2.1. Model requirements

We consider the following model requirements.

1. (i) The wall model should be able to account for different flow physics (e.g. laminar flow, wall-attached turbulence, separated flow) in a unified manner (i.e. the input and output structure of the model must be identical regardless of the case).

2. (ii) The model must be scalable to incorporate additional building-block flows if needed in future versions.

3. (ii) The model must provide a confidence score in the prediction at each point at the wall.

4. (iv) The model formulation must be directly applicable to complex geometries (e.g. realistic aircraft configuration) without any additional modifications. This requirement will constrain the allowable input variables and the parameters used for their non-dimensionalisation (i.e. they will need to be local in space).

5. (v) The model must account for the numerical errors of the schemes employed to integrate the LES equations. This implies that the input data used to train the model must be consistent with the data from the LES solver rather than from filtered DNS.

6. (vi) The inputs and outputs of the model must be given in non-dimensional form to comply with dimensional consistency.

7. (vii) The model must be invariant under constant space/time translations and rotations of the frame of reference.

8. (viii) The model must be Galilean invariant.

2.2. Model assumptions

The main modelling assumptions are as follows.

1. (i) There is a finite set of simple flows (referred to as building-block flows) that contains the essential flow physics to formulate generalisable wall models.

2. (ii) The effect of the (missing) near-wall SGS in WMLES of complex flows is representable by a linear combination of the near-wall behaviour of the building-block flows.

3. (iii) A set of $N$ non-dimensional model inputs based on local flow quantities is enough to discern among building-block flows, where $N$ is the minimum number of parameters characterising the building-block flow collection.

4. (iv) The non-dimensional form of the model inputs/outputs that provides the best predictive capabilities (i.e. interpolation/extrapolation between training cases) is obtained by scaling the variables with the kinematic viscosity and the distance to the wall.

5. (v) The flow information from two contiguous wall-normal locations is enough to predict the wall shear stress in the vicinity of those locations.

6. (vi) History effects for the SGS flow are captured using instantaneous accelerations without the need for additional information from past times.

Assumptions (i) and (ii) imply that the BFWM would provide accurate predictions as long as the (non-universal) large-scale flow motions are resolved by the WMLES grid, and the (smaller-scale) near-wall dynamics resemble the building-block flows or a combination of them. Assumption (iii) stems from the fact that the number of input variables to distinguish among different cases in the building-block flow collection must be, at least, equal to the number of non-dimensional groups required to characterise completely the wall shear stress across all the building-block flows. For the building-block flows chosen in this work, six parameters are needed to unambiguously identify the wall shear stress from one particular case (as will be discussed in § 2.3). These parameters are global quantities not available to the model. Instead, six non-dimensional inputs using local flow information are fed into the BFWM to predict the wall shear stress. However, there is no guarantee that these inputs can be used to discern among all possible building-block flows in a univocal manner at all times, and from there comes the need for assumption (iii).

In assumption (iv), it is assumed that the scaling proposed will be the best in all the flow scenarios that the model may encounter, which is not true in general. For example, the current scaling choice will not provide the best performance in the presence of strong compressibility effects, chemically reacting flows or multiphase flows.

Assumptions (v) and (vi) are adopted for the sake of model simplicity. The choice is informed by our previous work in Lozano-Durán & Bae (Reference Lozano-Durán and Bae2020), where a seven-point stencil was used for the input variables compared to the simpler, two-point stencil selected in the present work. It was noted that the seven-point stencil greatly complicated the model implementation without providing important benefits in terms of model performance. There are additional modelling assumptions that are not stated explicitly above. Nonetheless, points (i) to (vi) are the most critical assumptions affecting the model performance.

2.3. Building-block flows

Seven types of building-block flows are considered, and examples are shown in figure 2. All the cases entail an incompressible flow confined between two parallel walls, with the exception of the freestream flow. Cases with additional complexity, such as aerofoils, wings and bumps, are avoided intentionally. The rationale behind this choice is that the building blocks should encode the key flow physics to predict more complex scenarios. Hence we intend to avoid case overfitting, i.e. predicting the flow over a wing correctly merely because the model was also trained on similar wings instead of capturing the flow physics faithfully.

Figure 2.

Examples of building-block units taken as representative of different flow regimes: (a) freestream, (b) laminar channel flow, (c) turbulent channel flow, (d) turbulent Poiseuille–Couette flow for zero wall stress, (e) turbulent Poiseuille–Couette flow with a strong adverse mean pressure gradient, and ( f) turbulent channel flow with sudden imposition of spanwise mean pressure gradient.

For the building blocks, the streamwise, wall-normal and spanwise spatial coordinates are denoted by $x$, $y$ and $z$, respectively. The walls are separated by a distance $2h$. The density is $\rho$, and the dynamic and kinematic viscosities of the fluid are $\mu$ and $\nu$, respectively. In the following, we discuss the configuration and physical motivation behind each building block. We also include in parentheses the label for each building-block flow.

1. (1) Freestream (freestream). A uniform and constant velocity field is used as representative of freestream flows. The main role of this building-block flow is to identify near-wall regions with zero points per boundary layer thickness. In these situations, the BFWM applies a ZPG model (defined below) to estimate the wall stress. The prediction is accompanied by a low confidence score as there is not enough information to provide reliable predictions.

2. (2) Wall-bounded laminar flow (laminar). The near-wall region of a laminar flow is modelled using Poiseuille flow (i.e. parabolic mean velocity profile). The goal of this building block is to allow the prediction of the wall stress in wall-attached laminar scenarios. The case is characterised by the friction Reynolds number $Re_\tau = u_\tau h /\nu$, where $u_\tau$ is the friction velocity at the wall, and $h$ is the channel half-height. The range of Reynolds numbers considered is from $Re_\tau = 5$ to $Re_\tau =10^4$. A parabolic mean velocity profile is used to predict analytically the stress at the wall.

3. (3) Wall-bounded turbulence under zero mean pressure gradient (ZPG). Canonical wall turbulence without mean pressure gradient effects is modelled using turbulent channel flows as a building block. The wall stress predictions are provided by an ANN trained for $Re_\tau = 100$ to $Re_\tau =10\,000$ using numerical data (Lozano-Durán & Jiménez Reference Lozano-Durán and Jiménez2014a; Hoyas et al. Reference Hoyas, Oberlack, Alcántara-Ávila, Kraheberger and Laux2022).

4. (4) Wall-bounded turbulence under favourable/adverse mean pressure gradient and separation (FPG, APG and separation, respectively). We utilise the turbulent Poiseuille–Couette flow as a simplified representation of wall-bounded turbulence subject to favourable and adverse mean pressure gradient effects. The bottom wall is set at rest, and the top wall is set at a constant velocity equal to $U_t>0$. A streamwise mean pressure gradient, denoted by $\mathrm {d}P/\mathrm {d}\kern 0.06em x$, is applied to the flow. Favourable pressure gradient effects are obtained for values of $\mathrm {d}P/\mathrm {d}\kern 0.06em x$ accelerating the flow in the same direction as the top wall. Adverse pressure gradient conditions are achieved for values of $\mathrm {d}P/\mathrm {d}\kern 0.06em x$ that accelerate the flow in the direction opposite to that of the top wall. Flow separation is represented by values of $\mathrm {d}P/\mathrm {d}\kern 0.06em x$ at which the wall stress at the bottom wall is zero. The different flow regimes are characterised by the two Reynolds numbers $Re_P= \pm \sqrt {|\mathrm {d}P/\mathrm {d}\kern 0.06em x| / \rho }\,h/\nu$ and $Re_{U}= U_th/\nu$. The wall stress predictions are provided by an ANN trained for $Re_P$ from $-1.2 \times 10^3$ to $1.2 \times 10^3$, and $Re_{U}$ from $5 \times 10^3$ to $2 \times 10^4$. New DNS runs were conducted for these cases using the same numerical solver as in previous investigations by our group (Lozano-Durán, Hack & Moin Reference Lozano-Durán, Hack and Moin2018; Lozano-Durán & Bae Reference Lozano-Durán and Bae2019a).

