Heat accumulation due to successive laser pulse (HAP) incident on the same spot and heat accumulation due to successive scans (HAS) of the laser beam over the same spot significantly influences the process result, especially when the resulting temperature of the workpiece exceeds the melting temperature. In particular, heat accumulation is one of the dominating effects during short-pulse laser functionalization of surfaces and strongly affects the resulting surface structures. Within this study, a novel heat accumulation model is introduced to calculate the temperature increase in the workpiece for the whole process including the effects of HAP and HAS in which the latter is differentiated between heat accumulation due to multiple passes (HAS-I) and heat accumulation due to multiple layers (HAS-II). With the new model, the surface structure was successfully predicted when using an ultra-short pulsed (USP) laser with an average power of 420 W for laser surface structuring of polished AISI 316L.
Heat accumulation occurs when the time between successive heat inputs on the same spot is too short for the processed material to cool down to the initial temperature . The thus occurring gradual temperature increase eventually causes the temperature of the workpiece to exceed a given critical value Tcrit, e.g., the melting temperature Tmelt. Heat accumulation can, therefore, constitute a distinct processing limit [2, 3]. When processing with a pulsed laser beam, the heat accumulation from pulse to pulse (HAP) is determined by the number Npps = ds \(\cdot\) f/vfeed of pulses that are incident at one spot, where ds is the diameter of the laser beam on the surface of the workpiece, f is the pulse repetition rate of the laser, and vfeed is the feed rate.
In many processes, e.g., surface structuring and surface ablation, the workpiece is processed along parallel arranged lines [4,5,6,7] as exemplarily sketched in Fig. 1a. The solid red arrows represent the path of the center of the laser beam during the processing of the surface and the dashed red lines indicate the positioning of the laser beam between two successive processing lines. During this repositioning step, the laser is off. The length of the processing lines is ℓ and the distance between the adjacent lines is dℓ. An alternative scanning strategy with shorter repositioning paths and alternating feed direction on the processing lines is discussed in the “Appendix”. When the hatching distance dℓ of adjacent lines is smaller than the focal diameter ds, every spot within the processed area is scanned more than once. This is shown in Fig. 1b, with an example showing one pulse for each processing line to visualize the multiple interactions with a given point as marked by the white cross. This results in a number Npasses = ds/dℓ of passes of the laser beam over one spot which causes the heat accumulation between multiple scans (HAS-I). The time interval between two successive passes depends on the scanning strategy.
Figure 1 illustrates the path of the laser beam covering a given area to ablate one layer of the material. The ablation of several layers is usually necessary to reach the desired ablation depth. The number Klayers of layers required to reach the desired depth depends on the amount of ablation obtained by one single-processing layer which on its turn depends on the processing parameters. Different orientations of the beam trajectories for subsequent layers may be applied. The simplest method is to proceed the same way on every processing layer. Better processing results may be achieved when rotating the beam trajectory by an angle, e.g., 45° or 90° for each subsequent processing layer as, e.g., reported in . Additionally, the feed rate or the hatching distance may also be changed. The processing strategy, therefore, determines the time elapsing from layer to layer.
For the present study, a home-build mJ-ps-laser (wavelength λ = 1030 nm, pulse duration 8 ps, pulse energy EP = 1.4 mJ, pulse repetition rate f = 300 kHz) was used . Between two successive pulses, the thermal diffusion length is ℓdiff = (4·κ/f)0.5 = 7.11 µm , where κ = 3.75 × 10−6 m2/s is the thermal diffusivity of the processed material. Since this is small compared to the diameter ds = 500 µm of the beam on the workpiece used in this study, 1D heat flow can be assumed for the time between two consecutive pulses . For the larger number Npps = ds \(\cdot\) f/vfeed of pulses incident on one spot during a single pass of the laser beam, the thermal diffusion length modifies to ℓdiff = (4·κ·Npps/f)0.5 = (4·κ·ds/vfeed)0.5 . With ds = 500 µm, the 1D approximation of the heat flow induced by one isolated single pass of the laser beam is, therefore, justifiable for feed rates well above 0.03 m/s. When the ablation of a larger area is considered as sketched in Fig. 1, the relevant thermal diffusion length (assuming immediate reposition between the scan lines) is ℓdiff = (4·κ·(M·dℓ/vfeed))0.5, where M = 160 is the number of processing lines considered in this study. This diffusion length is found to be smaller than the width b = 10 mm of the processed square as long as the feed rate exceeds 0.24 m/s. The lowest applied feed rate in this study was 1 m/s, and therefore, we may assume 1D heat flow for all applied parameters.
