Stepped Spillways and Energy Dissipation: A Non-Uniform Step Length Approach

: A stepped spillway, which is deﬁned as a spillway with steps on the chute, can be used to improve the energy dissipation of descending water. Although uniform stepped spillways have been studied comprehensively, non-uniform stepped spillways need more attention. In the interest of maximum energy dissipation, in this study, non-uniform stepped spillways were investigated numerically. To this end, within the range of skimming ﬂow, four di ﬀ erent types of non-uniform step lengths, including convex, concave, random, and semi-uniform conﬁgurations, were tested in InterFOAM. To evaluate the inﬂuence of non-uniform step lengths on energy dissipation, the height and number of steps in all models were ﬁxed and equal to a constant number. The results indicated that in semi-uniform stepped spillways, when the ratio between the lengths of the successive steps is 1:3, a vortex interference region occurs within the two adjacent cavities of the entire stepped chute, and as a result, the energy dissipation increases by up to 20%. random aeration


Introduction
To prevent overtopping and possible failure of a dam, excess water in reservoirs is released by spillways. However, the released water, due to high kinetic energy, can cause erosion downstream [1][2][3]. In general, the effects of erosion are prevented by stilling basins, and hydraulic jumps are employed to protect the structures from erosion hazards [4,5]. The length of the stilling basin located at the foot of the spillway should be kept as short as possible to minimize construction costs. In order to achieve this goal, one possible solution is to consider stepped spillways instead of the traditional smooth spillways. A stepped spillway has a profile made up of steps on the chute, which increases the energy dissipation and in turn helps to reduce the required size of the stilling basin. The energy dissipation occurs by flow recirculation, with or without air entrainment, under the pseudo-bottom caused by the flow on each step [6,7]. Another important feature of stepped spillways is, because of the high turbulence of the flow and the absorbed air from the atmosphere, the risk of cavitation reduces [8][9][10].
The flow over a stepped spillway, with respect to the discharge rate, can be classified into three main regimes: Nappe flow for low discharge rates, skimming flow for higher discharge rates, and a transition regime that can be considered as the upper and lower boundaries of nappe and skimming flow, respectively. The flow regime can be affected by the channel slope and the spillway geometry, such as step height and length [11][12][13]. The amount of energy dissipation is directly related to the flow regime. The largest energy dissipation occurs under the nappe and transition flow regimes, however, these may cause flow instability [2]. Instable flows must be avoided as they can be dangerous due to causing unnecessary vibrations in the structures [11]. Therefore, in general, the hydraulic design of dams is based on the skimming flow regime [14][15][16].
For efficient design, the quantity of energy dissipation in stepped spillways, ∆E/E t , at the end of the stepped spillway is determined, where ∆E is the total head loss (∆E = E t − H res ) and E t is the maximum upstream head [2,16]. H res is the residual energy and can be calculated as: where C is the air concentration, y is measured perpendicular to the pseudo-bottom formed by the step edges, y 90 is the depth where the local C = 90%, and Z is the step edge elevation above the datum. Based on the uniform flow condition the amount of energy dissipation of the flow over a step can be calculated [3,15]. The uniform flow condition would imply a long chute with many steps, which may not be a typical form of stepped structure [13]. In the present study, due to the limited chute length, the energy dissipation was calculated in the absence of a uniform equilibrium flow condition.
The effect of the slope on energy dissipation for stepped spillways with uniform flat horizontal steps has been investigated, mostly by experimental studies [2,3,7,9,13,15,[17][18][19][20][21]. Experiments indicated that the energy loss due to the steps depends on the ratio of the critical flow depth (d c ) to the step height (h), and the number of steps, N. When the value of d c /h approaches one, near the limit of the skimming flow, the energy dissipation will be significantly affected by the stepped surface [22]. For higher values of d c /h, the effect of N becomes appreciable and at a certain d c /h, and the energy dissipation improves as N increases [13,22].
In the literature, there are few experimental studies that have focused on the flow over non-uniform stepped spillways. Stephenson [23] studied the energy dissipation on a stepped spillway with non-uniform step heights. He found an increase of 10% in the energy dissipation compared to uniform steps. On the other hand, Felder and Chanson [10,24] investigated the effect of uniform and non-uniform step heights on the energy dissipation performance, and showed that there was no significant difference between the two configurations. Li et al. [25] studied the energy dissipation due to non-uniform-height steps in curved spillways. Their results show that, compared to the smooth spillway, the water flow from the concave bank to the convex bank increased the energy dissipation by up to 66%.
In addition to these experimental studies, flow on stepped spillways have been modeled numerically with a high degree of accuracy using computational fluid dynamics (CFD). In numerical studies of stepped spillways, the flow over the stepped spillway is investigated by the volume of fluid (VOF) method, with turbulence closures of the k-ε family [26][27][28][29][30][31][32][33][34][35]. For instance, Wan et al. [36] have used VOF and the realizable k-ε model to determine the inception point of air entrainment in various stepped spillways, including flat steps, pooled steps, and round steps. Their results indicated that as the step height decreases, the air entrainment decreases, and with respect to aeration, the round stepped spillway was the optimum design.
The above mentioned experimental and numerical studies have investigated the energy dissipation of uniform stepped spillways for different slopes, numbers of steps, and discharges. In this study, the effect of non-uniform step length on the energy dissipation was investigated. To evaluate the performance of non-uniform step lengths on energy dissipation, the height and the number of steps in all models were fixed and equal to a constant number. Numerical analysis was performed by the InterFOAM solver in the OpenFOAM package, using the VOF method and the realizable k-ε model. The main aims of the presented study were: 1.
To investigate the effect of uniform step length on the energy dissipation for different slopes.