5. (5) Statistically unsteady wall turbulence with three-dimensional mean flow (unsteady). The last building-block flow considered is a turbulent channel flow subject to a sudden spanwise mean pressure gradient $\mathrm {d}P/\mathrm {d}z$. The role of this case is to capture out-of-equilibrium effects due to strong unsteadiness and mean flow three-dimensionality, such as the decrease in the magnitude of the wall stress and the misalignment between the wall stress vector and mean shear vector. Only the initial transient of the flow, where non-equilibrium effects manifest, is considered. The different flow regimes are characterised by the streamwise friction Reynolds number $Re_\tau = u_{\tau } h /\nu$ before the imposition of $\mathrm {d}P/\mathrm {d}z$ and the ratio of streamwise to spanwise mean pressure gradients $\varPi = (\mathrm {d}P/\mathrm {d}z)/(\mathrm {d}P/\mathrm {d} x)$. The wall stress predictions are provided by an ANN trained for $Re_\tau = 100$ to $1000$ and $\varPi = 5$ to $100$ using data from Lozano-Durán et al. (Reference Lozano-Durán, Giometto, Park and Moin2020b).

The wall shear stress from each case in the building-block flow collection considered is determined completely by the specification of six parameters: $Re_\tau$ (or $Re_P$), $Re_U$, $\varPi$, $t u_\tau /h$ (non-dimensional time for unsteady cases), turbulent/non-turbulent flow, and laminar/freestream. Not all parameters are relevant for each case, yet they are required to avoid ambiguities.

The DNS database for ZPG, FPG, APG, separation and unsteady contains roughly 500 simulations. Figure 3 contains examples of the DNS mean velocity profiles for a selection of building-block flows. An advantage of the present building-block set-up is that it allows the generation of contiguous data from one flow regime to another without modifying the geometry, only varying the non-dimensional numbers defining the case (e.g. from FPG to ZPG to APG to separation by just changing the mean pressure gradient). This facilitates the generation of training data filling the non-dimensional space of inputs, which translates into a more reliable model. The latter is an important requirement, as the role of a model should be not fitting one particular dataset but learning the scaling of the non-dimensional inputs and outputs controlling the problem at hand.

Figure 3.

Mean velocity profiles for a selection of building-block flows. (a) Turbulent channel flows for (from left to right) $Re_\tau =180$, 550, 950, 2000, 4200 and 10 000 (ZPG). (b) Turbulent Poiseuille–Couette flows with favourable mean pressure gradient (FPG) at $Re_U=6500$ (dashed) for $Re_P=0$, 100, 150, 200, 250, 300 (from left to right), and $Re_U=22\,360$ (solid) for $Re_P= 0$, 380, 550, 750, 800, 1000 (from left to right). (c) Turbulent Poiseuille–Couette flows with adverse mean pressure gradient (APG) and separation at $Re_U=6500$ (dashed) for $Re_P=0$, $-$100, $-$150, $-$200, $-$250, $-$300 (from right to left) and $Re_U=22\,360$ (solid) for $Re_P= 0$, $-$380, $-$550, $-$750, $-$800, $-$1000 (from right to left). (d) Turbulent channel flows with the sudden imposition of spanwise mean pressure gradient for increasing time (from light to dark colour) for the streamwise (in blue) and spanwise (in red) mean velocity profiles at $Re_\tau =550$ (solid) and $Re_\tau =950$ (dashed) for $\varPi = 60$. In all cases, $u_{\tau,ZPG}$ is the friction velocity of the same case without adverse/favourable/spanwise mean pressure gradient.

2.4. Input and output variables

The input variables are acquired using a two-point stencil as shown in figure 1. The stencil contains the centre of the control volume attached to the wall (where the wall shear stress is to be predicted) and the second control volume off the wall along the wall-normal direction. Given that the model is intended to be used in complex geometries, the centres do not need to align perfectly along the wall-normal direction. This misalignment is considered during the model training. The information collected from the flow is

(2.1)\begin{equation} \{ u_1, u_2, \gamma_{12}, a_1, \dot\gamma_1, k_1 , k_{m1} \}, \end{equation}

where $u_1 = |\boldsymbol {u}_1|$ and $u_2=|\boldsymbol {u}_2|$ are the magnitude of the wall-parallel velocities relative to the wall at the first and second control volumes, respectively, $\gamma _{12}$ is the angle between $\boldsymbol {u}_1$ and $\boldsymbol {u}_2$, $a_1$ is the magnitude of the acceleration at the first control volume, $\dot \gamma _1$ is the time derivative of the angle of $\boldsymbol {u}_1$ in the wall-parallel direction, and $k_1$ and $k_{m1}$ are the turbulent kinetic energy and mean kinetic energy, respectively, at the first control volume and relative to the wall. The mean velocity to compute $k_1$ and $k_{m1}$ is obtained via an exponential average in time (denoted by $(\bar {\cdot })$) with time scale $10\varDelta /\sqrt {k_{m1}}$, where $\varDelta$ is the characteristic grid size based on the cube root of the control volume. The quantities predicted by the model are

(2.2)\begin{equation} \{\tau_w, \gamma_{1w}, p_{class}^i, p_{conf} \}, \end{equation}

where $\tau _w = |\boldsymbol { \tau }_w|$ is the magnitude of the wall stress vector, $\gamma _{1w}$ is the angle between $\boldsymbol {u}_1$ and $\boldsymbol { \tau }_w$, $p_{class}^i \in [0,1]$ for $i=1,\ldots,7$ is the probability of the flow corresponding to each building-block category, and $p_{conf} \in [0,1]$ is the model confidence score.

The input to the wall model comprises the non-dimensional groups formed by the set

(2.3)\begin{equation} \left\{ \frac{ u_1 y_1}{\nu} , \frac{ u_2 y_2}{\nu}, \gamma_{12}, \frac{a_1 y_1^3}{\nu^2}, \frac{{\dot{\gamma}}_{1} y_1^2}{\nu}, \frac{ k_1}{ k_{m1}} \right\}.\end{equation}

The model applies the exponential averaged $(\bar {\cdot })$ to the input variables, and this is accounted for in the training. The non-dimensional output of the wall model is

(2.4)\begin{equation} \left\{ \frac{\tau_w y_1}{\mu \bar u_1}, \gamma_{1w} , p_{class}^i, p_{conf} \right\}. \end{equation}

We have avoided explicitly the use of flow parameters such as freestream velocity and bulk velocity flow, as they are not identifiable unambiguously for arbitrary geometries.