When ablating several consecutive layers, one should also take into account that every processed layer may lead to a change of the surface topography, which can lead to a change of the absorptance of the surface for one layer to the next [10,11,12].
Analytical model of the heat accumulation
The heat accumulation during pulsed laser materials processing has already been widely investigated [1, 2, 7, 10,11,12]. Every successive laser pulse contributes to the temperature increase of the workpiece. The absorbed part of the pulse energy EP is determined by the absorptance ηabs, which depends on the material (absorptivity) and the geometry of the interaction zone (multiple reflections). Part of the absorbed energy ηabs·EP is consumed for the actual ablation process but a fraction ηheat of the absorbed energy remains in the workpiece as what is sometimes termed residual heat. The residual heat left in the workpiece after each laser pulse is, therefore, given by Q = ηHeat \(\cdot\) ηabs \(\cdot\) EP. The material properties, the surface roughness, and the surface temperature influence both ηabs and ηHeat [13,14,15,16]. An average absorptance of ηabs = 0.55 during processing of stainless steel AISI 316L was used for the modeling. For the residual heat we adopt ηHeat = 0.38 as reported in .
Heat accumulation between multiple pulses (HAP)
The temperature distribution caused by the heat flow into the material depends on the deposited heat and on the material properties (density ρ, heat capacity cp, and thermal diffusivity κ) of the processed workpiece. The basic equations describing the heat accumulation between consecutive heat inputs were derived in  together with a detailed discussion of the necessary assumptions. For 1D heat flow, the temporal evolution of the resulting temperature increase caused by HAP on the processed surface of the workpiece just before the incidence of the subsequent pulse can be approximated by 
where f is the pulse repetition rate, ds is the diameter of the laser beam on the surface of the workpiece, and t > 0 is the duration of the processing. The first term is the (residual) heat input, the second term is given by the material properties, and the last term determines the temporal evolution of the temperature increase. The dashed green line in Fig. 2 shows the calculated temperature increase occurring during processing of AISI 316L (material properties at 20 °C: ρ = 8000 kg/m3, cp = 500 J/(kg K), κ = 3.75 × 10−6 m2/s, ηabs = 0.55, ηHeat = 0.38 ) with a resting laser beam with EP = 175 µJ and f = 300 kHz, ds = 90 µm. The red line represents the melting temperature when assuming an initial temperature of 22 °C. When the considered laser beam is moved over the workpiece with a velocity of vfeed = 2.0 m/s, the irradiation at a given point on the surface ends after the time tirr = ds/vfeed = 45 µs.
To model the decreasing temperature after the end of the irradiation time, according to  Eq. (1) can be extended by adding an identical negative heat source for the times t > tirr = ds/vfeed. The modified Eq. (1) then reads
where Θ is the Heaviside step function. For the above example, the solution of Eq. (2) is shown by the magenta line in Fig. 2. For t < tirr Eq. (2) is identical to Eq. (1). For t ≥ tirr the considered point on the surface is not heated anymore and the cooling caused by the heat dissipation into the workpiece leads to the gradually diminishing temperature as illustrated by the magenta line in Fig. 2.
Heat accumulation between multiple passes (HAS-I)
Based on Eq. (2), one can easily model the temperature evolution occurring during a process with multiple passes of the laser beam over one and the same point (HAS-I) by
where tpass is the time elapsing between two consecutive passes of the laser beam over the same spot, and N ∈ ℕ.
