FEM). Some isotherm curves from the resulting temperature field can be used to construct the spiral-like trajectory. However, due to the discretization inherent in FEM and the necessary interpolations, these curves are microscopically noisy and exhibit tangency discontinuities. To address this issue, a fitting-smoothing method is implemented.

2.3.1. Hermite Quartic Spline Interpolation

The Hermite quartic spline interpolation model (HQS) was presented by [32] and is a generalization of the usual Hermite cubic spline interpolation. The general form of the HQS interpolation is (Equation (5)):

$$\left\{\begin{array}{c}x\left(u\right)=e{a}_0\left(u\right)x_0+e{a}_1\left(u\right)x_1+e{b}_0\left(u\right)cos\left({\theta }_0\right)+e{b}_1\left(u\right)cos\left({\theta }_1\right)\hfill \\ y\left(u\right)=e{a}_0\left(u\right)y_0+e{a}_1\left(u\right)y_1+e{b}_0\left(u\right)sin\left({\theta }_0\right)+e{b}_1\left(u\right)sin\left({\theta }_1\right)\end{array}\right.$$

(5)

with $P_u=\left(x\left(u\right),y\left(u\right)\right)$, the coordinates of an interpolated point; $u\in \left[0,1\right]$, the real interpolant; $(x_0,y_0)$, the coordinates of the spline first point ($u=0$); $(x_1,y_1)$, the coordinates of the spline last point ($u=1$); ${\theta }_0$ and ${\theta }_1$, the orientations of the tangent at the beginning and at the end, respectively; and $e{a}_0,e{a}_1,e{b}_0,e{b}_1$, the blending functions (“e” is for extended).

The degree of blending function equals to 4 and, thereby, 5 constraints are allowed and detailed below.

• The spline passes over two points $P_0$ and $P_1$: +2 constraints;
• The spline respects tangent orientations at the beginning and at the end: +2 constraints;
• An initial curvature $C_0$ is fixed: +1 constraint.

The blending functions are described with four parameters: $k_0,k_1,\alpha ,\beta$ (Equation (6), Figure 4). If $\alpha$ and $\beta =0$, blending functions are those of classical cubic Hermite splines.

$$\left\{\begin{array}{c}e{a}_0\left(u\right)=1+(\alpha -3)u^2+2(1-\alpha )u^3+\alpha u^4\hfill \\ e{a}_1\left(u\right)=(3-\alpha )u^2+2(\alpha -1)u^3-\alpha u^4\hfill \\ e{b}_0\left(u\right)=k_0\left(t+(\beta -2)u^2+(1-2\beta )u^3+\beta u^4\right)\hfill \\ e{b}_1\left(u\right)=k_1\left(-(\beta +1)u^2+(2\beta +1)u^3-\beta u^4\right)\hfill \end{array}\right.u\in [0,1]$$

(6)

• $k_0$ and $k_1$ do not affect the orientation of the tangent, only the norm of the tangent vector;
• $\alpha$ and $\beta$ are called shape parameters and allow the shape modification of blending functions.

The initial curvature ($C_0$) is a complex function of $k_1$, $k_2$, $\alpha$ and $\beta$ (Equation (7)):

$$C_0=C{]}_{u=0}={\displaystyle \frac{\frac{dx}{du}.\frac{d^{2}x}{d{u}^2}-\frac{dy}{du}.\frac{d^{2}y}{d{u}^2}}{{({\frac{dx}{du}}^2+{\frac{dy}{du}}^2)}^{\frac{3}{2}}}}{]}_{u=0}=f_0(k_1,k_2,\alpha ,\beta )$$

(7)

But this expression can be analytically inverted to isolate $\beta$ by the use of the Symbolic Toolbox of MatLab, for example (Equation (8)). The final curvature is obtained in the same way but for $u=1$ in Equation (7) and is noted as $C_1=f_1(k_0,k_1,\alpha ,\beta )$:

$$\beta =f_0^{-1}(C_0,k_1,k_2,\alpha )$$

(8)

2.3.2. From Interpolation to Smooth Curve Decomposition

This model of interpolation, between two points, makes it possible to fit and decompose a discrete curve, in this case, an isotherm, into a small number of splines connected in tangency and curvature (named patches). Figure 5 explains the procedure followed.