The non-dimensional groups in (2.3) are devised to enable the classification and wall stress prediction according to the building-block flows considered. All the inputs contribute to the prediction of the outputs to some degree. However, it is possible to highlight the main role played by each input variable. The first two inputs, $u_1 y_1/\nu$ and $u_2 y_2/\nu$, represent the local Reynolds numbers at the first and second control volumes, respectively. They are key drivers for the prediction of the wall shear stress in all cases by detecting the shape of the mean velocity profile. They aid the distinction between turbulent channel flow, turbulence with favourable/adverse mean pressure gradient, and separation. The relative angle $\gamma _{12}$ is used to detect three-dimensionality in the mean velocity profile. The non-dimensional acceleration $a_1 y_1^3/\nu ^2$ and the angular rate of change $\dot {\gamma }_{1} y_1^2/\nu$ facilitate the prediction of the magnitude and direction of statistically unsteady effects in the wall shear stress. Finally, $k_1/k_{m1}$ is leveraged to discern between turbulent flows (ZPG, APG, FPG, etc.) and non-turbulent flows (freestream and laminar). The wall stress at the output is non-dimensionalised using the pseudo-wall-stress $\mu \bar u_1/y_1$, as it was found to minimise the spread of the data between cases. This scaling improved the generalisability of the model and facilitated learning the trends in the data by the ANNs.

2.5. WMLES with optimised SGS/wall model

The training data (discussed in § 2.6) are generated using WMLES with SGS/wall models optimised to obtain the exact values for the mean velocity profiles and wall stress distribution in order to attain consistency with the numerical discretisation and gridding strategy of the solver. This approach was preferred over filtered DNS data, as it is known that the SGS tensor in implicitly filtered LES ($\tau ^{SGS}_{ij}$) does not coincide with the Reynolds stress terms resulting from filtering the Navier–Stokes equations. The ambiguity in the filter operator renders DNS data inadequate for the development of SGS models because of inconsistent governing equations (Lund & Kaltenbach Reference Lund and Kaltenbach1995; Lund Reference Lund2003; Bae & Lozano-Durán Reference Bae and Lozano-Durán2017, Reference Bae and Lozano-Durán2018, Reference Bae and Lozano-Durán2022). This limitation is particularly relevant in the present work, as the typical grid sizes utilised in WMLES of external aerodynamics are orders of magnitude larger than the characteristic Kolmogorov length scale of the near-wall turbulence. Consequently, numerical errors are comparable to modelling errors, and the former must be accounted for in order to yield accurate predictions.

We introduce an exact-for-the-mean SGS (ESGS) model given by

(2.5)\begin{equation} \tau^{ESGS}_{ij} = \tau^{base}_{ij} + \Delta \tau^{SGS}_{ij}, \end{equation}

where $\tau ^{base}_{ij}$ is the SGS stress tensor provided by the baseline (imperfect) SGS model (in this case, the dynamic Smagorinsky model, albeit another model could have been selected), and $\Delta \tau ^{SGS}_{ij}$ is the SGS model correction such that the WMLES mean velocity profiles match the DNS counterparts. In this approach, instantaneous DNS flow fields are not needed, and neither is a specific LES filter shape. The correction $\Delta \tau ^{SGS}_{ij}$ is calculated on the fly as the instantaneous force $\partial \Delta \tau ^{SGS}_{ij}/\partial x_j$ required for $\langle u_i \rangle _{xz} = \langle u_i^{DNS} \rangle _{xzt}$, where $\langle {\cdot } \rangle _{xz}$ denotes average over the homogeneous directions $x$ and $z$, and $\langle u_i^{DNS} \rangle _{xzt}$ is the DNS mean velocity profile for the $i$th velocity component averaged over $x$, $z$ and $t$. If the DNS flow is not statistically stationary (e.g. the unsteady building-block flow), then the average is taken over $x$, $z$, and statistically equivalent realisations. At each wall-normal location, the force $\partial \Delta \tau ^{SGS}_{ij}/\partial x_j$ is calculated numerically as the value required in the right-hand side of the LES equations to match the DNS mean velocity profile in the next time step.

The boundary condition at the wall is also modified to reproduce the probability density function (p.d.f.) of the wall shear stress from DNS, and it is referred to as the exact boundary condition (EBC). This was achieved by using an inverse probability integral transform, which generates random numbers from an arbitrary probability distribution given its cumulative distribution function (Devroye Reference Devroye2006). During the runtime of WMLES with ESGS, random numbers are sampled from the uniform distribution and mapped onto the p.d.f. of the wall shear stress obtained previously from DNS. The process is performed for all wall locations at each time step.

WMLES of all the building-block flows was conducted using ESGS with EBC (hereafter, E-WMLES). The simulations were carried out in the same flow solver used later to implement the BFWM. This guarantees consistency of the training data with the actual numerical errors of the solver and gridding structure under the assumption of an SGS model able to predict accurately the mean velocity profiles.

2.6. E-WMLES training data, ANN architecture, and training method

Figure 4 offers an overview of the training workflow, which is divided into three steps.

Figure 4.

Overview of the training workflow for the BFWM. The details are discussed in § 2.6.

Step 1: generation of E-WMLES training database. The mean velocity profiles and the p.d.f.s of the wall shear stress from DNS are used to generate the training database using E-WMLES as described in § 2.5. The E-WMLES database comprises the building-block flows cases discussed in § 2.3 at isotropic grid resolutions $\varDelta = h/N$ with $N=5$, 10, 20, 40, 80, 160 and $380$, which cover (by a wide margin) the grid resolutions encountered in external aerodynamic applications. For grid resolutions finer than $\varDelta =h/380$, the BFWM was trained with DNS data to ensure convergence to the no-slip boundary condition. For each grid resolution, the E-WMLES data generated are time-resolved with a varying time step such that the Courant–Friedrichs–Lewy number is equal to 0.5. Time-resolved data were required to compute accelerations and time averages of the input variables that are representative of WMLES. The E-WMLES cases were run for 10 eddy-turnover times (defined by $h/u_\tau$). This time was sufficient to capture the statistical trends of the smallest flow scales in the E-WMLES, which have lifetimes of the order of $\varDelta /u_\tau$ (Lozano-Durán & Jiménez Reference Lozano-Durán and Jiménez2014b). It was found that reducing the time length of the training data below 3 eddy-turnover times significantly reduced the performance of the ANNs. The unsteady cases were simulated only for the period along which non-equilibrium effects are relevant (i.e. between 0.5 and 2 eddy-turnover times). Each E-WMLES contains of the order of 1000 to 10 000 snapshots, depending on the case. The training set was augmented by performing E-WMLES in which the $x$ direction (i.e. mean flow direction) was rotated parallel to the wall by $-45^\circ, -40^\circ, -35^\circ,\ldots,35^\circ, 40^\circ, 45^\circ$.