With the process strategy sketched in Fig. 1a, the time between successive passes over a given point is given by tpass = ℓ/vfeed + (ℓ2 + dℓ2)0.5/vpos, where vpos is the feed during repositioning. When vfeed ≪ vpos, the second term can be neglected.
Heat accumulation between multiple layers (HAS-II)
For the sake of simplicity, we assume that every layer is processed with the same scanning strategy, hence without rotating the scanning pattern, with the same feed of the laser beam on the surface, and with the same process parameters. When tpass and the number of lines M is known, the time interval between two consecutive layers is tlayer = M \(\cdot\) tpass. For the scanning strategy shown in Fig. 1a, the temperature increase caused during the ablation of the surface layer by layer yields
where K ∈ ℕ, and N ∈ ℕ.
Surface structuring of AISI 316L
When the accumulated heat leads to a temperature of at least Tbump = 607 °C, the ablated surface of the CrNi-Steel AISI 304 was found to be covered with small bumps with sizes in the range of few microns . We have experimentally investigated this transition using rolled, non-treated square plates (50 × 50 mm2) of AISI 316L (ρ = 8000 kg/m3, cp = 500 J/(kg K), κ = 3.75 × 10−6 m2/s, ηheat = 0.38) having a thickness of 2 mm. The workpiece was mounted on a flat steel block (70 × 100 × 10 mm3) which served as a heat sink. The laser-processed surfaces were examined by means of SEM and a white-light interferometer. The experiments were performed with a home-build mJ-ps-laser operating at a wavelength of λ = 1030 nm, with a pulse repetition rate of f = 300 kHz, and a pulse duration of τ = 8 ps. The workpiece was placed in the defocus of the focusing optics in a way to result in a beam diameter on the surface of the workpiece of ds = 500 µm resulting in a mean fluence of H = 0.71 J/cm2 ± 0.06 J/cm2. The uncertainty of the fluence results mainly from the experimental determination of the beam diameter of about ± 4%. The scanning pattern consisted of 160 parallel arranged lines (see Fig. 1a) with a length of ℓ = 10 mm. The hatching distance dℓ was either 62.5 or 125 µm resulting in Npasses = 8 or Npasses = 4, respectively. Since the experiments took place at room temperature, the temperature increase required to reach Tbump was given by ΔTbump = 585 K and the temperature increase at which Tmelt was exceeded was ΔTmelt = 1500 K. Which of the two temperatures constitutes a process limit depends on the application and the desired processing result. A mean fluence of H = 0.71 J/cm2 was used together with different feed rates to investigate the relevance of Tbump as well as Tmelt. The applied mean fluence is well above the ablation threshold 0.1 J/cm2 of stainless steel [19,20,21]. The feed rates were adapted in a way to result in maximum surface temperatures well below as well as above the temperatures Tbump and Tmelt during processing a single layer. The transition over the critical temperature Tbump was additionally investigated to analyze the influence of the changing absorptance during multiple-layer processing .
The temperature increase due to heat accumulation (HAP and HAS-I) was calculated with Eq. (3) using the material parameters listed above. Four different feed rates were applied for a mean fluence of 0.71 J/cm2: 1.0 m/s, 5.0 m/s, 10.0 m/s, and 20.0 m/s. The uncertainty of every applied feed rate is due to the accuracy of the galvo-mirrors in the scanner and was about 2%. Figure 3 shows the temperature increase expected for the said processes. Since Npasses = 8 (see above) the temperature reaches eight peaks. The temporal distance between the eight peaks, and therefore, the duration of the cooling phase between the upcoming and the current beam pass decreases with increasing feed rate. Due to the heat accumulation the upcoming peak is higher than the current one. For the considered mean fluence of 0.71 J/cm2 a feed of 20.0 m/s (green line in Fig. 3) results in a maximum temperature increase of ΔT = 385 K which is well below ΔTbump. The surface resulting from this process should be smooth. Decreasing the feed rate to 10 m/s (black line in Fig. 3) leads to a maximum temperature increase of ΔT = 585 K which is slightly below ΔTbump. The surface resulting from this process may therefore show the transition from a smooth surface to a bumpy surface. Further decreasing of the feed rate to 5.0 m/s (magenta line in Fig. 3) leads to a maximum temperature increase of ΔT = 860 K which is well below ΔTmelt and significantly above ΔTbump. The surface resulting from this process should be covered with well-pronounced grooves. Applying a feed rate of 1.0 m/s (blue line in Fig. 3) results in a maximum temperature increase of ΔT = 2030 K which is well above ΔTmelt. The surface resulting after this process is expected to show signs of solidified melt, and therefore, significantly differ compared to a surface processed with the higher feed rates.