2.
To investigate the effect of non-uniform step length on the energy dissipation for four different cases: 3.
Longer steps in the beginning, with the step length decreasing progressively toward the end (convex configuration).

4.
Shorter steps in the beginning, with the step length increasing progressively toward the end (concave configuration). 5.
Random step length distribution 6.
Semi-uniform step length distribution 7.
Investigation of the optimum step length configuration with respect to energy dissipation.

Materials and Methods
One of the main features of a stepped spillway is the air entrainment that causes a two-phase flow. To analyze two-phase flows in OpenFOAM, VOF can be used where, for a fixed Eulerian mesh, based on each fluid fraction, all the variables in every volume are weighted. One of the advantages of the VOF method is that a simple fluid model can be developed using a single equation [26,28,37]. To this end, the continuity equation for the volume fraction of water can be presented as: where α w is the fraction of water and t is time. In the VOF model, as the water and air phases share the same velocity and pressure field, the two-phase flow can be considered as a single-phase flow, where the realizable k-ε turbulence is homogeneous. By solving Equation (2), the free surface of water can be determined. In all the computational cells, the α w and the fraction of air (α a ) is considered as: α a = 1 − α w , therefore, the density (ρ) and the molecular (µ) viscosity can be described as: where ρ w and ρ a are the density and µ w and µ a are the molecular viscosity of water and air, respectively. The maximum and minimum values of α w , one and zero, indicate that the given cell is filled entirely with water or air, respectively. With the help of the Reynolds-averaged Navier-Stokes (RANS) equations [38], a two-phase flow is described in terms of a single velocity and pressure field that can be solved by the InterFoam solver based on the VOF phase fraction.
∇.u = 0 (5) where u is the mean component of the velocities, ρ is the density, p* is the modified pressure, g and h * are the gravitational acceleration and position vectors, F is the volumetric surface tension force, µ e f f = (µ + µ t ), µ is the molecular viscosity, and µ t is the turbulence viscosity term, which can be calculated by the turbulent model. In order to model the flow over a stepped spillway by Equations (5) and (6), a turbulence closure is required. There are several turbulence closures available in the OpenFOAM toolbox (standard k-ε, realizable k-ε, RNG k-ε, standard-k-ω, SST-k-ω model, etc.). Herein, the performance of two common turbulence models, including the realizable k-ε and RNG k-ε, were numerically evaluated to determine which turbulence model is more applicable.
The realizable k-ε model is based on the two equations for k (turbulent kinetic energy) and ε (rate of viscous dissipation), respectively.
where G k and G b are the generation of turbulent kinetic energy by the mean velocity gradients and buoyancy, respectively, S is the strain rate tensor, S k and S ε are the source terms for the kinetic energy and dissipation rate, respectively, and σ k , σ ε , C 1 , C 2 , C 1ε , and C 3ε are the adjustable constants.
All the models that have been numerically investigated in this article are described in Tables 1  and 2. Table 1. Uniform configurations of the stepped spillways modelled in this study.
Step Height h(m) Step Length L(m)