Step 2: training the ANN for the classifier. The classifier is trained using the full E-WMLES database and independently of the predictors. The classifier is an ANN with 5 hidden layers and 20 neurons per layer. The layers are connected with rectified linear units (ReLUs) as the activation function. The input to the classifier is the set of non-dimensional groups from (2.3). The last layer of the classifier is followed by the softmax activation function, which provides the probabilities of belonging to each building-block flow category ($p_{class}^i$, $i=1,\ldots,7$) such that $\sum p_{class}^i = 1$. The ANN weights and biases of the classifier are given by $\boldsymbol {w}_c = \mathrm {argmin}_{\boldsymbol {w}_c} \sum _{i=1}^7 \sum _{j=1}^N -p_{class,j}^{i,{true}} \log \left (p_{class,j}^{i,{predicted}}\right )$, where $N$ is the number of samples per category. The performance of the classifier after training is evaluated in figure 5, which shows the normalised confusion matrix. The diagonal of the matrix contains the percentages of inputs that are classified correctly, whereas off-diagonal values show the amount of misclassification among cases. The matrix shows that most samples are classified correctly. There are a few misclassifications (off-diagonal values) that are intentional to ensure a smooth transition between building blocks. This is caused by the overlap between contiguous building blocks, such as separation and strong APG, mild APG and ZPG, ZPG and mild FPG, and ZPG and unsteady. The only unintentional misclassification is the larger number of ZPG samples classified as FPG. However, this did not impact the performance of the BFWM, as the wall stress predictions for FPG and ZPG are comparable. Note that there is no ambiguity in the distinction between freestream/laminar and turbulent cases, which is important as their predictions vary considerably. A confidence score $p_{conf} \in [0,1]$ is inferred from the distance of the input to its nearest neighbour in the training set. In particular, the confidence is based on the ratio $d_s/d_i$ (clipped to be less than 1), where $d_i$ is the distance of the input to the closest sample in the training set, and $d_s$ is the average distance of the latter to its ten closest samples in the training set.

Figure 5.

Confusion matrix of the classifier. The categories are freestream (freestream), laminar channel flow (laminar), favourable mean pressure gradient wall turbulence (FPG), zero mean pressure gradient wall turbulence (ZPG), adverse mean pressure gradient wall turbulence (APG), separated turbulence (separation), and statistically unsteady wall turbulence (unsteady).

Step 3: five ANNs are trained, each dedicated to predicting one building-block flow, i.e. ZPG, APG, FPG, separation and unsteady. The ANN predictors are obtained via a deep feed-forward ANN with 5 hidden layers and 30 neurons per layer. The activation functions selected for the hidden layers are hyperbolic tangent sigmoid transfer functions and ReLU activation transfer functions. The ANN weights and biases of each predictor are given by $\boldsymbol {w}_p = \mathrm {argmin}_{\boldsymbol {w}_p} \|\boldsymbol {q}^{predicted} - \boldsymbol {q}^{true} \|$, where $\boldsymbol {q} = ( \tau _w y_1/\mu \bar u_1, \gamma _{1w} )$. Predictions of the ANN are calculated for each building-block category and added together, weighted by the probability of belonging to the $i$th category:

(2.6a,b)\begin{equation} \frac{\tau_w y_1}{\mu \bar u_1} = \sum_i p_{class}^i\, \frac{\tau_w^i y_1}{\mu \bar u_1}, \quad \gamma_{1w} = \sum_i p_{class}^i\,\gamma_{1w}^i, \end{equation}

where $\tau _w^i$ and $\gamma _{1w}^i$ are the predictions for the $i$th category. The process is illustrated in figure 6. The ANNs are trained using Bayesian regularisation back propagation by dividing the training data into two groups: the training set (80 % of the data) and the test set (20 % of the data). The test set includes full cases for Reynolds numbers (and $\varPi$ values) that are not part of the training set. This was found to improve the predictive capability of the network when interpolating and extrapolating among unseen cases. The errors from each training sample in the lost function were weighted to compensate for the different number of snapshots available for each case. Figure 7 shows the performance plot of the ANN trained for the unsteady building-block flow.

Figure 6.

Schematic of the predictor. The predictor consists of a collection of ANNs/analytical models specialised in predicting the wall shear stress of each building-block flow. The final output is the sum of the predictions from each building-block flow weighted by the probability of each category.

Figure 7.

Joint p.d.f. of the predicted output and actual output for (a) the magnitude of the wall stress $\widetilde {\tau _w}$, and (b) the relative angle $\widetilde {\gamma _{1w}}$. The tilde denotes values standardised by the mean and standard deviation of the training set. The results are for the statistically unsteady turbulent flow (unsteady).

For both the classifier and predictor, the inputs and outputs are standardised using the mean and the standard deviation of the training set. These values are stored as part of the model and used to standardise the inputs and outputs when the model is deployed. A parametric study was performed in terms of the number of layers and neurons per layer, and the present layouts were found to give a fair compromise between neural network complexity and predictive capabilities. Finally, it took roughly 12 h to train each ANN using 4 NVIDIA A100 with 40 GB of memory. The computational cost of the WMLES solver using the BFWM is between 1.1 and 1.3 times more expensive than the same WMLES solver using the algebraic equilibrium wall model from § 3.2. The particular cost depends on the number of boundary nodes the BFWM is applied to. However, no effort was devoted to optimise the current implementation of the BFWM.

3.1. Flow solver and grid generation

The simulations are conducted with the high-fidelity solver charLES developed by Cascade Technologies, Inc. (Bres et al. Reference Bres, Bose, Emory, Ham, Schmidt, Rigas and Colonius2018; Fu et al. Reference Fu, Karp, Bose, Moin and Urzay2021). The code integrates the compressible LES equations using a kinetic-energy-conserving, second-order-accurate, finite-volume method. The numerical discretisation relies on a flux formulation that is approximately entropy-preserving in the inviscid limit, thereby limiting the amount of numerical dissipation added into the calculation. The time integration is performed with a third-order Runge–Kutta explicit method.

The mesh generation follows a Voronoi hexagonal close-packed (HCP) point-seeding method, which automatically builds locally isotropic meshes for arbitrarily complex geometries. First, the watertight surface geometry is provided to describe the computational domain. Second, the coarsest grid resolution in the domain is set to uniformly seeded HCP points. Additional refinement levels are specified in the vicinity of the walls if needed. Ten iterations of Lloyd's algorithm smooth the transition between layers with different grid resolutions.

3.2. Traditional SGS/wall models

Two SGS models are considered: the dynamic Smagorinsky model (DSM; Germano et al. Reference Germano, Piomelli, Moin and Cabot1991) with the modification by Lilly (Reference Lilly1992), and the Vreman model (VREM; Vreman Reference Vreman2004). For the wall, we use a traditional equilibrium wall model (EQWM). The no-slip boundary condition at the wall is replaced by a wall stress boundary condition. The walls are assumed adiabatic, and the wall stress is obtained by an algebraic equilibrium wall model derived from the integration of the one-dimensional stress model along the wall-normal direction (Deardorff Reference Deardorff1970; Piomelli et al. Reference Piomelli, Ferziger, Moin and Kim1989):

(3.1)\begin{equation} u_{2}^+(y_\perp^+) =\begin{cases} y_\perp^+{+} a_1 (y_\perp^+)^2 & \text{for } y_\perp^+{<} 23, \\[5pt] \dfrac{1}{\kappa}\ln{y_\perp^+} + B & \text{otherwise}, \end{cases} \end{equation}

where $u_{2}$ is the model wall-parallel velocity at the second grid point off the wall, $y_\perp$ is the wall-normal direction to the surface, $\kappa =0.41$ is the Kármán constant, $B = 5.2$ is the intercept constant, and $a_1$ is computed to ensure $C^1$ continuity. The superscript $+$ denotes inner units defined in terms of wall friction velocity and $\nu$.