The above predictions on the expected surface quality were verified by experiments with the same parameters as used to calculate the results shown in Fig. 3. Figure 4 shows SEM images of the surfaces that were processed with a mean fluence of 0.71 J/cm2 per pulse and the feed rates 1.0 m/s, 5.0 m/s, 10.0 m/s, and 20.0 m/s. As expected, the processed areas show laser-induced periodic surface structures (LIPSS). According to , the LIPSS can be classified in ripples, grooves, and spikes, where grooves and spikes correspond to a bumpy surface structure . For the highest feed rate of 20.0 m/s, only ripples can be recognized in Fig. 4a. As expected from theory, the critical temperature required for the formation of bumps (grooves and spikes) was not reached. Decreasing the feed rate to 10.0 m/s leads to the creation of fine grooves and ripples on the surface (see Fig. 4b) as the temperature according to theory is in the range of Tbump. Applying a feed rate of 5.0 m/s leads to a surface that exhibits grooves covered with ripples as shown by Fig. 4c. The occurrence of grooves confirms the theoretical expectation that at these parameters the temperature increase exceeds ΔTbump which according to  leads to a bumpy surface. Further decreasing the feed to 1.0 m/s leads to a surface which is covered with micro-holes (Fig. 4d) which is a clear sign that the laser pulses interacted with a liquid surface. Hence, the experimental results are well consistent with the above theory.
To quantify the process-resulting roughness, all surfaces shown in Fig. 4 were additionally examined by means of a white-light interferometer to determine the mean roughness depth SRz. We performed five measurements on every processed area as well as on an untreated area. In Table 1 the mean values of SRz with corresponding standard deviation are listed for all resulting surface structures shown in Fig. 4. The mean roughness depth of an untreated area is 0.076 µm. After processing the mean roughness depth is significantly increased, e.g., applying a feed rate of 20 m/s results in a mean roughness depth of 1.298 µm. When the feed rate is decreased the mean roughness depth increases further. This is tantamount to rougher surfaces (see Fig. 4), and therefore, the mean roughness depth is a suitable parameter to describe the transitions from a smooth surface (covered only with ripples) to a bumpy surface.
For the investigation of the additional impact of HAS-II we consider a mean fluence of 0.71 J/cm2 combined with a feed rate of 10.0 m/s and a hatching distance of dℓ = 125 µm resulting in Npasses = 4 to reduce the maximum temperature increase per layer. According to Fig. 3, this leads to maximum temperature increase of 490 K during the first layer which is just 110 K below ΔTbump. The complete temperature increase caused by all three heat accumulation effects together (HAP, HAS-I, and HAS-II) was calculated with Eq. (4), again with the same material and scanning parameters as listed above. All material parameters were assumed to be constant. Taking this into account, the temperature increase calculated with Eq. (4) for the process of the first 50 layers is shown in Fig. 5. According to the used parameters Npasses equals 4 (compare Fig. 3). Hence, the peaks seen in Fig. 5 actually are four peaks that, however, are not resolved in the picture as they are so close to each other. One can see that the critical temperature increase ΔTbump is reached in the range around the eighth and tenth layer.