$D_{max}$ is the maximum acceptable distance between the curve and patch points; $C_0$ represents the algebraic initial curvature of the first patch. $D_{max}$ and $C_0$ are user-fixed parameters. $D_{opt}$ is the optimized (i.e., minimized) distance between the patch points and HQ spline. GA is for the Genetic Algorithm method, and GM is for the gradient descent method. $C_1$ is the calculated final curvature of the patch that becomes the initial curvature of the new patch.

By using this procedure, a discrete isotherm may be split into a minimum number of Hermite quartic splines, continuous, connected in tangency and curvature (called isoHQ), and respecting a maximum chordal error.

2.4. Selecting Structure Curves

To select the structure curves among isotherms and to build the toolpath, isotherms are first decomposed into isoHQ and then sampled.

The analytical expression of patches, along with Equation (9), enables the computation of the curvilinear length of each patch ($s_{patch}$) and, consequently, the total length of an isoHQ. Using normalization (the normalized length is set to one), points can be sampled, equally spaced along an isoHQ:

$$s_{patch}={\int }_0^1\sqrt{({\displaystyle \frac{dx\left(u\right)}{du}}{)}^2+({\displaystyle \frac{dy\left(u\right)}{du}}{)}^2}du$$

(9)

The selection of the structure curves is performed by evaluating the distance ($D_{isoHQ}$) between sampling points of 2 isoHQ (an external one $isoH{Q}_{ext}$ and an internal one $isoH{Q}_{int}$) and linking it with an acceptable distance ($D_{rte}$) equal to the radial tool engagement. If $P_j\in isoH{Q}_{ext}$ and $Q_i\in isoH{Q}_{int}$, Equation (10) is computed:

$$D_{isoHQ}=MA{X}_j\left\{MI{N}_i\left[\sqrt{{(P_j\left(x\right)-Q_i\left(x\right))}^2+{(P_j\left(y\right)-Q_i\left(y\right))}^2}\right]\right\}$$

(10)

• If $D_{isoHQ}<D_{rte}$, the work is restarted with a more internal $isoH{Q}_{int}$;
• If $D_{isoHQ}>D_{rte}$, the penultimate evaluated $isoH{Q}_{int}$ is chosen as the structure curve, and the loop is restarted.

Thereby, the distance between two structure curves is under control and always under $D_{rte}$, which guarantees machining without unmilled areas.

2.5. Building Curvilinear Spiral

To build a curvilinear spiral, a linear interpolation between points $(xis{o}_i\left(j\right);yis{o}_i\left(j\right))$ and $(xis{o}_{i+1}\left(j\right);yis{o}_{i+1}\left(j\right))$ of the same normalized curvilinear abscissa of two consecutive structure curves is achieved (Figure 6, Equation (11)):

$$\left\{\begin{array}{c}x{s}_i\left(j\right)=xis{o}_i\left(j\right)+{\displaystyle \frac{j}{n}}\{xis{o}_{i+1}\left(j\right)-xis{o}_i\left(j\right)\}\hfill \\ y{s}_i\left(j\right)=yis{o}_i\left(j\right)+{\displaystyle \frac{j}{n}}\{yis{o}_{i+1}\left(j\right)-yis{o}_i\left(j\right)\}\hfill \end{array}\right.$$

(11)

with $x{s}_i\left(j\right)$ and $y{s}_i\left(j\right)$, the coordinates of the point j from the turn i of the curvilinear spiral, and n, the total number of points along the isotherms.

3. Toolpath Quality Evaluation

As shown in many research works, notably in [13,14], discontinuities in the tangency and curvature of the toolpath geometry challenge the limited acceleration and jerk of each axis of the numerically controlled machine tool. Therefore, the average speed rate is always lower than the programmed one, and the milling time is longer than expected.

Here, a double objective is pursued: increasing the speed along the toolpath (which can reduce milling time) and mastering the position of the tool along the milling path. For the tool speed evaluation, two methods are employed:

• A local approach: VPOp.
• A global approach: Toolpath absolute curvature value.

VPOp (Velocity Profile Optimization—version 2.6) is licensed software developed by X. Beudaert and et al. [33]. Based on kinematic data and the CNC parameters of a given machine tool, it generates optimized feedrate planning that respects the capabilities of the milling center and thus predicts the actual tool speed and slowdowns for the tool. So, the modelized milling time is close to the real one. VPOp is used locally to analyze the velocity profile along two turns of the curvilinear spiral.

To analyze the entire trajectory, histograms of the toolpath absolute curvature value ($\left|C\right|$ in mm⁻¹) are used as well as $95\%$ and $99\%$ quantiles of $\left|C\right|$ named Cut95 and Cut99. These last indicators can quickly give, unlike VPOp, the geometrical quality of a toolpath and, consequently, the possibility of NC to respect the programmed feed rate.