4.1. External versus internal wall-modelling errors

Two sources of errors can be identified in a wall model (Lozano-Durán et al. Reference Lozano-Durán, Bose and Moin2022): errors from the outer LES input data, referred to as external wall-modelling errors, and errors from the wall model physical assumptions, referred to as internal wall-modelling errors. In the former, errors by the SGS model at the matching locations propagate to the value of $\tau _w$ predicted by the wall model. These errors can be labelled as external to the wall model inasmuch as they are present even if the wall model provides an exact physical representation of the near-wall region. The second source of errors represents the intrinsic wall model limitations: even in the presence of exact values for the input data, the wall model might incur errors when the physical assumptions of the model do not hold. In the BFWM, internal errors may come from the inadequacy of the building-block flows to represent the physics of the near-wall region (e.g. compressibility effects, heat transfer effects, separation differing from the physics modelled by Poiseuille–Couette flows). A consequence of internal errors is that WMLES might not converge to the DNS solution with grid refinements until the grid is in the DNS-like regime when the contribution of the wall model is negligible. The combined external plus internal error is referred to as total error. We use ESGS-BFWM to isolate the internal wall-modelling errors when possible.

4.2. Laminar boundary layer

The set-up for the laminar boundary layer is the flow over a flat plate with zero mean pressure gradient and imposed inflow velocity from the Blasius solution. At the top boundary, the freestream velocity is $U_\infty$ and the vertical velocity is also calculated from the Blasius solution. A convective boundary condition is used at the outflow. The range of Reynolds numbers is from $Re_x = U_\infty L_0/\nu = 10^4$ to $Re_x = 10^6$, where $L_0$ is the distance of the inlet to the leading edge of the plate. The streamwise, wall-normal and spanwise sizes of the domain are $150 L_0$, $2 L_0$ and $1 L_0$, respectively. The grid resolution is uniform in the three directions, with $\varDelta /\delta _i \approx 1/2$ at the inlet, which corresponds to $\varDelta /\delta _o \approx 1/20$ at the outlet, where $\delta _i$ and $\delta _o$ are the boundary layer thicknesses based on 99 % of $U_\infty$ at the inlet and outlet, respectively. The reference solution was computed by DNS of the same set-up.

The streamwise mean velocity profiles are captured within 5 % error for DSM-EQWM, VREM-EQWM, DSM-BFWM and VREM-BFWM, as shown in figure 8(a). Figure 8(b) reveals that the flow is classified correctly as laminar with confidence near 100 %. The only exception is a small region close to the inlet, where the flow is labelled as freestream with lower confidence owing to the lack of grid resolution in that region (there are only two points per boundary layer thickness at the inlet). The internal wall model errors are included in figure 8(c), which shows a clear improvement in performance by the BFWM compared to the EQWM. After the initial transient from the inflow, errors for the BFWM are below 1 % and decay faster than errors for the EQWM, which are always above 20 %. The total wall stress error is evaluated in figure 8(d). The performance of the BFWM is still superior to that of the EQWM. However, the accuracy of the BFWM is severely diminished due to the external wall-modelling errors from the DSM and VREM. Figure 8(d) also reveals that the DSM-EQWM and VREM-EQWM are subjected to internal/external error cancellation (i.e. predictions may improve despite the fact that input values differ from ESGS). The degraded accuracy of the BFWM due to SGS model errors and the presence of error cancellation using the EQWM are recurrent observations in the following validation cases.

Figure 8.

Validation case: laminar boundary layer. (a) The streamwise mean velocity profiles at $x/L_0 = 1$, 11, 21, 31 and $41$ for the DSM-EQWM (blue squares), VREM-EQWM (blue crosses), DSM-BFWM (red squares), VREM-BFWM (red crosses), and DNS (solid line). The mean velocity profiles are shifted by $\Delta u/U_\infty = (x/L_0-1)/5$. (b) Dominant flow classification (solid blue) and confidence score (solid red) by the DSM-BFWM as a function of the streamwise distance. (c) Internal wall-modelling error of the wall stress prediction for the ESGS-BFWM (diamonds) and ESGS-EQWM (circles) as a function of the streamwise distance. (d) Total wall-modelling error for the DSM-EQWM (dashed line and squares), DSM-BFWM (solid line and squares), VREM-EQWM (dashed line and crosses), and VREM-BFWM (solid line and crosses) as a function of the streamwise distance.

4.3. Zero mean pressure gradient turbulent boundary layer

For the zero pressure gradient turbulent boundary layer case, the range of $Re_\theta$ for the turbulent boundary layer is from 800 to 2000, where $Re_\theta$ is the Reynolds number based on $U_\infty$ and the momentum thickness ($\theta$). The length, height and width of the simulated box are $L_x=1060\,\theta _{avg}$, $L_y=18\,\theta _{avg}$ and $L_z=35\,\theta _{avg}$, where $\theta _{avg}$ denotes $\theta$ averaged along the streamwise coordinate. The boundary conditions at the top plane are $u = U_\infty$, $w=0$, and $v$ is estimated from the known experimental growth of the displacement thickness for the corresponding range of Reynolds numbers as in Jiménez et al. (Reference Jiménez, Hoyas, Simens and Mizuno2010). This controls the average streamwise pressure gradient, whose nominal value is set to zero. The turbulent inflow is generated by the recycling scheme of Lund, Wu & Squires (Reference Lund, Wu and Squires1998), in which the velocities from a reference downstream plane, $x_{ref}$, are used to synthesise the incoming turbulence. The reference plane is located well beyond the end of the inflow region to avoid spurious feedback (Nikitin Reference Nikitin2007; Simens et al. Reference Simens, Jiménez, Hoyas and Mizuno2009). In our case, $x_{ref}/\theta _i = 890$, where $\theta _i$ is the momentum thickness at the inlet. A convective boundary condition is applied at the outlet with convective velocity $U_\infty$ (Pauley, Moin & Reynolds Reference Pauley, Moin and Reynolds1990) and small corrections to enforce global mass conservation (Simens et al. Reference Simens, Jiménez, Hoyas and Mizuno2009). The spanwise direction is periodic. The grid resolution is uniform in the three directions. Compared to the boundary layer thickness, the grid size is $\varDelta /\delta _i \approx 1/5$ at the inlet and $\varDelta /\delta _o \approx 1/20$ at the outlet. The reference DNS solution is from Towne et al. (Reference Towne2022), which follows an identical numerical set-up.

To facilitate the comparison between DNS and WMLES, we use as independent variables $Re_x$ and $x/L_0$, as these are free from modelling errors. The streamwise mean velocity profiles (figure 9a) deviate about 10–30 % from the DNS profile. The flow is classified correctly by the BFWM as ZPG with almost 100 % confidence across the vast majority of the domain (figure 9b). Close to the inlet, the flow is labelled as unsteady and APG, probably because it is still recovering from the artificial inlet boundary condition. From the inlet, the confidence first drops from 40 % to 20 %, and then recovers up to 100 %. In particular, the flow decelerates close to the inlet under an adverse mean pressure gradient, as seen in the classification of unsteady and APG. This condition is not contained explicitly in the training set. Therefore, the drop in confidence occurs because the input data to the model move far away from the input data in the training set. After the transient, the flow approaches equilibrium under zero mean pressure gradient, resembling a ZPG turbulent boundary layer. At this point, the flow is identified as ZPG and the confidence increases close to 100 %. The internal wall-modelling errors are quantified in figure 9(c), which shows moderate improvements in the performance of the BFWM compared to the EQWM. In particular, the averaged wall stress error is below 0.5 % for the BFWM and about 2 % for the EQWM once the effect of the inlet condition is forgotten. This case demonstrates that the BFWM is able to interpolate successfully among grid resolutions and Reynolds numbers. In terms of total wall stress error (figure 9d), the BFWM and EQWM exhibit comparable performance, with errors between 5 % and 15 %. Similar to the previous case, the accuracy of the BFWM worsens due to the external wall-modelling errors when the wall model is coupled with the DSM and VREM.