The state of the surfaces that were observed after the ablation of different numbers of layers using the same parameters as discussed above are shown by the SEM images in Fig. 6. After the ablation of the first layer (Fig. 6a), the resulting surface is homogeneously covered with fine ripples. Processing two layers (Fig. 6b) leads to the formation of more pronounced ripples. This still applies for the resulting surface after the process of five layers as shown by Fig. 6c. Nevertheless, rougher ripples can be recognized after processing five layers. The surface may start to be in transition from a smooth surface to a bumpy surface. After the process of the tenth layer (Fig. 6d) the formation of fine micro-grooves perpendicular to the ripples can be recognized. The surface is in transition from a smooth surface to a bumpy surface. This is consistent with the theoretical prediction that the transition to a bumpy surface should occur after processing eight to ten layers, see Fig. 5. This surface appearance is maintained also after the ablation of further layers, as shown by the image taken after the ablation of 20 layers given in Fig. 6e. The grooves have a periodicity of a few microns. When the number of processed layers is further increased to 50 (Fig. 6f) more pronounced grooves with a higher periodicity are formed.
Again, all surfaces shown in Fig. 6 were examined by means of a white-light interferometer to determine the mean roughness depth SRz. The results are listed in Table 2. The more layers were processed the larger is the resulting mean roughness depth. This is tantamount to rougher surfaces (see Fig. 6), and therefore, the mean roughness depth is a suitable parameter to describe the transitions from a smooth surface (covered only with ripples) to a bumpy surface.
The known fundamental equation describing the temperature increase caused by heat accumulation between consecutive heat inputs and 1D heat flow into the workpiece was used to develop a simple analytical model to calculate the temperature increase that occurs during materials processing with multiple parallel scanning passes (HAS-I) and the ablation of multiple layers (HAS-II). The model was shown to be consistent with the experimental findings by analyzing the resulting surface topography produced by laser processing. Modeling of situations with 2D or 3D heat flow would follow the same approach as outlined here just using the known corresponding 2D and 3D versions of the fundamental heat accumulation equations.
The explicit expressions depend on the applied scanning pattern, as illustrated by the additional example in the “Appendix”.
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This project has received funding from the European Union’s Horizon 2020 Research and Innovation Programme under Grant Agreement No. 687613.
The scanning strategy shown in Fig. 7a is characterized by alternating feed direction along the adjacent parallel paths and results in shorter positioning ways between two successive lines, and therefore, leads to a shorter total processing time as the example discussed above. When the considered point is located at the center of the processing lines, the time interval between the successive passes of the laser beam at this point is constant for the reason of symmetry. When leaving the center of the processing lines two different time intervals between two successive passes occur due to the asymmetric beam trajectory as indicated by Fig. 7b.
For parallel arranged lines with alternating feed direction, there can be two different processing times of a single pass (tshort and tlong) depending on the current processing line. Since both processing times of a single pass are repetitive, the chronical interval depends on the parity of the processing line. Defining rightwards passes where the laser beam moves from the left side to the right side as lines with even parity leads to the temperature increase ΔTHAS−I and can be expressed by
where N ∈ ℕ, and k ∈ ℕ.
For the sake of simplicity, we assume that every layer is processed with the same scanning strategy, hence without rotating the scanning pattern, with the same feed of the laser beam on the surface, and with the same process parameters. When tshort, tlong, and the number of lines M is known the time interval between two consecutive layers is tlayer = M \(\cdot\)(tshort + tlong)/2. For the scanning strategy shown in Fig. 7a the temperature increase caused during the ablation of the surface layer by laser yields
where K ∈ ℕ, N ∈ ℕ, and k ∈ ℕ.
The introduced model can be used to calculate the temperature increase due to heat accumulation for all scanning strategies that can be parameterized.
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Faas, S., Bielke, U., Weber, R. et al. Prediction of the surface structures resulting from heat accumulation during processing with picosecond laser pulses at the average power of 420 W. Appl. Phys. A 124, 612 (2018). https://doi.org/10.1007/s00339-018-2040-4