Numerical Schemes
InterFoam uses the PIMPLE algorithm, a combination of the semi-implicit method for pressure-linked equations (SIMPLE) and the pressure-implicit with splitting of operators (PISO) algorithm, to solve the coupled system of equations in a segregated process utilizing an iterative sequence [39]. The convective terms within the momentum were discretized using the Gauss linear upwind method. The temporal term was discretized by a first-order implicit Euler scheme, while a Gauss linear corrected interpolation was used to discretize the Laplacian term [26].

Boundary Conditions
For all models investigated in this article, four boundary conditions were defined as follows: 1.
The water inflow boundary was set as a velocity-inlet condition and obtained based on the range of flow rates 1.1 ≤ d c /h ≤ 1.9. The term (d c /h) represents the ratio of the critical depth (d c ) to step height (h), in which critical depth is representative of the discharge.

2.
The outlet boundary condition was defined as an outlet pressure to allow the water flow out freely. 3. The walls were assumed to have a no-slip condition.

4.
As shown in Figure 1, the atmospheric pressure was considered at the free surface boundary. After validating the proposed numerical model by the experimental results obtained by Zhang and Chanson [40] and Felder [2], different uniform and non-uniform stepped spillways were investigated and, as shown in Figure 2, the optimized design was selected.

Mesh-Independence Test and Model Validation
The meshed domain was defined as a 2-D CFD model of flow over a stepped spillway. The meshes were created using the GMSH software. The grid convergence index (GCI) suggested by After validating the proposed numerical model by the experimental results obtained by Zhang and Chanson [40] and Felder [2], different uniform and non-uniform stepped spillways were investigated and, as shown in Figure 2, the optimized design was selected. After validating the proposed numerical model by the experimental results obtained by Zhang and Chanson [40] and Felder [2], different uniform and non-uniform stepped spillways were investigated and, as shown in Figure 2, the optimized design was selected.

Mesh-Independence Test and Model Validation
The meshed domain was defined as a 2-D CFD model of flow over a stepped spillway. The meshes were created using the GMSH software. The grid convergence index (GCI) suggested by Roache [41] was employed to ensure grid independence, and three different mesh types from dense

Mesh-Independence Test and Model Validation
The meshed domain was defined as a 2-D CFD model of flow over a stepped spillway. The meshes were created using the GMSH software. The grid convergence index (GCI) suggested by Roache [41] was employed to ensure grid independence, and three different mesh types from dense to coarse were tested. The mesh types were considered as: Mesh one with dimensions 0.0075 by 0.0075 m 2 , Mesh two with dimensions 0.01 by 0.01 m 2 , and Mesh three with dimensions 0.0133 by 0.0133 m 2 .
The grid refinement factor, which can be defined as r 21 = ∆h 2 /∆h 1 and r 32 = ∆h 3 /∆h 2 , where ∆h is a representative grid size, was 1.33, which is more than the recommended minimum value of 1.3 [42]. The water free surface and velocity profiles of the three mesh sizes mentioned here were compared with each other, and the results are shown in Figure 3. The grid refinement factor, which can be defined as r21 = Δh2/Δh1 and r32 = Δh3/Δh2, where Δh is a representative grid size, was 1.33, which is more than the recommended minimum value of 1.3 [42]. The water free surface and velocity profiles of the three mesh sizes mentioned here were compared with each other, and the results are shown in Figure 3.  In Figure 3c, the maximum GCI 21 at step six and step nine were 5.25% and 3.92%, respectively, corresponding to velocities of 2.697 m/s and 2.909 m/s, respectively. Along the whole spillway, the mean GCI 21 was less than 5%. As the results obtained from Mesh two and Mesh one were similar, to improve the modelling time, the grid size of Mesh two was selected. The proposed numerical model was validated through the experimental data obtained from Zhang and Chanson [40] by comparing the free surface profiles, velocity distribution, and energy dissipation. The physical model of Zhang and Chanson [40] is a large-size step spillway (1V:1H), with 12 steps with the height of 0.1 and the length of 0.1 m. The different volumetric flow rates were controlled by a broad crested weir.