Figure 9.

Validation case: zero mean pressure gradient turbulent boundary layer. (a) The streamwise mean velocity profiles at $Re_x = 6\times 10^5$, $8\times 10^5$, $10\times 10^5$ and $12\times 10^5$, for the DSM-EQWM (blue squares), VREM-EQWM (blue crosses), DSM-BFWM (red squares), VREM-BFWM (red crosses) and DNS (solid line). The mean velocity profiles are shifted by $\Delta u / U_\infty = (x/L_0-1)/5$. (b) Dominant flow classification (solid blue) and confidence score (solid red) by the DSM-BFWM as a function of the streamwise distance. (c) Internal wall-modelling error of the wall stress prediction for the ESGS-BFWM (diamonds) and ESGS-EQWM (circles) as a function of the streamwise distance. (d) Total wall-modelling error for the DSM-EQWM (dashed line and squares), DSM-BFWM (solid line and squares), VREM-EQWM (dashed line and crosses) and VREM-BFWM (solid line and crosses) as a function of the streamwise distance.

4.4. Turbulent pipe flow at $Re_\tau =40\,000$

The next validation case is a turbulent pipe flow at $Re_\tau \approx 40\,000$ with reference data obtained from experiments by Baidya et al. (Reference Baidya, Baars, Zimmerman, Samie, Hearst, Dogan, Mascotelli, Zheng, Bellani and Talamelli2019). The flow is driven by a mean streamwise pressure gradient that fixes the Reynolds number based on the centreline velocity to the correct experimental value. The radial coordinate is $r$. The length of the pipe is $100R$, where $R$ is the radius of the pipe, and the streamwise direction is periodic. Four grid resolutions are considered: $\varDelta /R \approx 1/5$, $1/10$, $1/20$ and $1/40$.

Figure 10(a) shows that the streamwise mean velocity profiles for the DSM-BFWM and the VREM-BFWM approach the reference data with grid refinement. The flow is classified accurately as ZPG for all the grid resolutions (figure 10b). The BFWM correctly identifies the flow as ZPG with high confidence (>95 %) for $R/\varDelta >5$. For the coarsest grid ($R/\varDelta \approx 5$), the flow is also labelled as ZPG but with lower confidence (<60 %). The latter is the consequence of the poorer performance of the DSM in the coarsest grid resolution, which results in a near-wall mean shear lower than expected from the training set. The internal wall-modelling errors are shown in figure 10(c). Overall, both the BFWM and the EQWM perform satisfactorily, with errors below 5 % even at the coarsest grid resolution. This validation case demonstrates that the BFWM extrapolates successfully to high Reynolds numbers for different grid resolutions. The total wall stress error (figure 10d) ranges from 4 % to 12 % for the BFWM and the EQWM, regardless of the SGS model, with a mildly improved accuracy for the BFWM. The results also exhibit the non-monotonic convergence to the true solution typically observed for WMLES in the range of grid resolution considered. This effect, which remains a key issue of WMLES, can be ascribed to the interplay between numerical errors and SGS modelling errors as discussed in Lozano-Durán & Bae (Reference Lozano-Durán and Bae2019b) and Lozano-Durán et al. (Reference Lozano-Durán, Bose and Moin2022).

Figure 10.

Validation case: turbulent pipe flow at $Re_\tau =40\,000$. (a) The streamwise mean velocity profiles non-dimensionalised by the mean centreline velocity ($U_{cl}$) for the DSM-BFWM (squares) and VREM-BFWM (crosses) for $R/\varDelta \approx 5$ (blue), 10 (red) and 20 (yellow). The dashed line is the experimental mean velocity profile from Baidya et al. (Reference Baidya, Baars, Zimmerman, Samie, Hearst, Dogan, Mascotelli, Zheng, Bellani and Talamelli2019). (b) Dominant flow classification (solid blue) and confidence score (solid red) by the DSM-BFWM as a function of the grid resolution. (c) Internal wall-modelling error of the wall stress prediction for the ESGS-BFWM (diamonds) and ESGS-EQWM (circles) as a function of the grid resolution. (d) Total wall-modelling error for the DSM-EQWM (dashed line and squares), DSM-BFWM (solid line and squares), VREM-EQWM (dashed line and crosses) and VREM-BFWM (solid line and crosses) as a function of the grid resolution.

4.5. Adverse/favourable mean pressure gradient Poiseuille–Couette turbulence

Turbulent Poiseuille–Couette flows at $Re_U=14\,000$ are tested for adverse mean pressure gradients until separation and beyond for $Re_P\times 10^{-3} = -1.40$, $-$1.32, $-$1.23, $-$1.13, $-$1.02, $-$0.90, $-$0.76 and $Re_U= 14\,000$, and for favourable mean pressure gradients for $Re_P \times 10^{-3}= 1.02$, 1.13, 1.23, 1.32, 1.41, 1.49. In all cases, the mean streamwise pressure gradient ensures that the Reynolds number based on the centreline velocity matches the correct value. The grid resolution is $h/\varDelta = 10$. The reference solutions were obtained by DNS. It is worth remarking that these validation cases are not included in the training or testing set discussed in § 2.5. Hence the current cases assess the predictive capabilities of the BFWM when both $Re_P$ and $Re_U$ are varied simultaneously.

The results for APG/separation cases and FPG cases are shown in figures 11 and 12, respectively. There are noticeable deviations in the prediction of the mean velocity profiles for both the DSM-EQWM and the VREM-EQWM. Similar results are obtained for their BFWM counterparts. Nonetheless, the flow classification (figures 11b and 12b) is accurate, with a high confidence score (>90 %). The internal wall-modelling errors for APG/separation and FPG cases are shown in figures 11(c) and 12(c), respectively. For the APG/separation cases, we report the value of the wall shear stress (rather than the relative error) to avoid dividing by zero close to separation. The BFWM outperforms the EQWM for APG/separation cases, whereas ZPG cases are all predicted accurately by both wall models, with errors below 3 %. The total wall stress error for APG/separation and FPG cases is shown in figures 11(d) and 12(d), respectively. For APG/separation, the EQWM provides more accurate predictions than the BFWM, but these are subjected to error cancellation: the EQWM underpredicts the wall shear stress; however, the mean velocities close to the wall are overpredicted. The combination of both effects results in better predictions for the EQWM, but for the wrong reasons. For FPG, the total error rises from 5 % to 20 % for increasing favourable pressure gradient. This trend applies to both the BFWM and the EQWM, although the BFWM still outperforms the EQWM.

Figure 11.

Validation case: turbulent Poiseuille–Couette flow with adverse mean pressure gradient. (a) The streamwise mean velocity profiles non-dimensionalised by the mean centreline velocity ($U_{cl}^{ZPG}$) of the case with zero mean pressure gradient for the DSM-EQWM (blue squares), VREM-EQWM (blue crosses), DSM-BFWM (red squares) and VREM-BFWM (red crosses), for different $Re_P$. The dashed lines are mean velocity profiles from DNS. (b) Dominant flow classification (solid blue) and confidence score (solid red) by the DSM-BFWM as a function of the adverse pressure gradient $Re_P$. (c) Wall stress prediction in the absence of external errors for the ESGS-BFWM (diamonds) and ESGS-EQWM (circles) as a function of $Re_P$. (d) Total wall-stress prediction for the DSM-EQWM (dashed line and squares), DSM-BFWM (solid line and squares), VREM-EQWM (dashed line and crosses), and VREM-BFWM (solid line and crosses) as a function of $Re_P$. In (c) and (d), the wall-stress prediction is non-dimensionalised by the DNS wall stress for the case with zero mean pressure gradient.