A comparison will be made between the “no fitted” toolpath (called RAW) and the fitted one with HQS method (called HQS). For another comparison point for milling time, a filtered toolpath is also computed, called FIR, and corresponding to a moving average on three points applied twenty times (this combination gives results close to the HQS method). Note that the more the filter is applied, the smoother the trajectory but the more the position control is lost. So, the FIR toolpath is absolutely not suitable to satisfy our goal.

4. Case Study 1—BIG Pocket

4.1. Fitting and Selecting Structure Curves

The $2.5D$ pocket given by M. Bieterman and D. Sandström [21] is considered for this work. Because it presents a large variety of tangency and curvature values, this pocket is a good test for the proposed algorithm.

With the conditions exposed in Section 2.4, a temperature field is computed using a finite element method ($12.{10}^3$ nodes). The maximum temperature is around $500\left[K\right]$. The mesh and some isotherms are shown in Figure 7. Our following analysis considers 100 of them; note that the temperature rises from the outside to the inside of the pocket.

To fit isotherms with HQS patches, the parameter $D_{chord}$ must be fixed. A too small value increases the number of patches, and the local smoothing is less efficient. On the other hand, a higher value may cause over-machining of the pocket’s border. $D_{chord}=0.5$[mm] seems, in this case, to be a good compromise but remains a parameter.

At this stage of the work, our fitting method splits each discrete isotherm (composed with a maximum of about 2500 points) into a maximum of about 25 $C^2$ connected patches. Figure 8 shows the result of a fit along an isothermal curve. Note that the beginning of the isotherm is chosen in a low-curvature zone. So, the initial curvature of the first patch is arbitrarily fixed at 0.1 [mm⁻¹] to respect the curvature orientation. As a reminder, the first patch and the last one of each isoHQ are only $C^0$ connected.

Now, a sample of each isotherm as described above must be performed. In total, 360 points are used to represent an isoHQ (Figure 9).

For this work, the tool diameter is fixed at 10 [mm] with a radial covering of $25\%$: the acceptable distance ($D_{rte}$) between two isotherms is 7.5 [mm]. Figure 10a shows the 23 automatically selected structure curves.

4.2. Building and Evaluation of Curvilinear Spiral

Finally, each revolving of curvilinear spiral is built by linear interpolation between two points of the same index (i.e., the same normalized curvilinear abscissa) of two consecutive structure curves. Figure 10b shows the curvilinear spiral built with our method.

Locally, the feedrate is simulated with VPOp. Two turns of the curvilinear spiral are chosen in three zones of the pocket (internal, intermediate, and external). The modeled machine tool is a Mikron UCP710. Its characteristics are reported in

Table 2. Kinematic characteristics of the Mikron UCP710 machine tool [34].

Mikron UCP710	${\mathbf{V}}_{\mathbf{max}}[\mathbf{m}/\mathbf{min}]$	${\mathbf{a}}_{\mathbf{max}}[\mathbf{m}/{\mathbf{s}}^2]$	${\mathbf{J}}_{\mathbf{max}}[\mathbf{m}/{\mathbf{s}}^3]$
$X_m$	30	$2.5$	5
$Y_m$	30	3	5

[34].

For each zone, three fitting methods are tested (RAW = no fit, FIR = moving average, HQS = Hermite quartic spline interpolation), and the toolpath length and the milling time are collected. The average feed rate is calculated. The programmed feed rate ($V_m$) is fixed at 10,000 [mm/min]. Data are summarized in

Table 3. Simulated milling time for 3 fitting methods.

Toolpath Location	Fitting Method	Toolpath Length [$\mathbf{mm}$]	Milling Time [s]	Δt/t [%]	$\overline{{\mathbf{V}}_{\mathbf{m}}}$ [mm/min]
Internal	RAW	346	19	/	1092
	FIR	345	15.5	−18	1335
	HQS	328	15.8	−17	1245
Intermediate	RAW	650	22	/	1773
	FIR	645	17	−22	2276
	HQS	635	18.5	−16	2059
External	RAW	1383	32.3	/	2569
	FIR	1358	29	−10	2810
	HQS	1398	29	−10	2892

, and Figure 11 shows the velocity profile as a function of the curvilinear abscissa for the three intermediate toolpaths (black = RAW, blue = HQS, red = FIR). Figure 12 links the velocity profile with the positions of the tool along the curvilinear spiral turns. Slowdowns for points A, B, C, E, F, G are due to the “high” curvature of the toolpath. D and H are, in fact, the beginnings of a curvilinear spiral turn, and there, as already explained, the $C^2$ connectivity is lost.