Free Surface Profiles
A standard practice for the VOF approach is to determine the numerical water depth at the position where the volume fraction α = 0.5 [26]. As shown in Figure 4, for different values of discharge (0.008 ≤ Q ≤ 0.250 m 3 /s), the simulated water surface profiles over a broad-crested weir length (L crest ) are very similar to the experimental values.
Appl. Sci. 2019, 9, x 7 of 18 In Figure 3c, the maximum GCI21 at step six and step nine were 5.25% and 3.92%, respectively, corresponding to velocities of 2.697 m/s and 2.909 m/s, respectively. Along the whole spillway, the mean GCI21 was less than 5%. As the results obtained from Mesh two and Mesh one were similar, to improve the modelling time, the grid size of Mesh two was selected. The proposed numerical model was validated through the experimental data obtained from Zhang and Chanson [40] by comparing the free surface profiles, velocity distribution, and energy dissipation. The physical model of Zhang and Chanson [40] is a large-size step spillway (1V:1H), with 12 steps with the height of 0.1 and the length of 0.1 m. The different volumetric flow rates were controlled by a broad crested weir.

Free Surface Profiles
A standard practice for the VOF approach is to determine the numerical water depth at the position where the volume fraction α = 0.5 [26]. As shown in Figure 4, for different values of discharge (0.008 ≤ Q ≤ 0.250 m 3 /s), the simulated water surface profiles over a broad-crested weir length (Lcrest) are very similar to the experimental values.

Velocity Distribution
In Figure 5, a comparison of the velocity profiles between the experimental and numerical results at some longitudinal stations with different discharges by using the realizable k-ε and RNG k-ε models is shown. The results revealed that the realizable k-ε model is the most efficient. The same result was reported in the literature as well [26,30,43,44].

Velocity Distribution
In Figure 5, a comparison of the velocity profiles between the experimental and numerical results at some longitudinal stations with different discharges by using the realizable k-ε and RNG k-ε models is shown. The results revealed that the realizable k-ε model is the most efficient. The same result was reported in the literature as well [26,30,43,44].
Appl. Sci. 2019, 9, x 7 of 18 In Figure 3c, the maximum GCI21 at step six and step nine were 5.25% and 3.92%, respectively, corresponding to velocities of 2.697 m/s and 2.909 m/s, respectively. Along the whole spillway, the mean GCI21 was less than 5%. As the results obtained from Mesh two and Mesh one were similar, to improve the modelling time, the grid size of Mesh two was selected. The proposed numerical model was validated through the experimental data obtained from Zhang and Chanson [40] by comparing the free surface profiles, velocity distribution, and energy dissipation. The physical model of Zhang and Chanson [40] is a large-size step spillway (1V:1H), with 12 steps with the height of 0.1 and the length of 0.1 m. The different volumetric flow rates were controlled by a broad crested weir.

Free Surface Profiles
A standard practice for the VOF approach is to determine the numerical water depth at the position where the volume fraction α = 0.5 [26]. As shown in Figure 4, for different values of discharge (0.008 ≤ Q ≤ 0.250 m 3 /s), the simulated water surface profiles over a broad-crested weir length (Lcrest) are very similar to the experimental values.