Figure 12.

Validation case: turbulent Poiseuille-Couette flow with favourable mean pressure gradient. (a) The streamwise mean velocity profiles non-dimensionalised by the mean centreline velocity ($U_{cl}^{ZPG}$) of the case with zero mean pressure gradient for the DSM-EQWM (blue squares), VREM-EQWM (blue crosses), DSM-BFWM (red squares) and VREM-BFWM (red crosses), for different $Re_P$. The dashed lines are mean velocity profiles from DNS. (b) Dominant flow classification (solid blue) and confidence score (solid red) by the DSM-BFWM as a function of $Re_P$. (c) Internal wall-modelling error of the wall stress prediction for the ESGS-BFWM (diamonds) and ESGS-EQWM (circles) as a function $Re_P$. (d) Total wall-modelling error for the DSM-EQWM (dashed line and squares), DSM-BFWM (solid line and squares), VREM-EQWM (dashed line and crosses) and VREM-BFWM (solid line and crosses) as a function of $Re_P$.

4.6. Turbulent channel flow with the sudden imposition of spanwise pressure gradient

The last canonical validation case is a turbulent channel flow with the sudden imposition of a mean spanwise pressure gradient. The ratio of spanwise to streamwise mean pressure gradient is $\varPi = 80$. The grid resolution is $h/\varDelta = 10$. The simulation is started from a turbulent channel flow at a statistically steady state with $Re_\tau =700$ for $t<0$, and the lateral pressure gradient is imposed at time $t=0$.

Figures 13(a,b) show the history of the streamwise and spanwise mean velocity profiles for all cases. Predictions of the mean flow remain accurate within 5 % error for the second grid point off the wall. More acute errors are observed for the first grid point off the wall. The classifier detects accurately the change of regime from ZPG to unsteady at $t=0$ with high confidence (figure 13c). The internal wall-modelling errors for the streamwise ($\tau _{w,x}$) and spanwise ($\tau _{w,z}$) wall stresses are shown in figures 13(d,e), respectively. As expected, the BFWM performs better than the EQWM, with errors below 1 % for all times. Additionally, the BFWM is able to predict the mild drop in $\tau _{w,x}$ as a function of time, which is completely missed by the EQWM. A similar conclusion applies to the relative angle between $\boldsymbol {u}_1$ and $\boldsymbol {\tau }_w$ (namely, $\gamma _{1w}$). The BFWM predicts correctly the increase and decrease of $\gamma _{1w}$, whereas $\gamma _{1w}$ remains zero for the EQWM essentially by construction of the model. Finally, the BFWM still improves the predictions compared to the EQWM in terms of the total wall stress and $\gamma _{1w}$ errors (figures 13g–i), but with lower accuracy than before due to the presence of external wall-modelling errors.

Figure 13.

Validation case: turbulent channel flow sudden imposition of spanwise mean pressure gradient. (a) Streamwise and (b) spanwise mean velocity profiles non-dimensionalised by the centreline mean velocity at $t=0$ ($U_{cl}^{ZPG}$) for the DSM-EQWM (blue squares), VREM-EQWM (blue crosses), DSM-BFWM (red squares) and VREM-BFWM (red crosses), at $t u_\tau ^{ZPG}/h=0.01, 0.2,\ldots,0.9$, where $u_\tau ^{ZPG}$ is $u_\tau$ at $t=0$. The dashed lines are DNS mean velocity profiles (same for all following panels). (c) Dominant flow classification (solid blue) and confidence score (solid red) by the DSM-BFWM as a function of time. Internal wall-modelling error of the (d) streamwise and (e) spanwise wall stress predictions and ( f) relative angle between $\boldsymbol {u}_1$ and $\boldsymbol {\tau }_w$, for the ESGS-BFWM (diamonds) and ESGS-EQWM (circles) as a function of time. Total wall-modelling error for (g) streamwise wall stress, (h) spanwise wall stress, and (i) relative angle between $\boldsymbol {u}_1$ and $\boldsymbol {\tau }_w$, for the DSM-EQWM (dashed line and squares), DSM-BFWM (solid line and squares), VREM-EQWM (dashed line and crosses) and VREM-BFWM (solid line and crosses) as a function of time.

4.7. NASA Common Research Model High-lift

The NASA Common Research Model High-lift (CRM-HL) is a geometrically complex aircraft that includes the bracketry associated with deployed flaps and slats as well as a flow-through nacelle mounted on the underside of the wing. The simulations are performed in free air at Reynolds number 5.49 million based on the mean aerodynamic chord and freestream velocity. The freestream Mach number is 0.20. The results are compared with wind tunnel experimental data from Evans et al. (Reference Evans, Lacy, Smith and Rivers2020) corrected for free air conditions. Further details of the experimental set-up can be found in Lacy & Sclafani (Reference Lacy and Sclafani2016).

We follow the computational set-up from Goc et al. (Reference Goc, Lehmkuhl, Park, Bose and Moin2021). A semi-span aircraft geometry is simulated, and the symmetry plane is treated with free-slip and no-penetration boundary conditions. A uniform plug flow is used as the inlet. A non-reflecting boundary condition with specified freestream pressure is imposed at the outlet (Poinsot & Lelef Reference Poinsot and Lelef1992). The total number of grid points is 30 million, and the number of grid points per boundary layer thickness ranges from 0 to 20. The reader is referred to Goc et al. (Reference Goc, Lehmkuhl, Park, Bose and Moin2021) for more details about the gridding strategy. Figure 14 offers one example of the grid topology. The SGS model is the DSM, and we perform simulations for the DSM-EQWM and the DSM-BFWM. No ESGS model is available for comparison in this case. A summary of previous WMLES of the CRM-HL can be found in Kiris et al. (Reference Kiris, Ghate, Duensing, Browne, Housman, Stich, Kenway, Fernandes and Machado2022), using traditional SGS and wall models. Here, we re-run the simulations using the DSM-EQWM, and perform new simulations for the DSM-BFWM at angles of attack 7$^\circ$ and 19$^\circ$.

Figure 14.

Validation case: NASA Common Research Model High-lift. Geometry of the aircraft and an inset of the grid across the wing section.

The lift ($C_L$), drag ($C_D)$ and pitching moment ($C_M$) coefficients are shown in figure 15. It is worth remarking that the BFWM has never ‘seen’ an aircraft-like flow or been trained in a case that resembles an aerofoil or a wing. The DSM-BFWM provides moderate improvements with respect to the DSM-EQWM, especially close to the stall. The improvements are manifested more clearly in the pitching moment, which is a marker of the accuracy in the force distribution along the wing. The exception is $C_L$ at low angles of attack, where the DSM-EQWM outperforms the DSM-BFWM. However, it has been reported that the good predictions by the DSM-EQWM at low angles of attack are coincidental and due to error cancellation, so this should not be taken as a failure of the DSM-BFWM. Despite the improvements by the DSM-BFWM, the results suggest that a superior wall model alone does not suffice to further boost the performance of WMLES unless the SGS model is also improved accordingly.