The results in Table 3 demonstrate that the method proposed in the paper, based on the reconstruction of isothermal curves with a small number of Hermite quartic spline patches, reduces the simulated milling time by 10% to 20% in each zone of the pocket, compared to the RAW toolpath. Although the FIR filter is selected for comparison, the HQS method offers an advantage: it maintains control over the distance between the RAW isotherm and the fitted one, a feature not preserved by the FIR method.

The histogram in Figure 13 and the statistical indicators in

Table 4. BIG pocket—curvature statistical indicators of entire curvilinear spiral.

	Curvature Absolute Value (|C|, mm−1)
	RAW	HQS
Cut95	0.24	0.14
Cut99	1.30	0.97

confirm the improvement of the toolpath: small curvatures are more populated, and both Cut95 and Cut99 values are significantly lower for the HQS method. Moreover, this new method eliminates the need for a Fresnel vector to generate the toolpath. Consequently, the limitation of using the Bieterman’s method exclusively for ’globally convex pockets’ is no longer necessary. Therefore, the HQS method allows the creation of curvilinear toolpaths similar to those by Bieterman and Sandström but applicable to non-convex cavities as demonstrated in the second case study.

5. Case Study 2—HUG Pocket

The second test case is a pocket with a similar geometry to the pocket proposed by Huang [35]. The major interest of this geometry is its non-convexity: the winding angle (Fresnel’s vector, a polar parametrization) approach proposed by Bieterman [21] is not functional, while the method proposed in this paper can handle such geometries. Figure 14 shows that our isotherms reconstruction method works for building a curvilinear spiral for “globally non-convex” pockets. It is built between 17 isotherms and constructed with around 6500 points. Note that the temperature field has two global maxima symmetrically disposed with the pocket axis: two beginning points for the curvilinear spiral are possible.

Toolpath Quality Indicators

Figure 15 shows a histogram of curvature for the entire curvilinear spiral.

As mentioned earlier, the method proposed by Bieterman is unable to generate a toolpath for this pocket. The comparison will be made using only RAW and HQS structure curves (isotherms). As in the previous case, three isotherms are selected (Figure 16): external (iso3), intermediate (iso10), and internal (iso14). The histograms (Figure 17), statistical indicators (

Table 5. HUG pocket—curvature quality statistical indicators.

	Curvature Absolute Value (|C|, mm−1)
	Entire Spiral
Cut95	0.12
Cut99	0.72
	Iso3		Iso10		Iso14
	RAW	HQS	RAW	HQS	RAW	HQS
Cut95	0.38	0.07	0.45	0.07	0.44	0.10
Cut99	1.07	0.08	1.05	0.13	1.51	0.12

), and simulated milling time (

Table 6. Simulated milling time comparison for 3 structure curves.

Toolpath Location	Fitting Method	Milling Time [s]	Δt/t [%]
Internal (Iso14)	RAW	9	/
	HQS	7.3	−19
Intermediate (Iso10)	RAW	15.2	/
	HQS	12.2	−20
External (Iso3)	RAW	22.3	/
	HQS	17	−24

) demonstrate the geometric improvement in the toolpath quality. In each case, the curvature distribution is more concentrated, and Cut95 and Cut99 values are significantly lower. Additionally, the simulated milling time along each isotherm decreases by approximately 20%.

6. Conclusions

This article proposes a new method to construct curvilinear spiral toolpaths from structure curves obtained by the FEM solution of PDE inspired from a thermal problem. To reduce the tangency discontinuities due to discretization, the structure curves of the spiral are rebuilt with Hermit quartic spline patches. This method performs the following:

• Models structure curves for any geometry of pockets thanks to the associated thermal model;
• Guarantees a $C^2$ continuity of the structure curves and enhances the continuity level of the curvilinear spiral;
• Creates a toolpath having, globally, a low curvature;
• Allows the user to define a maximum chordal error along the structure curves.

Two representative geometries of pockets are used as examples and show reductions of 10 to 18% of machining time as compared to the state of the art. The proposed method also offers a generalization to non-convex pockets as compared to methods from the literature.

In the future, the goal will be the use of Hermite quartic curves directly in a numerical controller that can handle spline interpolations.