Velocity Distribution
In Figure 5, a comparison of the velocity profiles between the experimental and numerical results at some longitudinal stations with different discharges by using the realizable k-ε and RNG k-ε models is shown. The results revealed that the realizable k-ε model is the most efficient. The same result was reported in the literature as well [26,30,43,44].

Energy Dissipation
For different volumetric flow rates within the range of 0.9 ≤ dc/h ≤ 1.7 the energy dissipation over a stepped chute was simulated. The results indicated energy dissipation of up to 60%. As can be seen in Figure 7, the numerically obtained results are very similar to the experimental results reported by Zhang and Chanson [16], indicating a high degree of accuracy of the proposed method.

Energy Dissipation
For different volumetric flow rates within the range of 0.9 ≤ dc/h ≤ 1.7 the energy dissipation over a stepped chute was simulated. The results indicated energy dissipation of up to 60%. As can be seen in Figure 7, the numerically obtained results are very similar to the experimental results reported by Zhang and Chanson [16], indicating a high degree of accuracy of the proposed method.

Energy Dissipation
For different volumetric flow rates within the range of 0.9 ≤ d c /h ≤ 1.7 the energy dissipation over a stepped chute was simulated. The results indicated energy dissipation of up to 60%. As can be seen in Figure 7, the numerically obtained results are very similar to the experimental results reported by Zhang and Chanson [16], indicating a high degree of accuracy of the proposed method.

Energy Dissipation
For different volumetric flow rates within the range of 0.9 ≤ dc/h ≤ 1.7 the energy dissipation over a stepped chute was simulated. The results indicated energy dissipation of up to 60%. As can be seen in Figure 7, the numerically obtained results are very similar to the experimental results reported by Zhang and Chanson [16], indicating a high degree of accuracy of the proposed method.  Furthermore, the proposed numerical model was tested by the experimental results for uniform and non-uniform stepped spillways reported by Felder [2]. As is shown in Figure 8 and Table 3, the proposed method has a high degree of accuracy and the numerically obtained results are very similar to the experimental ones.   Furthermore, the proposed numerical model was tested by the experimental results for uniform and non-uniform stepped spillways reported by Felder [2]. As is shown in Figure 8 and Table 3, the proposed method has a high degree of accuracy and the numerically obtained results are very similar to the experimental ones. Furthermore, the proposed numerical model was tested by the experimental results for uniform and non-uniform stepped spillways reported by Felder [2]. As is shown in Figure 8 and Table 3, the proposed method has a high degree of accuracy and the numerically obtained results are very similar to the experimental ones.

Uniform Stepped Spillways with Different Slopes
The effect of the spillway slope on the energy dissipation rate for all the configurations of uniform step length is discussed in this section. Figure 9 shows the water volume fraction of the flow, indicating recirculating flow in the step cavities. The results reveal that, as the step length increases, the air entrainment increases, which is simply caused by the increased length of the aerated flow region. It was observed that the rate of energy dissipation increases slightly when the spillway slope decreases, and this has an inverse relationship with the discharge (Figure 10). This can be explained by the formation of a recirculation flow at the step cavities, which creates large vortexes. For instance, for step lengths of 0.1, 0.15, and 0.2 m, a recirculation vortex fills the entire step cavities, acting as a roller and consequently conveying the flow. However, a part of this flow hits a step length which is larger than 0.2 m and generates a slight increase in the energy dissipation for slopes smaller than 1V:2H ( Figure 11). The flat slope 1V:2.2H yielded a slight increase in the energy dissipation by up to 1.3% compared to the slope 1V:2H, while the slope 1V:2.5 showed similar results against the flat slope 1V:2.2. Furthermore, the flat slopes 1V:3H and 1V:3.5 H yielded a slight increase in the energy dissipation by up to 2% compared to the slope 1V:2.2H, but the design would yield long and uneconomical designs. Among all uniform configurations tested here, the uniform stepped spillway with the 1V:2.2H slope was the optimum design in terms of the energy dissipation performance.
As shown in Figure 10 the results of energy dissipation for uniform configurations seem to have the same tendency. The energy dissipation is directly proportional to d c /h and can be estimated (R 2 > 0.94) by:

Non-Uniform Stepped Spillways
In this section, the effect of non-uniform step lengths on the energy dissipation for convex, concave, random, and semi-uniform configurations is discussed. The fraction of water flow over non-uniform configuration models investigated in this study can be seen in Figure 12. In the concave spillway, the extent of air entrainment was less in the water flow at the beginning of the steps and it increased towards the end of the chute, contrary to the convex spillway. The air entrainment in the concave configuration was larger compared to the convex configuration. The differences in the increase in the air entrainment could be explained by the flow disturbances resulting from an increase in the length of the steps toward the bottom of the spillway. In the random configurations, the air entrainment did not provide better aeration performance compared to uniform configurations.

Uniform Stepped Spillways with Different Slopes
The effect of the spillway slope on the energy dissipation rate for all the configurations of uniform step length is discussed in this section. Figure 9 shows the water volume fraction of the flow, indicating recirculating flow in the step cavities. The results reveal that, as the step length increases, the air entrainment increases, which is simply caused by the increased length of the aerated flow region.
(e) (f) It was observed that the rate of energy dissipation increases slightly when the spillway slope decreases, and this has an inverse relationship with the discharge (Figure 10). This can be explained by the formation of a recirculation flow at the step cavities, which creates large vortexes. For instance, for step lengths of 0.1, 0.15, and 0.2 m, a recirculation vortex fills the entire step cavities, acting as a roller and consequently conveying the flow. However, a part of this flow hits a step length which is larger than 0.2 m and generates a slight increase in the energy dissipation for slopes smaller than 1V:2H ( Figure 11). The flat slope 1V:2.2H yielded a slight increase in the energy dissipation by up to 1.3% compared to the slope 1V:2H, while the slope 1V:2.5 showed similar results against the flat slope 1V:2.2. Furthermore, the flat slopes 1V:3H and 1V:3.5 H yielded a slight increase in the energy dissipation by up to 2% compared to the slope 1V:2.2H, but the design would yield long and uneconomical designs. Among all uniform configurations tested here, the uniform stepped spillway with the 1V:2.2H slope was the optimum design in terms of the energy dissipation performance.

Non-Uniform Stepped Spillways
In this section, the effect of non-uniform step lengths on the energy dissipation for convex, concave, random, and semi-uniform configurations is discussed. The fraction of water flow over non-uniform configuration models investigated in this study can be seen in Figure 12. In the concave spillway, the extent of air entrainment was less in the water flow at the beginning of the steps and it increased towards the end of the chute, contrary to the convex spillway. The air entrainment in the concave configuration was larger compared to the convex configuration. The differences in the increase in the air entrainment could be explained by the flow disturbances resulting from an increase in the length of the steps toward the bottom of the spillway. In the random configurations, the air entrainment did not provide better aeration performance compared to uniform configurations.
(a) (b) The effect of non-uniform step length stepped spillways on the energy dissipation can be seen in Figure 13. Energy losses in the concave stepped spillway were approximately 9% more than the convex stepped spillway, and very similar to the uniform stepped spillway with the slope 1V:2.2H. For the concave spillway, a large vortex area occurs at the end of the lower half of the chute. The large vortex reduces the velocity, resulting in an increase of the energy dissipation. The small steps at the lower half of the convex spillway led to the formation of small vortices that contributed to a lower velocity reduction, resulting in less energy dissipation ( Figure 14). As shown in Figure 10 the results of energy dissipation for uniform configurations seem to have the same tendency. The energy dissipation is directly proportional to dc/h and can be estimated from