Figure 15.

Validation case: NASA Common Research Model High-lift: (a) lift, (b) drag, and (c) pitching moment coefficients, as functions of the angle of attack (AoA) for the DSM-BFWM (red circles) and DSM-EQWM (blue circles). The dashed lines are experimental results.

Figure 16 shows the confidence map of BFWM over the surface of the aircraft. Two types of low-confidence (<20 %) regions are identified. The first region is located at the leading edges of the nacelle, slats and flaps, and is probably related to the lack of grid resolution in those locations (i.e. zero points per boundary layer thickness). The second low-confidence region is related to separation at the wing tip and close to the wing root. This may hint at a lack of grid resolution, the inadequacy of the building-block flows to model separation, or a combination of both. It is worth mentioning that confidence values of 20 % still indicate that the flow features detected resemble the building blocks up to some reasonable extent. For example, the presence of a completely unknown flow (i.e. random values of the model inputs) will result in confidence scores of 0 %. The confidence map is a key feature of the BFWM that enables further evaluation of the model performance. As such, the information from figure 16 might aid grid refinement in poor-confidence regions and/or inform future developments of the model, for example, by suggesting alternative building-block flows or the necessity for new ones.

Figure 16.

Validation case: NASA Common Research Model High-lift. Visualisation of the instantaneous wall shear stress (left) and confidence map (right) by the DSM-BFWM.

4.8. NASA Juncture Flow experiment

The NASA Juncture Flow experiment consists of a full-span wing–fuselage body configured with truncated DLR-F6 wings and has been tested in the Langley 14 feet by 22 feet Subsonic Tunnel. The case has been proposed as a validation experiment for generic wing–fuselage junctions at subsonic conditions (Rumsey et al. Reference Rumsey, Carlson and Ahmad2019). The Reynolds number is $Re=L U_\infty /\nu =2.4$ million, where $L$ is the chord at the Yehudi break. We consider an angle of attack of $5^\circ$. The experimental dataset comprises a collection of local-in-space time-averaged measurements (Kegerise et al. Reference Kegerise, Neuhart, Hannon and Rumsey2019), such as velocity profiles and Reynolds stresses, which aid the validation of the BFWM in more detail. The frame of reference is such that the fuselage nose is located at $x = 0$, the $x$-axis is aligned with the fuselage centreline, the $y$-axis denotes the spanwise direction, and the $z$-axis is the vertical direction. The associated instantaneous velocities are denoted by $u$, $v$ and $w$.

The SGS model is the DSM, and we perform simulations for the DSM-EQWM and the DSM-BFWM. We use a boundary-layer-conforming grid (Lozano-Durán et al. Reference Lozano-Durán, Bose and Moin2022), such that the control volumes are distributed to achieve five points per boundary layer thickness. Figure 17 contains a visualisation of Voronoi control volumes for the boundary-layer-conforming grid. The reader is referred to Lozano-Durán et al. (Reference Lozano-Durán, Bose and Moin2022) for an in-depth description of the computational set-up, numerical methods and grid generation.

Figure 17.

Validation case: NASA Juncture Flow experiment. Visualisation of Voronoi control volumes for boundary-layer-conforming grid with five points per boundary layer thickness.

The prediction of the mean velocity profiles is shown in figure 18 and compared with experimental measurements. Three locations are considered: the upstream region of the fuselage, the wing–body juncture, and the wing–body juncture close to the trailing edge. Table 1 contains information about the flow classification and confidence in the solution at each location. In the first region, the flow resembles a ZPG turbulent boundary layer. Hence the DSM-EQWM and the DSM-BFWM perform accordingly (i.e. errors below 2 %). The flow is identified by the BFWM as 88 % ZPG and 12 % FPG with $98\,\%$ confidence. The outcome is expected as the BFWM was trained in turbulent channel flows, and the boundary layer at the fuselage resembles a ZPG.

Figure 18.

Validation case: NASA Juncture Flow experiment. The mean velocity profiles at (a) the upstream region of the fuselage at $x=1168.4$ mm and $z=0$ mm, (b) the wing–body juncture at $x=2747.6$ mm and $y=239.1$ mm, and (c) the wing–body juncture close to the trailing edge at $x=2922.6$ mm and $y=239.1$ mm. Solid lines with open symbols are for the DSM-EQWM, and closed symbols are for the DSM-BFWM. Dashed lines are experiments. Colours denote different velocity components. The distances $y$ and $z$ are normalised by the local boundary layer thickness $\delta$ at each location.

Table 1.

Validation case: NASA Juncture Flow experiment. The flow classification and confidence in the solution by the BFWM. The locations are (a) upstream region of the fuselage, (b) wing–body juncture, and (c) wing–body juncture close to the trailing edge.

There is a decline in accuracy by the DSM-EQWM in the wing–body juncture and trailing-edge region, which are dominated by adverse pressure gradient effects in the corner and flow separation at the trailing edge. Lozano-Durán et al. (Reference Lozano-Durán, Bose and Moin2022) have shown that not only does the DSM-EQWM exhibit larger errors in the wing–body juncture and trailing-edge region, but the rate of convergence of the DSM-EQWM by merely refining the grid is too slow to compensate for the modelling deficiencies at a reasonable computational cost.

The DSM-BFWM provides better predictions in the juncture location compared to the DSM-EQWM. The main reason for the improved results comes from the augmentation of the wall stress compared to the EQWM. This effect accumulates along the streamwise direction, decelerating the flow and alleviating the overprediction of $u$ and $w$ observed with the EQWM. The flow in the juncture is classified as 52 % APG and 41 % ZPG, which shows that the increase in accuracy is due mostly to the use of the APG building-block flow. The confidence in the prediction is above 80 %.

The performance of the DSM-BFWM in the separated region is also improved compared to the DSM-EQWM, but it is still far from satisfactory. The DSM-BFWM classifies the flow as a mix of ZPG, APG and separation, the latter being the most dominant class (56 %). The improvements with respect to the EQWM are caused not only by the use of the APG and separation building-block flows, but also by the improved streamwise history of the flow discussed above. Interestingly, the model prompts a warning about its potential poor performance, which is evidenced by the low confidence ($\sim$20 %) in the wall-stress prediction. The deficient performance of the DSM-BFWM and the DSM-EQWM is not surprising if we note that the separation zone has wall-normal thickness 0.3$\delta$ (with $\delta$ the boundary layer thickness), whereas the WMLES grid size is $\varDelta \approx 0.2\delta$. Thus there is only one grid point across the separation bubble. Despite the fact that the model was trained in separated flows, the external SGS model errors dominate the LES solution in this case. These errors hinder the capability of the BFWM to classify and predict the flow correctly. Nonetheless, the improvements from the BFWM and its ability to assess the confidence in the prediction is a competitive advantage with respect to traditional wall models.

Simulations of the NASA Juncture Flow experiment were also performed by Lozano-Durán & Bae (Reference Lozano-Durán and Bae2020) using a preliminary version of the BFWM trained with filtered DNS data and a smaller collection of building-block flows. The current version of the BFWM provides higher accuracy in the predictions compared to Lozano-Durán & Bae (Reference Lozano-Durán and Bae2020) because of the enhanced collection of building-block flows and the consistency with the numerical scheme of the flow solver.