Non-Uniform Stepped Spillways
In this section, the effect of non-uniform step lengths on the energy dissipation for convex, concave, random, and semi-uniform configurations is discussed. The fraction of water flow over non-uniform configuration models investigated in this study can be seen in Figure 12. In the concave spillway, the extent of air entrainment was less in the water flow at the beginning of the steps and it increased towards the end of the chute, contrary to the convex spillway. The air entrainment in the concave configuration was larger compared to the convex configuration. The differences in the increase in the air entrainment could be explained by the flow disturbances resulting from an increase in the length of the steps toward the bottom of the spillway. In the random configurations, the air entrainment did not provide better aeration performance compared to uniform configurations. The effect of non-uniform step length stepped spillways on the energy dissipation can be seen in Figure 13. Energy losses in the concave stepped spillway were approximately 9% more than the convex stepped spillway, and very similar to the uniform stepped spillway with the slope 1V:2.2H. For the concave spillway, a large vortex area occurs at the end of the lower half of the chute. The large vortex reduces the velocity, resulting in an increase of the energy dissipation. The small steps at the lower half of the convex spillway led to the formation of small vortices that contributed to a lower velocity reduction, resulting in less energy dissipation ( Figure 14).   In the random configurations, the vortex generation and the dissipation process associated with each vortex are disturbed by the next step, and interfere with it if the ratio between the successive step lengths is greater than 1:2. As can be seen in Figure 14, the water velocity on the steps with a lower length of 0.1 m is approximately zero. The reduction of water movement has affected the energy dissipation significantly. It can also be noted that the random configurations one, two, and three showed similar results with respect to energy dissipation, and they did not provide a better performance compared to uniform configurations. On the contrary, the maximum energy dissipation was obtained with the semi-uniform configuration, which has alternate steps of lengths 0.1 and 0.3 m along the whole chute. It was observed that with this ratio, the vortex interference region was confined between two adjacent cavities on the entire chute, as shown in Figure 15, which, in turn, improved the energy dissipation. Compared with the best uniform configuration (1V:2.2H), the energy dissipation in the semi-uniform model was improved by 20%. In the random configurations, the vortex generation and the dissipation process associated with each vortex are disturbed by the next step, and interfere with it if the ratio between the successive step lengths is greater than 1:2. As can be seen in Figure 14, the water velocity on the steps with a lower length of 0.1 m is approximately zero. The reduction of water movement has affected the energy dissipation significantly. It can also be noted that the random configurations one, two, and three showed similar results with respect to energy dissipation, and they did not provide a better performance compared to uniform configurations. On the contrary, the maximum energy dissipation was obtained with the semi-uniform configuration, which has alternate steps of lengths 0.1 and 0.3 m along the whole chute. It was observed that with this ratio, the vortex interference region was confined between two adjacent cavities on the entire chute, as shown in Figure 15, which, in turn, improved the energy dissipation. Compared with the best uniform configuration (1V:2.2H), the energy dissipation in the semi-uniform model was improved by 20%.

Conclusions
Utilizing the optimal design of stepped spillways is essential for maximizing the energy dissipation and, consequently, reducing the construction costs of hydraulic structures. In this article, different stepped spillway configurations with uniform, non-uniform, and semi-uniform step lengths were studied numerically. The results indicated that the air entrainment increases as the step length increases. For concave and convex stepped spillways, it was observed that the amount of air concentration in the concave spillway is more than in the convex one. As a result, it can be considered that the concave stepped spillway is more effective than the convex one in terms of reducing the risk of cavitation. Moreover, it was observed that, among all models, the main factor that influences the energy dissipation is the vortexes formed by the recirculation flow. For the different uniform configurations investigated in this article, the uniform stepped spillway design with a slope of 1V:2.2H was found to be optimum in terms of the energy dissipation performance. However, over all the models, the semi-uniform chute performed better. The results indicated that the vortex generation and dissipation process associated with each vortex became confined between two adjacent cavities on the entire chute when the ratio between the successive step lengths was 1:3, such that the energy dissipation was improved by up to 20%.